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Search Results (436)

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27 pages, 2758 KiB  
Review
A Review of SAW-Based Micro- and Nanoparticle Manipulation in Microfluidics
by Débora Amorim, Patrícia C. Sousa, Carlos Abreu and Susana O. Catarino
Sensors 2025, 25(5), 1577; https://doi.org/10.3390/s25051577 - 4 Mar 2025
Viewed by 142
Abstract
Surface acoustic wave (SAW)-based microfluidics has emerged as a promising technology for precisely manipulating particles and cells at the micro- and nanoscales. Acoustofluidic devices offer advantages such as low energy consumption, high throughput, and label-free operation, making them suitable for particle manipulation tasks [...] Read more.
Surface acoustic wave (SAW)-based microfluidics has emerged as a promising technology for precisely manipulating particles and cells at the micro- and nanoscales. Acoustofluidic devices offer advantages such as low energy consumption, high throughput, and label-free operation, making them suitable for particle manipulation tasks including pumping, mixing, sorting, and separation. In this review, we provide an overview and discussion of recent advancements in SAW-based microfluidic devices for micro- and nanoparticle manipulation. Through a thorough investigation of the literature, we explore interdigitated transducer designs, materials, fabrication techniques, microfluidic channel properties, and SAW operational modes of acoustofluidic devices. SAW-based actuators are mainly based on lithium niobate piezoelectric transducers, with a plethora of wavelengths, microfluidic dimensions, and transducer configurations, applied for different fluid manipulation methods: mixing, sorting, and separation. We observed the accuracy of particle sorting across different size ranges and discussed different alternative device configurations to enhance sensitivity. Additionally, the collected data show the successful implementation of SAW devices in real-world applications in medical diagnostics and environmental monitoring. By critically analyzing different approaches, we identified common trends, challenges, and potential areas for improvement in SAW-based microfluidics. Furthermore, we discuss the current state-of-the-art and opportunities for further research and development in this field. Full article
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Figure 1
<p>Example of a SAW-based microfluidic device for cell sorting. Adapted from [<a href="#B11-sensors-25-01577" class="html-bibr">11</a>], PNAS, under a Creative Commons Attribution (CC BY) license.</p>
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<p>(<b>a</b>) Schematics of an interdigitated transducer (IDT), showing the relation between the finger pairs and the wavelength of the resulting surface acoustic wave (SAW). (<b>b</b>) A typical SAW device, with the IDT patterned on the surface of the piezoelectric substrate. Reproduced from [<a href="#B30-sensors-25-01577" class="html-bibr">30</a>] with permission from Nature.</p>
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<p>Scheme of different IDT designs: (<b>a</b>) single electrode; (<b>b</b>) floating electrode; (<b>c</b>) chirped; (<b>d</b>) slanted; (<b>e</b>) focused.</p>
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<p>Schematic representation of a cross-sectional view of the two operation modes of SAW microfluidic devices. (<b>a</b>) Traveling SAW operation mode. (<b>b</b>) Standing SAW operation mode. Adapted from [<a href="#B23-sensors-25-01577" class="html-bibr">23</a>] with permission from Nature.</p>
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<p>Manipulation of fluorescent polystyrene beads. (<b>a</b>) 1D manipulation; (<b>b</b>) 2D manipulation; (<b>c</b>) microbead experimental patterning (1D); (<b>d</b>) microbead experimental patterning (2D). Reprinted with permission from [<a href="#B41-sensors-25-01577" class="html-bibr">41</a>] Copyright 2009, Royal Society of Chemistry.</p>
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<p>Schematic of a cross-sectional view of the SSAW microfluidic device, highlighting the forces acting within the system. The substrate generates Rayleigh waves, which induce both longitudinal and transverse motions. These motions give rise to acoustic streaming (depicted by red arrows) and the acoustic radiation force (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>F</mi> </mrow> <mrow> <mi>R</mi> </mrow> </msub> </mrow> </semantics></math> represented by green arrows). Blue dots indicate the pressure nodes, where the acoustic pressure amplitude is minimal, while red dots represent the pressure antinodes, where the acoustic pressure amplitude is maximal. Adapted from [<a href="#B59-sensors-25-01577" class="html-bibr">59</a>], PNAS, under a Creative Commons Attribution (CC BY) license.</p>
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<p>Schematic representation of different configurations of SAW-based microfluidic devices. (<b>a</b>) A SSAW-based device, for separation, with single electrode IDTs and a microfluidic channel with 3 inlets and 3 outlets. Reprinted from [<a href="#B13-sensors-25-01577" class="html-bibr">13</a>], American Chemical Society, under a Creative Commons Attribution (CC BY) license. (<b>b</b>) A device using SSAWs for concentration and TSAWs for separation. TSAWs are generated alternately by the focused IDTs on both sides of the channel. Adapted from [<a href="#B10-sensors-25-01577" class="html-bibr">10</a>], with permission from Elsevier. (<b>c</b>) A tilted-angle SSAW device for separation. Adapted from [<a href="#B42-sensors-25-01577" class="html-bibr">42</a>], American Chemical Society, under a Creative Commons Attribution (CC BY) license. (<b>d</b>) A SSAW-based device for 3D manipulation with two pairs of single-electrode IDTs arranged orthogonally to each other. Adapted from [<a href="#B59-sensors-25-01577" class="html-bibr">59</a>], PNAS, under a Creative Commons Attribution (CC BY) license. (<b>e</b>) A device with two slanted IDTs to generate TSAWs and manipulate a static sample. Adapted from [<a href="#B16-sensors-25-01577" class="html-bibr">16</a>], American Association for the Advancement of Science, under a Creative Commons Attribution (CC BY) license.</p>
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19 pages, 12391 KiB  
Article
Investigation into Enhancing Ultrasonic Cleaning Efficiency Through Symmetrical Transducer Configuration
by Lei Wei, Sheng Liu and Fang Dong
Symmetry 2025, 17(3), 348; https://doi.org/10.3390/sym17030348 - 25 Feb 2025
Viewed by 184
Abstract
This paper investigates the symmetrical layout effect in ultrasonic cleaning via acoustic solid coupling simulation, with emphasis on how the symmetrical arrangement of transducers influences sound pressure distribution. Two specific transducer layout methods are examined: uniform arrangement at the bottom and symmetrical arrangement [...] Read more.
This paper investigates the symmetrical layout effect in ultrasonic cleaning via acoustic solid coupling simulation, with emphasis on how the symmetrical arrangement of transducers influences sound pressure distribution. Two specific transducer layout methods are examined: uniform arrangement at the bottom and symmetrical arrangement along the sides. The findings indicate that when the tank length is an integer multiple of one-quarter of the acoustic wavelength, the symmetrical side arrangement markedly enhances the sound pressure level within the tank and optimizes the propagation and reflection of acoustic waves. In megasonic cleaning, focusing is achieved through a 7 × 7 transducer array by precisely controlling the phase, and the symmetrical arrangement ensures uniform sound pressure distribution. By integrating 1 MHz megasonic sources from both focused and unfocused configurations, the overall sound pressure distribution and peak sound pressure at the focal point are calculated using multi-physics field coupling simulations. A comparative analysis of the sound fields generated by focused and unfocused sources reveals that the focused source can produce significantly higher sound pressure in specific regions. Leveraging the enhanced cleaning capability of the focused acoustic wave in targeted areas while maintaining broad coverage with the unfocused acoustic wave significantly improves the overall cleaning efficiency. Ultrasonic cleaning finds extensive applications in industries such as electronic component manufacturing, medical device sterilization, and automotive parts cleaning. Its efficiency and environmental friendliness make it highly significant for both daily life and industrial production. Full article
(This article belongs to the Section Engineering and Materials)
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<p>Schematic diagram of acoustic cavitation collapse.</p>
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<p>Shows the evolution process of a single bubble radius under the influence of an acoustic field (<b>a</b>) Different radii (<b>b</b>) Theoretical simulation comparison (<b>c</b>) Different sound pressures (<b>d</b>) Resonant frequency.</p>
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<p>(<b>a</b>) Aluminum foil corrosion test results [<a href="#B29-symmetry-17-00348" class="html-bibr">29</a>] (<b>b</b>) Two types of ultrasonic cleaning models.</p>
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<p>Model of the flow field diagram.</p>
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<p>The thickness of the boundary layer decreases as the frequency increases [<a href="#B30-symmetry-17-00348" class="html-bibr">30</a>] (<b>a</b>) Acoustic boundary layer (<b>b</b>) Thickness of acoustic boundary layer.</p>
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<p>Megasonic cleaning [<a href="#B25-symmetry-17-00348" class="html-bibr">25</a>].</p>
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<p>Comparison before and after cleaning [<a href="#B25-symmetry-17-00348" class="html-bibr">25</a>]. (<b>a</b>) Ultrasonic cleaning. (<b>b</b>) Megasonic cleaning.</p>
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<p>(<b>a</b>) Unfocused megasonic source (Model a) (<b>b</b>) Focused megasonic source (Model b).</p>
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<p>Non-focused sound sources combined with focused sound sources (<b>a</b>) Model c (<b>b</b>) Model d.</p>
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<p>The distribution of the sound pressure and sound pressure level at 40 kHz (<b>a</b>) Model 1 (<b>b</b>) Model 2 (<b>c</b>) Model 3.</p>
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<p>The pressure exerted on the silicon wafers in the cleaning tank. (<b>a</b>) Model 1 (<b>b</b>) Model 2. (<b>c</b>) Model 3.</p>
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<p>The distribution of the sound pressure and sound pressure level on the horizontal cross section.</p>
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<p>Sound pressure distribution (<b>a</b>) Model a (<b>b</b>) Model b.</p>
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<p>The distribution of the cross-sectional sound pressure and the values of sound pressure along the cross-sectional line (<b>a</b>) Model a (<b>b</b>) Model b.</p>
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<p>The pressure exerted on the silicon wafer (<b>a</b>) Model a (<b>b</b>) Model b.</p>
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<p>Sound pressure distribution (<b>a</b>) Model c (<b>b</b>) Model d.</p>
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<p>The distribution of the cross-sectional sound pressure and the values of the sound pressure along the cross-sectional line (<b>a</b>) Model c (<b>b</b>) Model d.</p>
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<p>The pressure exerted on the silicon wafe (<b>a</b>) Model c (<b>b</b>) Model d.</p>
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22 pages, 2998 KiB  
Review
Recent Advances in AlN-Based Acoustic Wave Resonators
by Hao Lu, Xiaorun Hao, Ling Yang, Bin Hou, Meng Zhang, Mei Wu, Jie Dong and Xiaohua Ma
Micromachines 2025, 16(2), 205; https://doi.org/10.3390/mi16020205 - 11 Feb 2025
Viewed by 627
Abstract
AlN-based bulk acoustic wave (BAW) filters have emerged as crucial components in 5G communication due to their high frequency, wide bandwidth, high power capacity, and compact size. This paper mainly reviews the basic principles and recent research advances of AlN-based BAW resonators, which [...] Read more.
AlN-based bulk acoustic wave (BAW) filters have emerged as crucial components in 5G communication due to their high frequency, wide bandwidth, high power capacity, and compact size. This paper mainly reviews the basic principles and recent research advances of AlN-based BAW resonators, which are the backbone of BAW filters. We begin by summarizing the epitaxial growth of single-crystal, polycrystalline, and doped AlN films, with a focus on single-crystal AlN and ScAlN, which are currently the most popular. The discussion then extends to the structure and fabrication of BAW resonators, including the basic solidly mounted resonator (SMR) and the film bulk acoustic resonator (FBAR). The new Xtended Bulk Acoustic Wave (XBAW) technology is highlighted as an effective method to enhance filter bandwidth. Hybrid SAW/BAW resonators (HSBRs) combine the benefits of BAW and SAW resonators to significantly reduce temperature drift. The paper further explores the application of BAW resonators in ladder and lattice BAW filters, highlighting advancements in their design improvements. The frequency-reconfigurable BAW filter, which broadens the filter’s application range, has garnered substantial attention from researchers. Additionally, optimization algorithms for designing AlN-based BAW filters are outlined to reduce design time and improve efficiency. This work aims to serve as a reference for future research on AlN-based BAW filters and to provide insight for similar device studies. Full article
(This article belongs to the Special Issue RF and Power Electronic Devices and Applications)
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<p>Single-crystal AlN and its epitaxial growth. (<b>a</b>) Graphical illustration of growth process under different growth temperatures [<a href="#B27-micromachines-16-00205" class="html-bibr">27</a>]. Step (1) is Wafer surface cleaning; Step (2) is GaN nucleation layer; Step (3) is GaN growth; Step (4) is AlN growth. This image has been obtained with permission from IEEE Publishing. (<b>b</b>) Schematic using the epitaxial AlN layer as a sputtering template to grow the single-crystal AlN substrate. Adapted from [<a href="#B29-micromachines-16-00205" class="html-bibr">29</a>].</p>
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<p>Properties and preparation of doped AlN. (<b>a</b>) TCF of Sc<sub>x</sub>Al<sub>1−x</sub>N films as a function of Sc concentration (x) [<a href="#B30-micromachines-16-00205" class="html-bibr">30</a>]. This image has been obtained with permission from IEEE Publishing. (<b>b</b>) Method for depositing c-axis zig-zag ScAlN multilayers. Adapted from [<a href="#B56-micromachines-16-00205" class="html-bibr">56</a>].</p>
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<p>The structure of BAW. (<b>a</b>–<b>d</b>) SMR, back silicon etching-type FBAR, lower concave cavity-type FBAR, and upper convex cavity-type FBAR, respectively.</p>
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<p>Fabrication of BAW-SMR. (<b>a</b>) Schematic representation of SMR structures without and with electrode frames. Adapted from [<a href="#B66-micromachines-16-00205" class="html-bibr">66</a>]. (<b>b</b>) Schematic diagram of SMR on acoustic reflector diagram. The bottom electrode cannot be directly accessed by the RF probe and is instead excited by the capacitive coupling effect. Adapted from [<a href="#B64-micromachines-16-00205" class="html-bibr">64</a>].</p>
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<p>The fabrication of BAW-FBAR. (<b>a</b>) Fabrication process of the FBAR device. Adapted from [<a href="#B75-micromachines-16-00205" class="html-bibr">75</a>]. (<b>b</b>) Fabrication of AlScN-based upper mounted cavity-type FBAR. Adapted from [<a href="#B82-micromachines-16-00205" class="html-bibr">82</a>] (<b>c</b>) Wafer bonding and layer transfer techniques. Adapted from [<a href="#B29-micromachines-16-00205" class="html-bibr">29</a>].</p>
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<p>The fabrication of BAW-FBAR. (<b>a</b>) Fabrication process of the FBAR device. Adapted from [<a href="#B75-micromachines-16-00205" class="html-bibr">75</a>]. (<b>b</b>) Fabrication of AlScN-based upper mounted cavity-type FBAR. Adapted from [<a href="#B82-micromachines-16-00205" class="html-bibr">82</a>] (<b>c</b>) Wafer bonding and layer transfer techniques. Adapted from [<a href="#B29-micromachines-16-00205" class="html-bibr">29</a>].</p>
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<p>BAW-XBAW resonator. (<b>a</b>) Simplified section view of the XBAR resonator. Adapted from [<a href="#B92-micromachines-16-00205" class="html-bibr">92</a>]. (<b>b</b>) Traditional frequency scaling, simple nth overtone scaling and P3F scaling [<a href="#B89-micromachines-16-00205" class="html-bibr">89</a>]. This image has been obtained with permission from IEEE Publishing.</p>
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<p>Construction and fabrication of HSBRs. Six-mask process flow for fabricating HSBRs. Adapted from [<a href="#B95-micromachines-16-00205" class="html-bibr">95</a>].</p>
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<p>Improvement of HSBR performance. (<b>a</b>) Schematic of the coupled BAW/SAW resonator proposed in [<a href="#B101-micromachines-16-00205" class="html-bibr">101</a>]. (<b>b</b>) The estimation results by FEM (marked stars show the experimental results and phase velocity of the excited mode for Si and GaN substrates) [<a href="#B101-micromachines-16-00205" class="html-bibr">101</a>]. (<b>c</b>) The phase velocity of the excited mode for Si and GaN substrates [<a href="#B101-micromachines-16-00205" class="html-bibr">101</a>]. Images (<b>a</b>–<b>c</b>) have been obtained with permission from IEEE Publishing.</p>
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<p>The measures to expand bandwidth. (<b>a</b>) Ladder filter. (<b>b</b>) lattice filter. (<b>c</b>) ladder-lattice filter [<a href="#B78-micromachines-16-00205" class="html-bibr">78</a>]. (<b>d</b>) Topological structure of the ladder-type FBAR filter circuit. Adapted from [<a href="#B109-micromachines-16-00205" class="html-bibr">109</a>]. (<b>e</b>) The filter topology structure combining BAW and IPD technologies. Adapted from [<a href="#B110-micromachines-16-00205" class="html-bibr">110</a>] (<b>f</b>) Topology of the hybrid B41 BAW filter. Adapted from [<a href="#B111-micromachines-16-00205" class="html-bibr">111</a>] with AlN resonators.</p>
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16 pages, 4962 KiB  
Article
Design and Numerical Simulation of a Standing Surface Acoustic Wave-Based Microdevice for Whole Blood Cell Separation
by Maryam Hajimoradi, Moein Talebian Gevari, Keith Robert Pullen and Mohammad Mojaddam
Computation 2025, 13(2), 42; https://doi.org/10.3390/computation13020042 - 6 Feb 2025
Viewed by 665
Abstract
Standing surface acoustic wave (SSAW)-based acoustofluidics is widely used due to its compatibility with soft materials and polymer structures. In the presence of an acoustic field, particles move either toward pressure nodes or anti-nodes according to their contrast factor. Using this technique, blood [...] Read more.
Standing surface acoustic wave (SSAW)-based acoustofluidics is widely used due to its compatibility with soft materials and polymer structures. In the presence of an acoustic field, particles move either toward pressure nodes or anti-nodes according to their contrast factor. Using this technique, blood cells with a certain characteristic can be oriented in different streamlines in a microchannel. The cumulative effect of parameters, such as the inlet velocity ratio of the buffer solution to the blood sample, acoustic frequency, voltage, and channel geometry, is key to effective separation in these microfluidic chips. In this study, simultaneous separation of white blood cells, red blood cells, and platelets in one stage is simulated by means of numerical calculations. The linear constitutive equation for the piezoelectric substrate, the Helmholtz equation for the acoustic field, and the Navier–Stokes equations for fluid mechanics are solved simultaneously to precisely capture the blood cell behavior in the SSAW-based device. The results show that whole blood cell separation can be achieved using a velocity ratio of 6.25, a resonance frequency of 8.28 MHz, and a voltage of 8.5 V in the proposed five-outlet microfluidic chip. Full article
(This article belongs to the Section Computational Engineering)
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<p>A schematic representation of an acoustofluidic microchip based on a piezoelectric substrate (1) utilizing IDTs (2) to separate blood cells suspended in the flow. The traveling acoustic waves generated by the IDTs form pressure nodes (PNs) and anti-nodes (PANs) across the microchannel (3) (shown by the red waves). The blood cells are attracted by either PNs or PANs and isolated through the outlets.</p>
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<p>(<b>a</b>) Two-dimensional schematic representation of the microfluidic device, including the IDTs on the sides of the microchannel to generate traveling surface acoustic waves. The microchannel has three inlets to inject the buffer solution and the blood samples and five outlets to isolate the separated blood cells by acoustic waves (all dimensions are in µm); (<b>b</b>) 3D schematic of the setup and the designated inlet/outlets.</p>
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<p>Results validated by a former study [<a href="#B50-computation-13-00042" class="html-bibr">50</a>]. (<b>a</b>) Pressure acoustic profile at a resonance frequency of 7.453 MHz, (<b>b</b>) pressure magnitude at a voltage of 3 V, (<b>c</b>) pressure magnitude at a voltage of 5 V, (<b>d</b>) WBC isolation through the middle outlet, and (<b>e</b>) PLT isolation via the side outlets.</p>
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<p>The dimensionless lateral displacement versus velocity ratio for particles with (<b>a</b>) 3 µm, (<b>b</b>) 8 µm, and (<b>c</b>) 15 µm diameters.</p>
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<p>Comparison of particle deflection at V = 3 V with different <math display="inline"><semantics> <mrow> <mi>α</mi> <mo> </mo> <mi mathvariant="normal">v</mi> <mi mathvariant="normal">a</mi> <mi mathvariant="normal">l</mi> <mi mathvariant="normal">u</mi> <mi mathvariant="normal">e</mi> <mi mathvariant="normal">s</mi> </mrow> </semantics></math>: (<b>a</b>) velocity field at <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>=</mo> <mn>0</mn> <mo>,</mo> </mrow> </semantics></math> (<b>b</b>) particle deflection at <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>=</mo> <mn>0</mn> <mo>,</mo> <mo> </mo> </mrow> </semantics></math> (<b>c</b>) velocity field at <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>=</mo> <mn>0.6</mn> <mo>,</mo> </mrow> </semantics></math> and (<b>d</b>) particle deflection at <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>=</mo> <mn>0.6</mn> </mrow> </semantics></math>.</p>
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<p>Lateral displacement of particles versus velocity of the system.</p>
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<p>Dimensionless lateral displacement of particles ranging from 2 to 20 µm versus voltage.</p>
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<p>Results of the new system’s design: (<b>a</b>) pressure acoustic field; (<b>b</b>) separation and capturing of particles in the specific reservoir.</p>
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<p>Results of the new system’s design: (<b>a</b>) pressure acoustic field; (<b>b</b>) separation and capturing of particles in the specific reservoir.</p>
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<p>The flowchart indicates the process and setting required to separate blood cells using the proposed SSAW-based microchip.</p>
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23 pages, 3047 KiB  
Review
Advancements in Surface Acoustic Wave Gyroscope Technology in 2015–2024
by Alexander Kukaev, Egor Shalymov, Sergey Shevchenko, Maria Sorvina and Vladimir Venediktov
Sensors 2025, 25(3), 877; https://doi.org/10.3390/s25030877 - 31 Jan 2025
Viewed by 366
Abstract
Although the theoretical basis for surface acoustic wave gyroscopes (SAWGs) was first proposed in 1980, their design concepts are still under development. Nevertheless, these sensors are of a great interest in the potential market owing to their exceptional shock resistance, small size, low [...] Read more.
Although the theoretical basis for surface acoustic wave gyroscopes (SAWGs) was first proposed in 1980, their design concepts are still under development. Nevertheless, these sensors are of a great interest in the potential market owing to their exceptional shock resistance, small size, low power consumption, and simple manufacturing process that ensures low cost. This paper aims to conscientiously investigate the ideas that have been proposed over the past decade in this area and evaluate the potential development required to bring SAWGs to market. It should be of interest for researchers in the field who might have missed some useful solutions that could be a missing piece in their own design, or for young researchers to inspire their creativity and open new research on the topic. Additionally, since some of the reviewed SAWG design concepts are based on a combination of several physical principles (for example, optical measurements), researchers from other fields may find useful solutions for incorporating surface acoustic wave techniques into their device concepts. Full article
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<p>Coriolis effect in running SAWs. (<b>a</b>) Particle velocities in unperturbed wave, (<b>b</b>) diagram of Coriolis forces when subjected to rotation, (<b>c</b>) directions of resulting particle velocities, (<b>d</b>) demonstration of the phase shift caused by Coriolis force.</p>
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<p>The Coriolis effect in standing SAWs.</p>
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<p>Impact of the electrode thickness on the gyroscopic effect in an IDT (<b>a</b>), and a split IDT structure (<b>b</b>) [<a href="#B11-sensors-25-00877" class="html-bibr">11</a>].</p>
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<p>Structure of the sensor considered in [<a href="#B13-sensors-25-00877" class="html-bibr">13</a>].</p>
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<p>The scheme of the orthogonal 45° rotated SAWG described in [<a href="#B18-sensors-25-00877" class="html-bibr">18</a>].</p>
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<p>Reflective structure providing the best Q-factor, according to [<a href="#B19-sensors-25-00877" class="html-bibr">19</a>].</p>
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<p>The “skewed” resonator structure from [<a href="#B20-sensors-25-00877" class="html-bibr">20</a>].</p>
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<p>The scheme of the SAWG with ovenization system by Mahmoud Ash. and et al. [<a href="#B21-sensors-25-00877" class="html-bibr">21</a>].</p>
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<p>(<b>a</b>) The scheme of a standing wave-based SAWG with focused IDTs and (<b>b</b>) microphotos of fabricated device (from [<a href="#B23-sensors-25-00877" class="html-bibr">23</a>]).</p>
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<p>Design of the gyro with bulk acoustic wave excitation proposed in [<a href="#B23-sensors-25-00877" class="html-bibr">23</a>].</p>
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<p>Design of the acousto-optical gyroscope from [<a href="#B30-sensors-25-00877" class="html-bibr">30</a>].</p>
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<p>Design of the acousto-optical gyroscope by Lu Tian et al. [<a href="#B32-sensors-25-00877" class="html-bibr">32</a>].</p>
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<p>Illustration of Raman–Nath diffraction on SAW (simulation from [<a href="#B32-sensors-25-00877" class="html-bibr">32</a>]).</p>
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<p>SAW Gyroscope with a phononic crystal: scheme of the device (<b>a</b>) and the phononic crystal structure (<b>b</b>) [<a href="#B36-sensors-25-00877" class="html-bibr">36</a>].</p>
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15 pages, 3594 KiB  
Article
Numerical Design and Optimization of High Performance Langasite and Hetero-Acoustic Layer-Based Surface Acoustic Wave Device
by Minglong Deng, Jinkai Chen, Jikai Zhang, Weilun Xie, Hao Jin, Weipeng Xuan, Shurong Dong and Jikui Luo
Micromachines 2025, 16(2), 166; https://doi.org/10.3390/mi16020166 - 30 Jan 2025
Viewed by 570
Abstract
La3Ga5SiO14 (langasite, LGS)-based surface acoustic wave (SAW) devices are widely used for industrial health monitoring in harsh high-temperature environments. However, a conventional LGS-based SAW structure has a low quality factor (Q) due to its spurious resonant peaks. A [...] Read more.
La3Ga5SiO14 (langasite, LGS)-based surface acoustic wave (SAW) devices are widely used for industrial health monitoring in harsh high-temperature environments. However, a conventional LGS-based SAW structure has a low quality factor (Q) due to its spurious resonant peaks. A hetero-acoustic layer (HAL)-based structure can effectively enhance the Q factor and the figure of merit (FOM) of SAWs due to its better energy confinement of SAWs. In this work, a HAL-based structure is proposed to achieve a high FOM and high-temperature resistance at the same time. Based on the finite element method (FEM) and coupling-of-model (COM) combined simulation, a systematic numerical investigation was conducted to find the optimal materials and structural parameters considering the viability of an actual fabricating process. After optimizing the layer number, an intermediate-layer material choice and structural parameters, Pt/(0°, 138.5°, 27°) LGS/YX-LGS/SiC HAL structure were chosen. The proposed structure achieves a Q factor and FOM improvement of more than 5 and 2.6 times higher than those of conventional SAW structures, which is important for the development of high temperature SAW sensors. These findings pave a viable method for improving the Q factor and FOM of LGS-based SAW and can provide material and device structural design guidance for fabrication and high-temperature applications in the future. Full article
(This article belongs to the Special Issue Surface and Bulk Acoustic Wave Devices)
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<p>Schematic diagram of the COM model configuration for one-port resonator.</p>
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<p>(<b>a</b>) The process of the COM model parameter extraction based on the (<b>b</b>) unit cell model of the resonator.</p>
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<p>(<b>a</b>) FEM simulation model diagrams of (<b>i</b>) conventional structure, (<b>ii</b>) two-layer structure, (<b>iii</b>) three-layer structure, and (<b>iv</b>) four-layer structure. Displacement component and vibration mode diagrams for a conventional structure at (<b>b</b>) 435.13 MHz and (<b>c</b>) 437.69 MHz resonance frequency, for a two-layer HAL structure at (<b>d</b>) 458.96 MHz and (<b>e</b>) 517.67 MHz resonance frequency, for a three-layer HAL structure at (<b>f</b>) 426.39 MHz and (<b>g</b>) 422.04 MHz resonance frequency, and for a four-layer HAL structure at (<b>h</b>) 425.55 MHz and (<b>i</b>) 421.43 MHz resonance frequency.</p>
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<p>(<b>a</b>) Three-layer FEM simulation model diagram. (<b>b</b>) The admittance spectrum with 0.5<span class="html-italic">λ</span> LGS thickness and varying SiO<sub>2</sub> thicknesses. The variation trend of (<b>c</b>) frequency, (<b>d</b>) <span class="html-italic">K</span><sup>2</sup>, and (<b>e</b>) Q factor in the structure of Pt/LGS/SiO<sub>2</sub>/SiC with different LGS and SiO<sub>2</sub> thicknesses.</p>
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<p>(<b>a</b>) Three-layer FEM simulation model diagram. (<b>b</b>) The admittance spectrum with <span class="html-italic">λ</span> YX-LGS thickness and varying (0°,138.5°,27°) LGS thicknesses. The variation trend of (<b>c</b>) frequency, (<b>d</b>) <span class="html-italic">K</span><sup>2</sup>, and (<b>e</b>) Q factor in the structure of Pt/(0°,138.5°,27°)LGS/YX-LGS/SiC.</p>
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<p>(<b>a</b>) FEM Simulation model diagram of the four-layer HAL structure. Comparison of (<b>b</b>) frequency, (<b>c</b>) <span class="html-italic">K</span><sup>2</sup>, (<b>d</b>) Q factor, and (<b>e</b>) FOM between three-layer and four-layer HAL structures with varied thickness of YX-LGS.</p>
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<p>(<b>a</b>) FEM simulation model diagram of the three-layer HAL structure with varying electrode thickness. Comparison of (<b>b</b>) frequency, (<b>c</b>) <span class="html-italic">K</span><sup>2</sup>, (<b>d</b>) Q factor and (<b>e</b>) FOM from the conventional and HAL structure SAW devices with varied Pt electrode thicknesses.</p>
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<p>The comparison of (<b>a</b>) admittance spectrum and (<b>b</b>) performance parameters between optimized HAL and conventional structure SAW devices.</p>
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11 pages, 1923 KiB  
Article
Experimental Study on Noise-Reduced Propagation Characteristics of the Parametric Acoustic Array Field in a Neck Phantom
by Li Wang, Fengji Li, Jie Zhou and Haijun Niu
Sensors 2025, 25(3), 802; https://doi.org/10.3390/s25030802 - 29 Jan 2025
Viewed by 574
Abstract
The electrolarynx (EL) is a common device for voice reconstruction in laryngectomy patients, but its mechanical sound source generates significant radiation noise, affecting the naturalness and acceptability of the speech. The parametric acoustic array (PAA), which produces directionally propagated difference-frequency sound waves, presents [...] Read more.
The electrolarynx (EL) is a common device for voice reconstruction in laryngectomy patients, but its mechanical sound source generates significant radiation noise, affecting the naturalness and acceptability of the speech. The parametric acoustic array (PAA), which produces directionally propagated difference-frequency sound waves, presents a promising alternative for creating a more natural glottal-like voice source in the trachea while reducing radiation noise. In this study, we developed a tissue-mimicking phantom to simulate human neck tissue and used a single-transducer-based PAA platform to generate modulated ultrasound signals with glottal waveform characteristics. Ultrasonic microphones captured sound signals fromthe trachea and surrounding air, and signal processing was used to isolate the difference-frequency signals. The results demonstrated that difference-frequency signals were successfully detected in the phantom’s trachea, with time-domain waveforms and frequency spectra closely resembling the designed glottal waveform (Pearson correlation coefficient = 0.9438). Additionally, radiation noise produced by the PAA was significantly lower (23 dB, p < 0.0001) compared to the traditional EL. These findings demonstrate the potential of PAA for voice source reconstruction in laryngectomy patients and suggest its capacity to enhance speech rehabilitation outcomes. Further research is required to refine the frequency range and evaluate clinical applicability. Full article
(This article belongs to the Section Biomedical Sensors)
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<p>Experimental setup for investigating the propagation characteristics of the PAA difference-frequency sound field in a neck phantom. (<b>a</b>) Schematic diagram of the experimental platform; (<b>b</b>) photograph of the physical setup of the system: the ultrasound transducer is placed on the surface of the phantom, with coupling gel applied in the center. A microphone (Microphone 1) is inserted into a hole on the opposite side of the phantom, with its tip positioned at the center of the phantom’s trachea to capture the sound field inside the trachea. Another microphone (Microphone 2) is placed 10 cm from the trachea center on the outside of the phantom, at the same horizontal plane as Microphone 1 and at an approximate 45° angle to Microphone 1, to collect radiated noise.</p>
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<p>(<b>a</b>) Predefined glottal waveform and (<b>b</b>) corresponding AM-modulated excitation signal.</p>
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<p>(<b>a</b>) Time−domain waveforms of LFS, AS, and TMS. (<b>b</b>) Normalized comparison of one period from the LFS, AS, TMS, and EL signals, derived from one cycle in <a href="#sensors-25-00802-f003" class="html-fig">Figure 3</a>a (between the two dotted lines), highlighting waveform distortions and differences in peak and rise times. In contrast, the excitation signal produced by the EL is completely different from the glottal wave signal. The Pearson correlation between the EL signal and the LFS is only 0.0057, indicating minimal similarity.</p>
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<p>Burg AR power spectral density (PSD) curves of (<b>a</b>) LFS, (<b>b</b>) AS, and (<b>c</b>) TMS signals.</p>
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<p>Comparison of radiation noise levels: (<b>a</b>) SPL of radiation noise for EL and PAA excitation sources, and (<b>b</b>) SPL difference (Δ<span class="html-italic">L</span>) between external and internal microphones for EL and PAA (***: <span class="html-italic">p</span> &lt; 0.001).</p>
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12 pages, 3482 KiB  
Article
Driving Rotational Circulation in a Microfluidic Chamber Using Dual Focused Surface-Acoustic-Wave Beams
by Jin-Chen Hsu and Kai-Li Liao
Micromachines 2025, 16(2), 140; https://doi.org/10.3390/mi16020140 - 25 Jan 2025
Viewed by 701
Abstract
In this paper, enhanced rotational circulation in a circular microfluidic chamber driven by dual focused surface-acoustic-wave (SAW) beams is presented. To characterize the resonant frequency and focusing effect, we simulate the focused SAW field excited by an arc-shaped interdigital transducer patterned on a [...] Read more.
In this paper, enhanced rotational circulation in a circular microfluidic chamber driven by dual focused surface-acoustic-wave (SAW) beams is presented. To characterize the resonant frequency and focusing effect, we simulate the focused SAW field excited by an arc-shaped interdigital transducer patterned on a 128°Y-cut lithium-niobate (LiNbO3) substrate using a finite element method. A full three-dimensional perturbation model of the combined system of the microfluidic chamber and the SAW device is conducted to obtain the acoustic pressure and acoustic streaming fields, which show rotational acoustic pressure and encircling streaming resulted in the chamber. Accordingly, the SAW acoustofluidic system is realized using microfabrication techniques and applied to perform acoustophoresis experiments on submicron particles suspending in the microfluidic chamber. The result verifies the rotational circulation motion of the streaming flow, which is attributed to enhanced angular momentum flux injection and Eckart streaming effect through the dual focused SAW beams. Our results should be of importance in driving particle circulation and enhancing mass transfer in chamber embedded microfluidic channels, which may have promising applications in accelerating bioparticle or cell reactions and fusion, enhancing biochemical and electrochemical sensing, and efficient microfluidic mixing. Full article
(This article belongs to the Special Issue Surface and Bulk Acoustic Wave Devices)
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<p>(<b>a</b>) Schematics of the device structure. A microfluidic chamber is actuated by two misaligned focused SAWs excited using the offset IDTs on a LiNbO<sub>3</sub> substrate. (<b>b</b>) Geometrical parameters of the device, where <span class="html-italic">D</span> is the chamber diameter, <span class="html-italic">R</span> is the radius of the first electrode of the focused IDTs, <span class="html-italic">θ<sub>c</sub></span> is the coverage angle of the focused IDTs, and <span class="html-italic">e</span> is the offset distance of the IDTs from the horizontal centerline of the circular chamber.</p>
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<p>(<b>a</b>) Calculated S11 spectrum of 20-pair IDT of <span class="html-italic">p</span><sub>IDT</sub> = 200 μm on the 128°<span class="html-italic">Y</span>-cut LiNbO<sub>3</sub> along the <span class="html-italic">X</span> direction using the 2D FE model, which shows a resonant frequency at 20.4 MHz. (<b>b</b>) Calculated S11 value when IDT of the same pitch is arranged long other directions at an angle <span class="html-italic">θ</span> to the <span class="html-italic">X</span> direction and excited at the frequency of 20.4 MHz, showing that the excitation efficiency of the IDT decreases as <span class="html-italic">θ</span> is increased. A threshold (the dashed line) is set at <span class="html-italic">θ</span> = 30° for the focused IDT design.</p>
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<p>(<b>a</b>) Calculated focused SAW field at the frequency <span class="html-italic">f</span><sub>SAW</sub> = 20.4 MHz using a full 3D model, which shows a highly focused SAW beam achieved by the arc-shaped IDT. (<b>b</b>) Horizontal and (<b>c</b>) vertical distributions of the displacement amplitude on the top surface of the LiNbO<sub>3</sub> substrate along the dashed lines in (<b>a</b>).</p>
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<p>Measured S11 spectrum of the fabricated focused SAW device with <span class="html-italic">p</span><sub>IDT</sub> = 200 μm, <span class="html-italic">N<sub>e</sub> </span>= 20, and <span class="html-italic">θ<sub>c</sub></span> = 60°. The measured resonant frequency occurs at 19.1 MHz.</p>
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<p>(<b>a</b>) Coupled acoustic-wave field of the SAW device and the microfluidic chamber, where the chamber diameter <span class="html-italic">D </span>= 1000 μm. (<b>b</b>) Top views of the acoustic pressure field and the associated first-order velocity field in the circular chamber. (<b>c</b>) Top view and cross-section view of the second-order streaming field in the chamber.</p>
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<p>(<b>a</b>) Coupled acoustic-wave field of the SAW device and the microfluidic chamber, where the chamber diameter <span class="html-italic">D </span>= 2000 μm. (<b>b</b>) Top view and cross-section view of the second-order streaming field in the chamber.</p>
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<p>Time-evolution images of particle motion in the microfluidic chamber driven by the dual focused SAW beams, showing strong rotational circulation of the particle streams. The dashed arrows indicate the direction of circulation.</p>
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17 pages, 3945 KiB  
Article
Numerical Simulation Analysis of Laser Ultrasonic Detection of Defects in Silicon Carbide
by Yuan Yin, Jinbao Xia, Hongkun Nie, Bo Yao, Daofa Sun, Longnan Ma, Ruihang Li, Zihao Li and Baitao Zhang
Crystals 2025, 15(2), 125; https://doi.org/10.3390/cryst15020125 - 24 Jan 2025
Viewed by 573
Abstract
Silicon carbide (SiC) is widely used in power electronic devices and other fields, the defects of which can significantly impact its performance in device fabrication. Laser ultrasonic non-destructive testing (NDT) as a novel and effective approach can detect these defects in real time. [...] Read more.
Silicon carbide (SiC) is widely used in power electronic devices and other fields, the defects of which can significantly impact its performance in device fabrication. Laser ultrasonic non-destructive testing (NDT) as a novel and effective approach can detect these defects in real time. This study introduces a numerical model for the SiC NDT that elucidates the dynamic interactions between laser-induced ultrasonic waves and surface defects, and internal defects in SiC, respectively. Results show NDT is an effective way to locate the SiC defect and the ultrasonic waves’ vibration amplitude of detection points at defect edges increases by at least 16% compared to adjacent points, with a maximum of 43%. A comparative assessment between surface and internal defect vibration responses for acoustic is also made. For internal defects, the oscillation time of the acoustic wave at the detection point on the surface away from the edge of the defect at the excitation point exceeds that of surface defects by 100 ns, and the amplitude near the excitation point is more pronounced, reaching 1.44 nm, which is 4.2 times that of corresponding surface defects. Additionally, a linear relationship is observed between the arrival time of transmitted Rayleigh Waves (RSR) and internal defect length, with a correlation coefficient of 0.9878. Similarly, a linear relationship is established between the amplitude of reflected Rayleigh Waves (rR) and defect width, with a correlation coefficient of 0.9976, providing an effective way to quantify the inner defect. Furthermore, transient temperature profiles at distinct positions and transient acoustic fields and the relationship of acoustic vibration amplitude increasing with laser spot size under a fixed laser power density are also analyzed. This model provides a theoretical foundation for laser ultrasonic NDT setup and choice of micro-vibration detection device. Full article
(This article belongs to the Special Issue Design and Synthesis of Functional Crystal Materials)
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<p>Schematic diagram with a surface defect (<b>a</b>) or an internal defect (<b>b</b>).</p>
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<p>Temperature change curve at the excitation point (−2,0).</p>
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<p>Temporal temperature evolution at various depths following pulsed laser irradiation on SiC.</p>
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<p>Acoustic field distribution of specimens with a surface defect at (<b>a</b>) t = 350 ns and (<b>b</b>) t = 700 ns.</p>
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<p>Shows the distribution of the sound field at (<b>a</b>) t = 550 ns and (<b>b</b>) t = 700 ns of a specimen with an internal defect.</p>
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<p>Time domain diagram of the reflected wave signal measured at (1,0) (<b>a</b>) and the transmitted wave signal measured at (4,0) (<b>b</b>).</p>
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<p>Surface inspection points of SiC specimens with a surface defect (<b>a</b>) or with an internal defect (<b>b</b>).</p>
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<p>Detection points at the edge of the defect on the same side of the excitation point (<b>a</b>) and on the opposite side of the excitation point (<b>b</b>).</p>
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<p>Schematic diagram of the estimated length and width of the internal defect.</p>
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<p>Transmitted wave vibration image with different internal defect lengths.</p>
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<p>Defect length and RSR wave arrival time relationship.</p>
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<p>Reflected wave vibration images with different defect widths.</p>
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<p>Relationship between defect width and rR wave amplitude.</p>
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<p>Acoustic wave vibration images with different spot radii.</p>
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14 pages, 9165 KiB  
Article
Curvature Determination Method for Diverging Acoustic Lens of Underwater Acoustic Transducer
by Minze Li, Mingzhen Xin, Fanlin Yang, Yu Luo, Jinpeng Liu and Niuniu Wu
Sensors 2025, 25(2), 568; https://doi.org/10.3390/s25020568 - 19 Jan 2025
Viewed by 702
Abstract
Underwater acoustic transducers need to expand the coverage of acoustic signals as much as possible in most ocean explorations, and the directivity indicators of transducers are difficult to change after the device is packaged, which makes the emergence angle of the underwater acoustic [...] Read more.
Underwater acoustic transducers need to expand the coverage of acoustic signals as much as possible in most ocean explorations, and the directivity indicators of transducers are difficult to change after the device is packaged, which makes the emergence angle of the underwater acoustic transducer limited in special operating environments, such as polar regions, submarine volcanoes, and cold springs. Taking advantage of the refractive characteristics of sound waves propagating in different media, the directivity indicators can be controlled by installing an acoustic lens outside the underwater acoustic transducer. To increase the detection range of an underwater acoustic transducer in a specific marine environment, a curvature-determining method for the diverging acoustic lens of an underwater acoustic transducer is proposed based on the acoustic ray tracing theory. The relationship equation between the original directivity indicators of the underwater acoustic transducer and the emergence angle in the specific environment is constructed, and the slope of the acoustic lens at different positions of the underwater acoustic transducer is obtained by a progressive solution. Then, the least squares polynomial fitting of the acoustic lens slope at all the refractive positions is carried out to obtain the optimal curvature of the acoustic lens. Experiments are designed to verify the effectiveness of the curvature determination method for the diverging acoustic lens of an underwater acoustic transducer, and the directivity indicators of acoustic lenses under different materials and different marine environments are analyzed. The experimental results show that the acoustic lens can change the directivity of the underwater acoustic transducer without changing the acoustic unit array, and the curvature of the acoustic lens directly affects the directivity indicators after refraction, so the method proposed in this paper has important reference value for determining the optimal shape of the diverging acoustic lens. Full article
(This article belongs to the Section Navigation and Positioning)
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<p>Schematic diagram of the diverging acoustic lens of an underwater acoustic transducer. (<b>a</b>) Underwater acoustic transducers and acoustic lenses; (<b>b</b>) propagation of sound waves in acoustic lenses; (<b>c</b>) Snell’s law of sound propagation.</p>
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<p>Curvature determination algorithm flow chart.</p>
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<p>The shape of the acoustic lens with the different materials. (<b>a</b>) PDMS; (<b>b</b>) LK; (<b>c</b>) SI; (<b>d</b>) RTV; (<b>e</b>) LDPE; (<b>f</b>) PS.</p>
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<p>The shape of the acoustic lens with the different emergence angles. (<b>a</b>) Emergence angle = 10°; (<b>b</b>) emergence angle = 20°; (<b>c</b>) emergence angle = 35°; (<b>d</b>) emergence angle = 55°; (<b>e</b>) emergence angle = 70°; (<b>f</b>) emergence angle = 85°.</p>
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<p>The variation in the maximum emergence angle of the acoustic lens with different materials. (<b>a</b>) PDMS; (<b>b</b>) LK; (<b>c</b>) SI; (<b>d</b>) RTV; (<b>e</b>) LDPE; (<b>f</b>) PS.</p>
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<p>The variation in the maximum emergence angle of the acoustic lens with different materials. (<b>a</b>) PDMS; (<b>b</b>) LK; (<b>c</b>) SI; (<b>d</b>) RTV; (<b>e</b>) LDPE; (<b>f</b>) PS.</p>
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<p>The variation in the maximum emergence angle of the acoustic lens with different marine environments. (<b>a</b>) T = −2 °C, C = 1440 m/s; (<b>b</b>) T = 5 °C, C = 1485 m/s; (<b>c</b>) T = 10 °C, C = 1497 m/s; (<b>d</b>) T = 16 °C, C = 1512 m/s; (<b>e</b>) T = 23 °C, C = 1527 m/s; (<b>f</b>) T = 30 °C, C = 1546 m/s.</p>
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28 pages, 14974 KiB  
Article
Multidimensional Particle Separation by Tilted-Angle Standing Surface Acoustic Waves—Physics, Control, and Design
by Sebastian Sachs, Jörg König and Christian Cierpka
Powders 2025, 4(1), 2; https://doi.org/10.3390/powders4010002 - 8 Jan 2025
Viewed by 648
Abstract
Lab-on-a-Chip devices based on tilted-angle standing surface acoustic waves (tasSAWs) emerged as a promising technology for multidimensional particle separation, highly selective in particle size and acoustic contrast factor. For this active separation method, a tailored acoustic field is used to focus and separate [...] Read more.
Lab-on-a-Chip devices based on tilted-angle standing surface acoustic waves (tasSAWs) emerged as a promising technology for multidimensional particle separation, highly selective in particle size and acoustic contrast factor. For this active separation method, a tailored acoustic field is used to focus and separate particles on stationary pressure nodes by means of the acoustic radiation force. However, additional non-linear acoustofluidic phenomena, such as the acoustically induced fluid flow or dielectrophoretic effects, are superimposed on the separation process. To obtain a particle separation of high quality, control parameters that can be adjusted during the separation process as well as design parameters are available. The latter are specified prior to the separation and span a high-dimensional parameter space, ranging from the acoustic wavelength to the dimensions and materials used for the microchannel. In this paper, the physical mechanisms to control and design tasSAW-based separation devices are reviewed. By combining experimental, semi-analytical, and numerical findings, a critical channel height and width are derived to suppress the influence of the acoustically induced fluid flow. Dealing with the three-dimensional nature of the separation process, particles are focused at different height levels of equal force balance by implementing a channel cover of high acoustic impedance while achieving an approx. three-times higher acoustic pressure. Using this improved channel design, the particle shape is identified as an additional separation criterion, rendering the continuous acoustofluidic particle separation as a multidimensional technology capable of selectively separating microparticles below 10 μm with regard to size, acoustic contrast, and shape. Full article
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<p>Schematic representation of the work flow applied in this project, where the multiphysical phenomena were studied by experiments and numerical simulations in conjunction with crucial design and control parameters. Based on the correlations found between the particle behavior and the parameters set, the design of the acoustofluidic device was revised systematically.</p>
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<p>Schematic of the acoustofluidic device using tasSAW to separate three particle species from a mixture (<b>a</b>), which is inserted with the volume flow rate <math display="inline"><semantics> <msub> <mi>Q</mi> <mn>2</mn> </msub> </semantics></math>. For visualization purposes, the PDMS cover to seal the microchannel was omitted. Top view of the particle separation with pressure nodes indicated by dashed lines and the rotated coordinate system (<math display="inline"><semantics> <mrow> <msup> <mi>x</mi> <mo>′</mo> </msup> <mo>,</mo> <msup> <mi>y</mi> <mo>′</mo> </msup> <mo>,</mo> <mi>z</mi> </mrow> </semantics></math>) (<b>b</b>).</p>
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<p>Measured positions (exp) and numerically calculated trajectories (sim) of polystyrene particles with two different sizes at the beginning (<b>a</b>) and end (<b>b</b>) of the IDTs. The edges of the opposite IDTs are indicated by red dashed lines.</p>
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<p>Numerically calculated trajectories of particles with (<b>a</b>) different radii (<math display="inline"><semantics> <mrow> <msub> <mi>Q</mi> <mi>total</mi> </msub> <mo>=</mo> <mn>1.67</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">L</mi> <mo> </mo> <mi>min</mi> </mrow> </mrow> </semantics></math><sup>−1</sup>, <math display="inline"><semantics> <mrow> <msub> <mi>P</mi> <mi>el</mi> </msub> <mo>=</mo> <mn>612.25</mn> <mo> </mo> <mrow> <mi mathvariant="normal">m</mi> <mi mathvariant="normal">W</mi> </mrow> </mrow> </semantics></math>, polystyrene) and (<b>b</b>) materials (<math display="inline"><semantics> <mrow> <msub> <mi>Q</mi> <mi>total</mi> </msub> <mo>=</mo> <mn>5.04</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">L</mi> <mo> </mo> <mi>min</mi> </mrow> </mrow> </semantics></math><sup>−1</sup>, <math display="inline"><semantics> <mrow> <msub> <mi>P</mi> <mi>el</mi> </msub> <mo>=</mo> <mn>205.10</mn> <mo> </mo> <mrow> <mi mathvariant="normal">m</mi> <mi mathvariant="normal">W</mi> </mrow> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <mi>r</mi> <mo>=</mo> <mn>1.25</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">m</mi> </mrow> </mrow> </semantics></math>, silicon dioxide (<math display="inline"><semantics> <msub> <mi>SiO</mi> <mn>2</mn> </msub> </semantics></math>), polymethylmethacrylate (PMMA), polystyrene (PS)). The motion of the particles is affected by a tasSAW with a tilt angle of <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>=</mo> <mn>11</mn> <mo>°</mo> </mrow> </semantics></math> within the dashed lines. Main flow is applied in the positive <span class="html-italic">y</span>-direction.</p>
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<p>Multidimensional separation of feed particles with bimodal Gaussian-distributed radii and acoustic contrast factors as illustrated by the normalized probability density <math display="inline"><semantics> <msup> <mover accent="true"> <mi>f</mi> <mo>˜</mo> </mover> <mi>f</mi> </msup> </semantics></math> (<b>a</b>). The separation result with <math display="inline"><semantics> <mrow> <msub> <mi>Q</mi> <mi>total</mi> </msub> <mo>=</mo> <mn>4.18</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">L</mi> <mo> </mo> <mi>min</mi> </mrow> </mrow> </semantics></math><sup>−1</sup>, <math display="inline"><semantics> <mrow> <msub> <mi>P</mi> <mi>el</mi> </msub> <mo>=</mo> <mn>88.78</mn> <mo> </mo> <mrow> <mi mathvariant="normal">m</mi> <mi mathvariant="normal">W</mi> </mrow> </mrow> </semantics></math>, and <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>=</mo> <mn>11.3</mn> <mo>°</mo> </mrow> </semantics></math> is evaluated by a bivariate Tromp (<b>b</b>) and Shannon entropy function (<b>c</b>).</p>
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<p>Evaluation of the separation of particles with radii of <math display="inline"><semantics> <mrow> <mn>0.25</mn> <mo> </mo> </mrow> </semantics></math><math display="inline"><semantics> <mo>μ</mo> </semantics></math><math display="inline"><semantics> <mi mathvariant="normal">m</mi> </semantics></math>, <math display="inline"><semantics> <mrow> <mn>0.5</mn> <mo> </mo> </mrow> </semantics></math><math display="inline"><semantics> <mo>μ</mo> </semantics></math><math display="inline"><semantics> <mi mathvariant="normal">m</mi> </semantics></math>, and <math display="inline"><semantics> <mrow> <mn>2.5</mn> <mo> </mo> </mrow> </semantics></math><math display="inline"><semantics> <mo>μ</mo> </semantics></math><math display="inline"><semantics> <mi mathvariant="normal">m</mi> </semantics></math> across the control parameters based on the normalized maximum separation distance <math display="inline"><semantics> <mrow> <mo>Δ</mo> <msub> <mover accent="true"> <mi>x</mi> <mo>˜</mo> </mover> <mi>sep</mi> </msub> </mrow> </semantics></math> (<b>a</b>) and the respective tilt angle <math display="inline"><semantics> <mi>α</mi> </semantics></math> (<b>b</b>). In regions I and III, a separation distance of <math display="inline"><semantics> <mrow> <mo>Δ</mo> <msub> <mover accent="true"> <mi>x</mi> <mo>˜</mo> </mover> <mi>sep</mi> </msub> <mo>&lt;</mo> <mn>0.5</mn> </mrow> </semantics></math> is indicated, while results with <math display="inline"><semantics> <mrow> <mo>Δ</mo> <msub> <mover accent="true"> <mi>x</mi> <mo>˜</mo> </mover> <mi>sep</mi> </msub> <mo>≥</mo> <mn>0.5</mn> </mrow> </semantics></math> are evident in region II. The red dashed lines indicate the maximum <math display="inline"><semantics> <mrow> <mo>Δ</mo> <msub> <mover accent="true"> <mi>x</mi> <mo>˜</mo> </mover> <mi>sep</mi> </msub> </mrow> </semantics></math> at the tilted angle <math display="inline"><semantics> <msub> <mi>α</mi> <mi>max</mi> </msub> </semantics></math>.</p>
Full article ">Figure 7
<p>Three-dimensional representation of the normalized separation distance <math display="inline"><semantics> <mrow> <mo>Δ</mo> <msub> <mover accent="true"> <mi>x</mi> <mo>˜</mo> </mover> <mi>sep</mi> </msub> </mrow> </semantics></math> achieved by varying the input power <math display="inline"><semantics> <msub> <mi>P</mi> <mi>el</mi> </msub> </semantics></math>, the volume flow rate <math display="inline"><semantics> <msub> <mi>Q</mi> <mi>total</mi> </msub> </semantics></math>, and the aperture <math display="inline"><semantics> <mrow> <mi>A</mi> <mi>P</mi> </mrow> </semantics></math>. In the separation, particles with radii of <math display="inline"><semantics> <mrow> <mn>0.25</mn> <mo> </mo> </mrow> </semantics></math><math display="inline"><semantics> <mo>μ</mo> </semantics></math><math display="inline"><semantics> <mi mathvariant="normal">m</mi> </semantics></math>, <math display="inline"><semantics> <mrow> <mn>0.5</mn> <mo> </mo> </mrow> </semantics></math><math display="inline"><semantics> <mo>μ</mo> </semantics></math><math display="inline"><semantics> <mi mathvariant="normal">m</mi> </semantics></math>, and <math display="inline"><semantics> <mrow> <mn>2.5</mn> <mo> </mo> </mrow> </semantics></math><math display="inline"><semantics> <mo>μ</mo> </semantics></math><math display="inline"><semantics> <mi mathvariant="normal">m</mi> </semantics></math> were used.</p>
Full article ">Figure 8
<p>Experimentally (left half of the subfigures, <math display="inline"><semantics> <mrow> <msub> <mi>u</mi> <mi>tr</mi> </msub> <mo>=</mo> <msqrt> <mrow> <msubsup> <mi>u</mi> <mi>x</mi> <mn>2</mn> </msubsup> <mo>+</mo> <msubsup> <mi>u</mi> <mi>z</mi> <mn>2</mn> </msubsup> </mrow> </msqrt> </mrow> </semantics></math>) and numerically (right half of the subfigures, <math display="inline"><semantics> <mrow> <msub> <mi>u</mi> <mi>tr</mi> </msub> <mo>=</mo> <msqrt> <mrow> <msubsup> <mi>u</mi> <mrow> <mn>2</mn> <mo>,</mo> <mi>x</mi> </mrow> <mn>2</mn> </msubsup> <mo>+</mo> <msubsup> <mi>u</mi> <mrow> <mn>2</mn> <mo>,</mo> <mi>z</mi> </mrow> <mn>2</mn> </msubsup> </mrow> </msqrt> </mrow> </semantics></math> using the second-order fluid velocity <math display="inline"><semantics> <msub> <mi mathvariant="bold-italic">u</mi> <mn>2</mn> </msub> </semantics></math>) derived time-averaged absolute velocity fields for varying wavelengths of the SAW <math display="inline"><semantics> <msub> <mi>λ</mi> <mi>SAW</mi> </msub> </semantics></math> (horizontal) and channel heights <span class="html-italic">H</span> (vertical). The acoustically induced fluid flow is indicated by white streamlines and the magnitude of <math display="inline"><semantics> <msub> <mi>u</mi> <mi>tr</mi> </msub> </semantics></math> by colors. This figure is adapted from Sachs et al. (2022) [<a href="#B51-powders-04-00002" class="html-bibr">51</a>].</p>
Full article ">Figure 9
<p>Mean force coefficient <math display="inline"><semantics> <mi>ψ</mi> </semantics></math> against the particle radius <span class="html-italic">r</span> for different configurations of (<math display="inline"><semantics> <msub> <mi>λ</mi> <mi>SAW</mi> </msub> </semantics></math>, <span class="html-italic">H</span>) (<b>a</b>). The course of <math display="inline"><semantics> <mi>ψ</mi> </semantics></math> up to a particle radius of <math display="inline"><semantics> <mrow> <mi>r</mi> <mo>=</mo> <mn>1</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">m</mi> </mrow> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <mi>ψ</mi> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math> is shown in the inset. The numerical data were linked by quadratic regression. This subfigure was adapted from Sachs et al. (2022) [<a href="#B51-powders-04-00002" class="html-bibr">51</a>]. Average force difference <math display="inline"><semantics> <mrow> <mo>Δ</mo> <mi>F</mi> </mrow> </semantics></math> as a function of the channel height <span class="html-italic">H</span> for wavelengths of 90<math display="inline"><semantics> <mo> </mo> <mo>μ</mo> </semantics></math><math display="inline"><semantics> <mi mathvariant="normal">m</mi> </semantics></math> and 150<math display="inline"><semantics> <mo> </mo> <mo>μ</mo> </semantics></math><math display="inline"><semantics> <mi mathvariant="normal">m</mi> </semantics></math> with the corresponding critical channel heights <math display="inline"><semantics> <msub> <mi>H</mi> <mrow> <mi>crit</mi> <mo>,</mo> <mn>90</mn> </mrow> </msub> </semantics></math> and <math display="inline"><semantics> <msub> <mi>H</mi> <mrow> <mi>crit</mi> <mo>,</mo> <mn>150</mn> </mrow> </msub> </semantics></math> highlighted by dashed lines (<b>b</b>). The volume flow rate and electrical power were set constant at <math display="inline"><semantics> <mrow> <msub> <mi>Q</mi> <mi>total</mi> </msub> <mo>=</mo> <mn>0.03</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">L</mi> <mo> </mo> <mi>min</mi> </mrow> </mrow> </semantics></math><sup>−1</sup> and <math display="inline"><semantics> <mrow> <msub> <mi>P</mi> <mi>el</mi> </msub> <mo>=</mo> <mn>20</mn> <mo> </mo> <mrow> <mi mathvariant="normal">m</mi> <mi mathvariant="normal">W</mi> </mrow> </mrow> </semantics></math>, respectively.</p>
Full article ">Figure 10
<p>Experimental results on the velocity field near the beginning (<b>a</b>) and end (<b>c</b>) of the IDTs, which are marked by red dashed lines (<math display="inline"><semantics> <mrow> <msub> <mi>λ</mi> <mi>SAW</mi> </msub> <mo>=</mo> <mn>20</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">m</mi> </mrow> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <mi>H</mi> <mo>=</mo> <mn>185</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">m</mi> </mrow> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mi>P</mi> <mi>el</mi> </msub> <mo>=</mo> <mn>154</mn> <mo> </mo> <mrow> <mi mathvariant="normal">m</mi> <mi mathvariant="normal">W</mi> </mrow> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mi>Q</mi> <mi>total</mi> </msub> <mo>=</mo> <mn>1.6</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">L</mi> <mo> </mo> <mi>min</mi> </mrow> </mrow> </semantics></math><sup>−1</sup>). These subplots were adapted from [<a href="#B54-powders-04-00002" class="html-bibr">54</a>]. In (<b>b</b>,<b>d</b>), the acoustically induced vortices are calculated numerically in the same regions (<math display="inline"><semantics> <mrow> <msub> <mi>λ</mi> <mi>SAW</mi> </msub> <mo>=</mo> <mn>90</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">m</mi> </mrow> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <mi>H</mi> <mo>=</mo> <mn>185</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">m</mi> </mrow> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mi>P</mi> <mi>el</mi> </msub> <mo>=</mo> <mn>29.8</mn> <mo> </mo> <mrow> <mi mathvariant="normal">m</mi> <mi mathvariant="normal">W</mi> </mrow> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mi>Q</mi> <mi>total</mi> </msub> <mo>=</mo> <mn>0.33</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">L</mi> <mo> </mo> <mi>min</mi> </mrow> </mrow> </semantics></math><sup>−1</sup>). The streamlines are colored in correspondence to the velocity component <span class="html-italic">v</span> in main flow direction.</p>
Full article ">Figure 11
<p>Measured positions of particles with radii of <math display="inline"><semantics> <mrow> <mn>4.94</mn> <mo> </mo> </mrow> </semantics></math><math display="inline"><semantics> <mo>μ</mo> </semantics></math><math display="inline"><semantics> <mi mathvariant="normal">m</mi> </semantics></math>, <math display="inline"><semantics> <mrow> <mn>2.52</mn> <mo> </mo> </mrow> </semantics></math><math display="inline"><semantics> <mo>μ</mo> </semantics></math><math display="inline"><semantics> <mi mathvariant="normal">m</mi> </semantics></math>, and <math display="inline"><semantics> <mrow> <mn>0.57</mn> <mo> </mo> </mrow> </semantics></math><math display="inline"><semantics> <mo>μ</mo> </semantics></math><math display="inline"><semantics> <mi mathvariant="normal">m</mi> </semantics></math> from a top view (<b>a</b>) and in the channel cross-section (<b>b</b>) of the tasSAW device (<math display="inline"><semantics> <mrow> <msub> <mi>λ</mi> <mi>SAW</mi> </msub> <mo>=</mo> <mn>150</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">m</mi> </mrow> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <mi>H</mi> <mo>=</mo> <mn>70</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">m</mi> </mrow> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mi>P</mi> <mi>el</mi> </msub> <mo>=</mo> <mn>285</mn> <mo> </mo> <mrow> <mi mathvariant="normal">m</mi> <mi mathvariant="normal">W</mi> </mrow> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mi>Q</mi> <mi>total</mi> </msub> <mo>=</mo> <mn>4.6</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">L</mi> <mo> </mo> <mi>min</mi> </mrow> </mrow> </semantics></math><sup>−1</sup>). A main flow was applied in positive <span class="html-italic">y</span>-direction.</p>
Full article ">Figure 12
<p>Particle trajectories calculated in a three-dimensional numerical model with a channel ceiling made of PDMS (<b>a</b>,<b>c</b>) at <math display="inline"><semantics> <mrow> <msub> <mi>λ</mi> <mi>SAW</mi> </msub> <mo>=</mo> <mn>150</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">m</mi> </mrow> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <mi>H</mi> <mo>=</mo> <mn>60</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">m</mi> </mrow> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mi>P</mi> <mi>el</mi> </msub> <mo>=</mo> <mn>285</mn> <mo> </mo> <mrow> <mi mathvariant="normal">m</mi> <mi mathvariant="normal">W</mi> </mrow> </mrow> </semantics></math>, and <math display="inline"><semantics> <mrow> <msub> <mi>Q</mi> <mi>total</mi> </msub> <mo>=</mo> <mn>5.7</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">L</mi> <mo> </mo> <mi>min</mi> </mrow> </mrow> </semantics></math><sup>−1</sup> or silicon (<b>b</b>,<b>d</b>) at <math display="inline"><semantics> <mrow> <msub> <mi>Q</mi> <mi>total</mi> </msub> <mo>=</mo> <mn>6.5</mn> <mo> </mo> <mrow> <mo>μ</mo> <mi mathvariant="normal">L</mi> <mo> </mo> <mi>min</mi> </mrow> </mrow> </semantics></math><sup>−1</sup>. The normalized amplitude <math display="inline"><semantics> <mover accent="true"> <mi>A</mi> <mo>˜</mo> </mover> </semantics></math> of the tasSAW used as boundary condition is depicted in (<b>a</b>,<b>b</b>). The final particle positions at the end of the computational domain are illustrated against the normalized time-averaged absolute acoustic pressure field <math display="inline"><semantics> <mrow> <mo>〈</mo> <mo>|</mo> <msub> <mover accent="true"> <mi>p</mi> <mo>˜</mo> </mover> <mn>1</mn> </msub> <mo>|</mo> <mo>〉</mo> </mrow> </semantics></math> in the channel cross-section in (<b>c</b>,<b>d</b>). The size of the dots corresponds to the number of particles found in the respective location.</p>
Full article ">Figure 13
<p>Measured locations of particles forming clusters at discrete focus positions in the channel cross-section (<b>a</b>). These clusters are located mainly at the two height levels, <math display="inline"><semantics> <msub> <mi>z</mi> <mn>1</mn> </msub> </semantics></math> and <math display="inline"><semantics> <msub> <mi>z</mi> <mn>2</mn> </msub> </semantics></math>. In (<b>b</b>), the distribution of the detected particles is depicted as a function of the depth position <span class="html-italic">z</span> in a histogram.</p>
Full article ">Figure 14
<p>Prolate spheroids dried on a silicon wafer and recorded by scanning electron microscopy (<b>a</b>). The position (<math display="inline"><semantics> <mrow> <mi>x</mi> <mo>,</mo> <mi>y</mi> <mo>,</mo> <mi>z</mi> </mrow> </semantics></math>) and orientation (<math display="inline"><semantics> <mrow> <mi>φ</mi> <mo>,</mo> <mi>θ</mi> </mrow> </semantics></math>) of the non-spherical particles is defined in the coordinate system given in (<b>b</b>), which was adapted from Sachs et al. (2023) [<a href="#B57-powders-04-00002" class="html-bibr">57</a>].</p>
Full article ">Figure 15
<p>Relative frequency of the detected in-plane angle <math display="inline"><semantics> <mi>φ</mi> </semantics></math> (<b>a</b>) and position <span class="html-italic">x</span> of particles along the channel width (<b>b</b>). The preferred orientation of the prolate spheroids with and without the influence of the sSAW is indicated by green ellipses with the main flow direction indicated by black arrows. This figure was adapted from Sachs et al. (2023) [<a href="#B57-powders-04-00002" class="html-bibr">57</a>].</p>
Full article ">Figure 16
<p>Normalized acoustic force component <math display="inline"><semantics> <msub> <mover accent="true"> <mi>F</mi> <mo>˜</mo> </mover> <mi>x</mi> </msub> </semantics></math> acting on a prolate spheroid and a sphere of identical volume against the <span class="html-italic">x</span>-position (<b>a</b>). The numerically calculated data are fitted by smoothing splines. Normalized time-averaged absolute acoustic pressure <math display="inline"><semantics> <mrow> <mo>〈</mo> <mo>|</mo> <msub> <mover accent="true"> <mi>p</mi> <mo>˜</mo> </mover> <mn>1</mn> </msub> <mo>|</mo> <mo>〉</mo> </mrow> </semantics></math> in half the channel cross section with the prolate spheroid depicted at a stable position (<b>b</b>). This figure was adapted from Sachs et al. (2023) [<a href="#B57-powders-04-00002" class="html-bibr">57</a>].</p>
Full article ">Figure A1
<p>Computational mesh covering the channel cross section in the two-dimensional numerical model in a coarse configuration for visualization. Boundary conditions applied to calculate the first- and second-order field quantities are highlighted. This figure was adapted from [<a href="#B51-powders-04-00002" class="html-bibr">51</a>].</p>
Full article ">Figure A2
<p>Three-dimensional numerical model along with the imposed boundary condition to calculate the first- and second-order quantities in a schematic representation (<b>a</b>). A detailed view on the prolate spheroid modeled as a solid domain within the fluid is given in subfigure (<b>b</b>). This figure was adapted from [<a href="#B57-powders-04-00002" class="html-bibr">57</a>].</p>
Full article ">Figure A3
<p>Schematic representation of the acoustofluidic device in a cross-sectional view. Counter-propagating SAWs are excited by two opposing IDTs, which radiate energy into the fluid-filled microchannel consisting of side walls made of DFR and a channel cover of silicon.</p>
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14 pages, 2695 KiB  
Article
Sound-Induced Round Window Vibration—Experiment and Numerical Simulations of Energy Transfer Through the Cochlea of the Human Ear
by Robert Zablotni, Sylwester Tudruj, Jaroslaw Latalski, Marcin Szymanski, Andrzej Kucharski, Grzegorz Zając and Rafał Rusinek
Appl. Sci. 2025, 15(1), 301; https://doi.org/10.3390/app15010301 - 31 Dec 2024
Viewed by 531
Abstract
This study investigates the dynamic properties of the human middle ear and the energy transfer phenomena between the stapes footplate (SF) and the round window membrane (RWM) under sound stimulation. A series of laboratory tests were conducted, and a numerical model of the [...] Read more.
This study investigates the dynamic properties of the human middle ear and the energy transfer phenomena between the stapes footplate (SF) and the round window membrane (RWM) under sound stimulation. A series of laboratory tests were conducted, and a numerical model of the system was prepared. During the experiments, vibrations in human temporal bones were recorded using a Laser Doppler Vibrometer (LDV), and the frequency response functions (FRFs) of the RWM and SF footplate were computed. Key resonances were identified, with notable differences in vibration amplitude depending on whether the artificial external ear canal was left open or closed. To evaluate the amplification of acoustic waves within the cochlea, the authors proposed a novel index defined as the ratio of the FRF of the RWM and SF, respectively. The performed computations showed that signal amplification is particularly noticeable in the frequency range from 1 to 2 kHz. Subsequently, a simplified computational fluid dynamics (CFD) model of the cochlea was developed to simulate internal pressure distribution within the scala vestibuli (SV) and scala tympani (ST) spaces. The numerical computations of acoustic signal amplification showed good agreement with the experimental data, particularly at the frequencies of 1 and 2 kHz. These findings provide new insights into cochlear acoustics and offer a potential tool for evaluating pathological disorders and designing prosthetic devices. Full article
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Figure 1

Figure 1
<p>Scheme of experimental setup used in experiment on temporal bone.</p>
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<p>RWM vibration and stapes footplate (SF) vibration as frequency response functions for open (red) and closed (blue) artificial ear canal.</p>
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<p>FRF ratios (<span class="html-italic">H<sub>TV(RWM)</sub></span>/<span class="html-italic">H<sub>TV(SF)</sub></span>) measured for the RWM (<span class="html-italic">H<sub>TV(RWM)</sub></span>) and the stapes footplate (<span class="html-italic">H<sub>TV(SF)</sub></span>) from experiments with open (red) and closed (blue) canals. Black points represent outcomes from CFD simulations.</p>
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<p>The inner ear model with visible surfaces (<span class="html-italic">s</span>1 and <span class="html-italic">s</span>2) representing the equivalent of the basilar membrane.</p>
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<p>Trend of basilar membrane stiffness (<span class="html-italic">k</span>) relative to position from the basilar membrane’s origin.</p>
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<p>(<b>a</b>) Single spring–damper element of the basilar membrane model: <span class="html-italic">k</span>—spring element, <span class="html-italic">c</span>—damper element, <span class="html-italic">m</span>—mass of the element, <span class="html-italic">s</span>1 and <span class="html-italic">s</span>2—surface 1 and surface 2. (<b>b</b>) Independent spring–damper elements (<span class="html-italic">e</span>1, <span class="html-italic">e</span>2, <span class="html-italic">e</span>3) constitute the basilar membrane.</p>
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<p>The initial stages of the inner-ear simulation with a visible traveling pressure wave: (<b>a</b>)—3.75 × 10<sup>−6</sup> s; (<b>b</b>)—1.5 × 10<sup>−5</sup> s; (<b>c</b>)—3.0 × 10<sup>−5</sup> s.</p>
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34 pages, 15971 KiB  
Review
MEMS Acoustic Sensors: Charting the Path from Research to Real-World Applications
by Qingyi Wang, Yang Zhang, Sizhe Cheng, Xianyang Wang, Shengjun Wu and Xufeng Liu
Micromachines 2025, 16(1), 43; https://doi.org/10.3390/mi16010043 - 30 Dec 2024
Viewed by 3806
Abstract
MEMS acoustic sensors are a type of physical quantity sensor based on MEMS manufacturing technology for detecting sound waves. They utilize various sensitive structures such as thin films, cantilever beams, or cilia to collect acoustic energy, and use certain transduction principles to read [...] Read more.
MEMS acoustic sensors are a type of physical quantity sensor based on MEMS manufacturing technology for detecting sound waves. They utilize various sensitive structures such as thin films, cantilever beams, or cilia to collect acoustic energy, and use certain transduction principles to read out the generated strain, thereby obtaining the targeted acoustic signal’s information, such as its intensity, direction, and distribution. Due to their advantages in miniaturization, low power consumption, high precision, high consistency, high repeatability, high reliability, and ease of integration, MEMS acoustic sensors are widely applied in many areas, such as consumer electronics, industrial perception, military equipment, and health monitoring. Through different sensing mechanisms, they can be used to detect sound energy density, acoustic pressure distribution, and sound wave direction. This article focuses on piezoelectric, piezoresistive, capacitive, and optical MEMS acoustic sensors, showcasing their development in recent years, as well as innovations in their structure, process, and design methods. Then, this review compares the performance of devices with similar working principles. MEMS acoustic sensors have been increasingly widely applied in various fields, including traditional advantage areas such as microphones, stethoscopes, hydrophones, and ultrasound imaging, and cutting-edge fields such as biomedical wearable and implantable devices. Full article
(This article belongs to the Special Issue Recent Advances in Silicon-Based MEMS Sensors and Actuators)
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Figure 1

Figure 1
<p>Classification of MEMS acoustic sensors based on different working principles.</p>
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<p>Piezoelectric MEMS acoustic sensors. (<b>a</b>) Basic working principle and typical multilayer structure of piezoelectric MEMS acoustic sensors. (<b>b</b>) A ZnO MEMS acoustic sensor with air cavity [<a href="#B29-micromachines-16-00043" class="html-bibr">29</a>]. (<b>c</b>) Multilayer cantilever design of a piezoelectric MEMS microphone, with AlN as piezoelectric material and MO as an electrode material [<a href="#B30-micromachines-16-00043" class="html-bibr">30</a>].</p>
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<p>Piezoelectric MEMS acoustic sensor based on ZnO film. (<b>a</b>) ZnO based structure for development of MEMS acoustic sensor [<a href="#B29-micromachines-16-00043" class="html-bibr">29</a>]. (<b>b</b>–<b>d</b>) The cavity structure with microtunnel design, which relates to the atmosphere, as a replacement of the traditional acoustic holes. (<b>b</b>) The fabricated cavity and metal electrode structure of ZnO MEMS acoustic sensor [<a href="#B48-micromachines-16-00043" class="html-bibr">48</a>]. (<b>c</b>) A ZnO MEMS acoustic sensor for aeroacoustic measurements [<a href="#B50-micromachines-16-00043" class="html-bibr">50</a>]. (<b>d</b>) A MEMS acoustic sensor with microtunnel for high SPL measurement, and with less risk of microtunnel blockages [<a href="#B51-micromachines-16-00043" class="html-bibr">51</a>].</p>
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<p>Piezoelectric MEMS acoustic sensor based on AlN. (<b>a</b>) A AlN pMUT based on the compatibility characteristics between AlN and CMOS processes [<a href="#B53-micromachines-16-00043" class="html-bibr">53</a>]. (<b>b</b>) AlN MEMS acoustic sensor aiming for ultra low working frequency [<a href="#B54-micromachines-16-00043" class="html-bibr">54</a>]. (<b>c</b>) AlN MEMS acoustic sensor with ultra-thin silicon substrate, and different structures for low and high working frequency [<a href="#B56-micromachines-16-00043" class="html-bibr">56</a>]. (<b>d</b>) AlN MEMS acoustic sensor with enhanced SNR (67.03 dB at 1 kHz) [<a href="#B22-micromachines-16-00043" class="html-bibr">22</a>]. (<b>e</b>) AlN MEMS hydrophone with high sensitivity (−178 dB, re. 1 V/μPa) and low noise density (52.6 dB@100 Hz, re. μPa/√Hz) [<a href="#B58-micromachines-16-00043" class="html-bibr">58</a>]. (<b>f</b>) AlN MEMS wideband (10 Hz to more than 10 kHz) acoustic sensor coated by organic film (elastic polyurethane) [<a href="#B59-micromachines-16-00043" class="html-bibr">59</a>].</p>
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<p>Piezoelectric MEMS hydrophone. (<b>a</b>) A face to face, cross-configuration of four cantilevers design [<a href="#B67-micromachines-16-00043" class="html-bibr">67</a>]. (<b>b</b>) Single cantilever beam design [<a href="#B68-micromachines-16-00043" class="html-bibr">68</a>].</p>
Full article ">Figure 6
<p>Wearable acoustic sensor based on piezoelectric method. (<b>a</b>) Air-silicone composite device for physiological sounds detection [<a href="#B69-micromachines-16-00043" class="html-bibr">69</a>,<a href="#B72-micromachines-16-00043" class="html-bibr">72</a>]. (<b>b</b>) MEMS bionic hydrophone for heart sound sensing [<a href="#B73-micromachines-16-00043" class="html-bibr">73</a>].</p>
Full article ">Figure 7
<p>Representative structure and working principle diagram of piezoresistive MEMS hydrophone.</p>
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<p>Piezoresistive MEMS acoustic sensor. (<b>a</b>) Low-frequency-detectable acoustic sensor using a piezoresistive cantilever [<a href="#B57-micromachines-16-00043" class="html-bibr">57</a>]. (<b>b</b>) Frequency-specific highly sensitive acoustic sensor using a piezoresistive cantilever and parallel Helmholtz resonators [<a href="#B81-micromachines-16-00043" class="html-bibr">81</a>].</p>
Full article ">Figure 9
<p>Piezoresistive hydrophones with cilium structure. (<b>a</b>) Traditional cilium design in piezoresistive hydrophones [<a href="#B88-micromachines-16-00043" class="html-bibr">88</a>]. (<b>b</b>) CCVH: cilia cluster vector hydrophone [<a href="#B85-micromachines-16-00043" class="html-bibr">85</a>]. (<b>c</b>) DCVH: dumbbell-shaped ciliary vector hydrophone [<a href="#B86-micromachines-16-00043" class="html-bibr">86</a>]. (<b>d</b>) HCVH: hollow cilium cylinder vector hydrophone [<a href="#B87-micromachines-16-00043" class="html-bibr">87</a>]. (<b>e</b>) BCVH: beaded cilia MEMS vector hydrophone [<a href="#B88-micromachines-16-00043" class="html-bibr">88</a>]. (<b>f</b>) CSCVH: cap-shaped ciliary vector hydrophone [<a href="#B89-micromachines-16-00043" class="html-bibr">89</a>]. (<b>g</b>) SCVH: sculpture-shape cilium MEMS vector hydrophone [<a href="#B90-micromachines-16-00043" class="html-bibr">90</a>]. (<b>h</b>) CCCVH: crossed-circle cilium vector hydrophone [<a href="#B91-micromachines-16-00043" class="html-bibr">91</a>].</p>
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<p>Piezoresistive hydrophones with multiple cilium structure. (<b>a</b>,<b>b</b>) FUVH: four-unit MEMS vector hydrophone [<a href="#B93-micromachines-16-00043" class="html-bibr">93</a>,<a href="#B95-micromachines-16-00043" class="html-bibr">95</a>]. (<b>c</b>) FUVH with annulus-shaped structure [<a href="#B94-micromachines-16-00043" class="html-bibr">94</a>].</p>
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<p>Representative structure and working principle diagram of capacitive MEMS acoustic sensors.</p>
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<p>Capacitive MEMS Microphone. (<b>a</b>) Low-power digital capacitive MEMS microphone based on a triple-sampling delta-sigma ADC with embedded gain [<a href="#B101-micromachines-16-00043" class="html-bibr">101</a>]. (<b>b</b>) Wearable capacitive MEMS microphone for cardiac monitoring at the wrist [<a href="#B102-micromachines-16-00043" class="html-bibr">102</a>]. (<b>c</b>) Capacitive MEMS stethoscope with anti-stiction-dimple array design in the diaphragm and the backplate for highly reliable heart or lung sounds detection [<a href="#B105-micromachines-16-00043" class="html-bibr">105</a>].</p>
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<p>Capacitive MEMS microphone with biomimetic design. (<b>a</b>) Dual-band MEMS directional acoustic sensor for near-resonance operation [<a href="#B110-micromachines-16-00043" class="html-bibr">110</a>]. (<b>b</b>) Directional-resonant MEMS acoustic sensor and associated acoustic vector sensor [<a href="#B111-micromachines-16-00043" class="html-bibr">111</a>]. Both (<b>a</b>,<b>b</b>) are inspired by the tympana configuration of the parasitic fly <span class="html-italic">Ormia ochracea</span>. The circled numbers in (<b>b</b>) are used to distinguish different structures.</p>
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<p>MEMS acoustic sensor based on optical grating interferometer. (<b>a</b>) A grating interferometer design by a diffraction grating integrated backplate and a pressure-sensitive diaphragm [<a href="#B117-micromachines-16-00043" class="html-bibr">117</a>]. (<b>b</b>) Design of a MEMS optical microphone transducer based on light phase modulation [<a href="#B120-micromachines-16-00043" class="html-bibr">120</a>]. (<b>c</b>) Grating interferometer design with short-cavity structure and grating-on-convex-platform structure [<a href="#B118-micromachines-16-00043" class="html-bibr">118</a>,<a href="#B119-micromachines-16-00043" class="html-bibr">119</a>].</p>
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<p>MEMS acoustic sensor based on Fabry–Perot method. (<b>a</b>) A typical structure of Fabry–Perot MEMS acoustic sensors. (<b>b</b>) An acoustic sensor based on active fiber Fabry–Pérot microcavities [<a href="#B21-micromachines-16-00043" class="html-bibr">21</a>]. (<b>c</b>) An application in the detection and position of partial discharge [<a href="#B122-micromachines-16-00043" class="html-bibr">122</a>].</p>
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<p>Applications of MEMS acoustic sensors in biomedical field.</p>
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31 pages, 28202 KiB  
Article
Analysis of Acoustic Surface Wave Focused Unidirectional Interdigital Transducers Using Coupling-of-Mode Theory
by Guopeng Hui, Tinglun Ao, Haotian Liu, Minglei Li and Chen Chen
Micromachines 2025, 16(1), 3; https://doi.org/10.3390/mi16010003 - 24 Dec 2024
Viewed by 561
Abstract
In cell or droplet separation, high acoustic wave energy of a surface acoustic wave (SAW) device is required to generate sufficient acoustic radiation force. In this paper, the electrode width-control floating electrode focused unidirectional interdigital transducer (EWC-FEFUDT) is proposed due to its enhanced [...] Read more.
In cell or droplet separation, high acoustic wave energy of a surface acoustic wave (SAW) device is required to generate sufficient acoustic radiation force. In this paper, the electrode width-control floating electrode focused unidirectional interdigital transducer (EWC-FEFUDT) is proposed due to its enhanced focusing properties. The performance of the EWC-FEFUDT is investigated using the Coupling-of-Mode (COM) theory, and the COM parameter is extracted using the Finite Element Method (FEM). The four different forbidden band edge frequencies account for the unidirectionality of the proposed EWC-FEFUDT. A direction angle of ϕκϕζ=44.5° of the EWC-FEFUDT (Design 3) is obtained, being fairly close to the optimum value of 45°. The EWC-FEFUDT (Design 3) has a lower insertion loss (IL) of −5.1 dB and greater unidirectionality (20 × log10(D) = 13.8 dB). The SAW maximum amplitude of the EWC-FEFUDT (Design 3) is increased by about 1.5×104 µm compared to that of the focused interdigital transducers (FIDTs). The maximum acoustic pressure of the EWC-FEFUDT is an order of magnitude higher than that of FIDTs. The EWC-FEFUDT exhibits enhanced focusing properties. The proposed EWC-FEFUDT may provide an alternative method for cell or droplet separation in an efficient manner. Full article
Show Figures

Figure 1

Figure 1
<p>Various types of IDTs. (<b>a</b>) Conventional uniform IDT; (<b>b</b>) FIDT; (<b>c</b>) EWC-UDT; (<b>d</b>) FEUDT; (<b>e</b>) SPFT; (<b>f</b>) FUDT.</p>
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<p>EWC-FEFUDT.</p>
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<p>Schematic diagram of particle separation using EWC-FEFUDT (<b>a</b>) x–y plane view; (<b>b</b>) view of y–z cross-section taken along the line AA’ of (<b>a</b>).</p>
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<p>The complete FEM model of the EWC-FEFUDT.</p>
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<p>Elements and nodes of FEM model of EWC-FEFUDT.</p>
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<p>A single-period FEM model of the EWC-FEFUDT and the mesh convergence analysis. (<b>a</b>) A single-period FEM model of the EWC-FEFUDT; (<b>b</b>) meshes of a single-period FEM model of the EWC-FEFUDT; (<b>c</b>) mesh convergence analysis.</p>
Full article ">Figure 7
<p>The total displacements of eigenmodes. (<b>a</b>) The lower frequency of the forbidden band in a short-circuited grating; (<b>b</b>) the upper frequency of the forbidden band in a short-circuited grating; (<b>c</b>) the lower frequency of the forbidden band in an open-circuited grating; (<b>d</b>) the upper frequency of the forbidden band in an open-circuited grating.</p>
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<p>The displacement components of <a href="#micromachines-16-00003-f007" class="html-fig">Figure 7</a>a.</p>
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<p>Admittance curves of EWC-FEFUDT on 128°Y-X LiNbO<sub>3</sub>.</p>
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<p>Two-dimensional FEM models of the SAW device. (<b>a</b>) The model for the analysis of the EWC-FEFUDT; (<b>b</b>) the model for the IL calculation of the EWC-FEFUDT.</p>
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<p>The effect of <math display="inline"><semantics> <mrow> <mi>n</mi> </mrow> </semantics></math> on the IL of the EWC-FEFUDT.</p>
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<p>The effect of <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>D</mi> </mrow> <mrow> <mi>a</mi> </mrow> </msub> </mrow> </semantics></math> on IL of the EWC-FEFUDT.</p>
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<p>IL of EWC-FEFUDT with different electrode thicknesses.</p>
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<p>Effect of <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> </mrow> </semantics></math> on IL of EWC-FEFUDT.</p>
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<p>EWC-FEFUDT loss for different <math display="inline"><semantics> <mrow> <mi>L</mi> </mrow> </semantics></math>. (<b>a</b>) Insertion loss; (<b>b</b>) return loss.</p>
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<p>S parameters. (<b>a</b>) FIDT; (<b>b</b>) EWC-FEFUDT.</p>
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<p>Focus region of EWC-FEFUDT.</p>
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<p>The half-symmetry FEM model of the EWC-FEFUDT. (<b>a</b>) The model for the analysis of SAW displacement; (<b>b</b>) the model for the analysis of acoustic pressure.</p>
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<p>The effect of <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>D</mi> </mrow> <mrow> <mi>a</mi> </mrow> </msub> </mrow> </semantics></math> on SAW displacement and acoustic pressure. (<b>a</b>) SAW displacement for <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>D</mi> </mrow> <mrow> <mi>a</mi> </mrow> </msub> <mo>=</mo> <mn>30</mn> <mo>°</mo> </mrow> </semantics></math> (Design 3); (<b>b</b>) acoustic pressure for <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>D</mi> </mrow> <mrow> <mi>a</mi> </mrow> </msub> <mo>=</mo> <mn>30</mn> <mo>°</mo> </mrow> </semantics></math> (Design 3); (<b>c</b>) SAW displacement for <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>D</mi> </mrow> <mrow> <mi>a</mi> </mrow> </msub> <mo>=</mo> <mn>60</mn> <mo>°</mo> </mrow> </semantics></math> (Design 4); (<b>d</b>) acoustic pressure for <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>D</mi> </mrow> <mrow> <mi>a</mi> </mrow> </msub> <mo>=</mo> <mn>60</mn> <mo>°</mo> </mrow> </semantics></math> (Design 4); (<b>e</b>) SAW displacement for <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>D</mi> </mrow> <mrow> <mi>a</mi> </mrow> </msub> <mo>=</mo> <mn>90</mn> <mo>°</mo> </mrow> </semantics></math> (Design 5); (<b>f</b>) acoustic pressure for <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>D</mi> </mrow> <mrow> <mi>a</mi> </mrow> </msub> <mo>=</mo> <mn>90</mn> <mo>°</mo> </mrow> </semantics></math> (Design 5).</p>
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<p>Effect of <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> </mrow> </semantics></math> on acoustic pressure and SAW displacement. (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> <mo>=</mo> <mn>45</mn> <mo> </mo> <mi>µ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math> (Design 3); (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> <mo>=</mo> <mn>65</mn> <mo> </mo> <mi>µ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math> (Design 8); (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> <mo>=</mo> <mn>85</mn> <mo> </mo> <mi>µ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math> (Design 9); (<b>d</b>) x component of SAW displacement in the Design 3 (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> <mo>=</mo> <mn>45</mn> <mo> </mo> <mi>µ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>), Design 8 (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> <mo>=</mo> <mn>65</mn> <mo> </mo> <mi>µ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>), and Design 9 (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> <mo>=</mo> <mn>85</mn> <mo> </mo> <mi>µ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>).</p>
Full article ">Figure 20 Cont.
<p>Effect of <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> </mrow> </semantics></math> on acoustic pressure and SAW displacement. (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> <mo>=</mo> <mn>45</mn> <mo> </mo> <mi>µ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math> (Design 3); (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> <mo>=</mo> <mn>65</mn> <mo> </mo> <mi>µ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math> (Design 8); (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> <mo>=</mo> <mn>85</mn> <mo> </mo> <mi>µ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math> (Design 9); (<b>d</b>) x component of SAW displacement in the Design 3 (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> <mo>=</mo> <mn>45</mn> <mo> </mo> <mi>µ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>), Design 8 (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> <mo>=</mo> <mn>65</mn> <mo> </mo> <mi>µ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>), and Design 9 (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>L</mi> </mrow> </msub> <mo>=</mo> <mn>85</mn> <mo> </mo> <mi>µ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>).</p>
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<p>Substrate displacement and acoustic pressure distribution. (<b>a</b>) FEM model for calculating displacement amplitude in FIDT; (<b>b</b>) FEM model for calculating displacement amplitude in EWC-FEFUDT; (<b>c</b>) SAW displacements generated by FIDT and EWC-FEFUD in +X direction of (<b>a</b>,<b>b</b>); (<b>d</b>) acoustic pressure generated by EWC-FEFUDT; (<b>e</b>) acoustic pressure generated by FIDT.</p>
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<p>SAW displacements generated by EWC-FEFUDT and FIDT. (<b>a</b>) Total displacement generated by EWC-FEFUDT; (<b>b</b>) SAW displacement generated by EWC-FEFUDT along red line of (<b>a</b>); (<b>c</b>) Total displacement generated by FIDT; (<b>d</b>) SAW displacement generated by FIDT along red line of (<b>c</b>).</p>
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<p>SAW standing wave distributions. (<b>a</b>) SAW standing waves under short-circuit conditions; (<b>b</b>) SAW standing waves under open circuit conditions.</p>
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<p>The relationships between COM parameters and normalized electrode thicknesses. (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>C</mi> </mrow> <mrow> <mi>p</mi> </mrow> </msub> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <mi>v</mi> </mrow> </semantics></math> versus normalized electrode thickness; (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>κ</mi> </mrow> <mrow> <mn>12</mn> </mrow> </msub> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <mi>ζ</mi> </mrow> </semantics></math> versus normalized electrode thickness; (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ϕ</mi> </mrow> <mrow> <mi>κ</mi> </mrow> </msub> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ϕ</mi> </mrow> <mrow> <mi>ζ</mi> </mrow> </msub> </mrow> </semantics></math> versus normalized electrode thickness; (<b>d</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ϕ</mi> </mrow> <mrow> <mi>κ</mi> </mrow> </msub> <mo>−</mo> <msub> <mrow> <mi>ϕ</mi> </mrow> <mrow> <mi>ζ</mi> </mrow> </msub> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <mi>D</mi> </mrow> </semantics></math> versus normalized electrode thickness.</p>
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<p>Two fibers. (<b>a</b>) Coupled fibers; (<b>b</b>) fibers without coupling.</p>
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<p>Input and output for an arbitrary section.</p>
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<p>Symmetric and anti-symmetric modes. (<b>a</b>) Symmetric modes; (<b>b</b>) anti-symmetric modes.</p>
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<p>Periodic structure.</p>
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<p>Reflection coefficient <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Γ</mi> </mrow> <mrow> <mo>±</mo> </mrow> </msub> </mrow> </semantics></math> of periodic structure.</p>
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<p>Single-periodic structure of the EWC-FEFUDT.</p>
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<p>Unit section of EWC-FEFUDT.</p>
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<p>Current on busbar of EWC-FEFUDT.</p>
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<p>(<b>a</b>) Shorted-circuited gratings; (<b>b</b>) open-circuited gratings.</p>
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59 pages, 20006 KiB  
Review
Magnetoelectric BAW and SAW Devices: A Review
by Bin Luo, Prasanth Velvaluri, Yisi Liu and Nian-Xiang Sun
Micromachines 2024, 15(12), 1471; https://doi.org/10.3390/mi15121471 - 3 Dec 2024
Viewed by 1533
Abstract
Magnetoelectric (ME) devices combining piezoelectric and magnetostrictive materials have emerged as powerful tools to miniaturize and enhance sensing and communication technologies. This paper examines recent developments in bulk acoustic wave (BAW) and surface acoustic wave (SAW) ME devices, which demonstrate unique capabilities in [...] Read more.
Magnetoelectric (ME) devices combining piezoelectric and magnetostrictive materials have emerged as powerful tools to miniaturize and enhance sensing and communication technologies. This paper examines recent developments in bulk acoustic wave (BAW) and surface acoustic wave (SAW) ME devices, which demonstrate unique capabilities in ultra-sensitive magnetic sensing, compact antennas, and quantum applications. Leveraging the mechanical resonance of BAW and SAW modes, ME sensors achieve the femto- to pico-Tesla sensitivity ideal for biomedical applications, while ME antennas, operating at acoustic resonance, allow significant size reduction, with high radiation gain and efficiency, which is suited for bandwidth-restricted applications. In addition, ME non-reciprocal magnetoacoustic devices using hybrid magnetoacoustic waves present novel solutions for RF isolation, which have also shown potential for the efficient control of quantum defects, such as negatively charged nitrogen-vacancy (NV) centers. Continued advancements in materials and device structures are expected to further enhance ME device performance, positioning them as key components in future bio-sensing, wireless communication, and quantum information technologies. Full article
(This article belongs to the Special Issue Novel Surface and Bulk Acoustic Wave Devices)
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Figure 1

Figure 1
<p>Magnetoelectric (ME) device possibilities using BAW and SAW concepts. The ME devices include magnetic sensors, antennas, isolators, and filters.</p>
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<p>(<b>a</b>) Schematic diagram of the Metglas/piezo fiber ME sensor configuration, featuring ID electrodes on the PMN-PT fiber core composite and symmetric three-layer Metglas actuators. (<b>b</b>) Exploded view of individual components. (<b>c</b>) Illustration of multiple alternating push–pull units for enhanced ME coupling. (<b>d</b>) Optical microscopy image of a longitudinally poled push–pull element within the core composite. (<b>e</b>) Photographs of the fully assembled Metglas/piezo fiber ME sensor. Reproduced with permission from Refs. [<a href="#B17-micromachines-15-01471" class="html-bibr">17</a>,<a href="#B64-micromachines-15-01471" class="html-bibr">64</a>]. Copyright 2021 IEEE; Copyright 2011 John Wiley and Sons.</p>
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<p>(<b>a</b>) Process flow of cantilever-based ME sensors. (<b>b</b>) Bonding process flow of capped wafer to effectively improve the mechanical quality factor and reduce the equivalent magnetic noise. (<b>c</b>) Photographs of ME sensor die on wafer (<b>d</b>) cantilever-based ME sensor with (1) ME cantilever, (2) etch groove, (3) bond frame, and (4) bond pads. Reprinted with permission from Ref. [<a href="#B222-micromachines-15-01471" class="html-bibr">222</a>]. Copyright Elsevier 2013.</p>
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<p>Magnetically modulated cantilever ME sensor with antiparallel exchange bias (APEB) stack. (<b>a</b>) The sketch illustrates the ME cantilever design with the magnetic field sensing axis indicated. A cross-sectional view highlights the ME sensor’s structure, showing the Si substrate, a piezoelectric AlN layer, a Pt and Au electrode, and the magnetostrictive layer. The magnetostrictive layer consists of a repeated multilayer structure with Ta/Cu seed layers, an antiferromagnetic MnIr layer, and a magnetostrictive FeCoSiB phase. This structure includes a 20× repeated two-layer configuration. Key magnetic parameters are indicated, including the uniaxial anisotropy axis K<sub>u</sub>, the exchange bias field H<sub>eb</sub>, and the magnetic stray field distribution H<sub>stray</sub>. (<b>b</b>) A diagram shows the temporal application of temperature and magnetic field during the annealing process. (<b>c</b>) An inductive measurement shows the magnetization loop along the alternating EB axis, with a magnetization loop from a parallel exchange-biased (PEB) sample included for comparison. (<b>d</b>) Magnetic domain (MD) structures at 300 °C after demagnetizing the sensor and achieving a stabilized magnetization state at room temperature (RT) for the APEB sensor. The alignment of magnetization M, the EB field H<sub>eb</sub> in the top layer, the sensor’s magnetic field sensing axis, and the magneto-optical sensitivity (MO) axis are depicted. Reprinted with permission from Ref. [<a href="#B181-micromachines-15-01471" class="html-bibr">181</a>]. Copyright 2019 AIP Publishing.</p>
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<p>Magnetic domain behavior and noise performance of magnetically modulated cantilever ME sensor with antiparallel exchange bias (APEB) stack and PEB stack. (<b>a</b>) A full-sensor view of the APEB’s magnetic domain structure, with magnetization directions marked by arrows. (<b>c</b>) A full-sensor view for the PEB sensor, highlighting differences in magnetic domain patterns compared to APEB. (<b>b</b>,<b>d</b>) Provide high-resolution domain images of specific regions at the right cantilever edge (indicated by red dashed boxes in (<b>a</b>,<b>c</b>)) for both APEB and PEB, respectively, illustrating domain behavior with and without an applied magnetic field. Dashed arrows denote the magnetization alignment in the second, non-visible FeCoSiB layer. (<b>e</b>) The magnetoelectric (ME) coefficient α<sub>ME</sub> changes with bias field H<sub>bias</sub> at the mechanical resonance frequency f<sub>res</sub>. (<b>f</b>) Frequency spectra of voltage noise density V<sub>ME</sub> for both APEB and PEB sensors under the same modulation H<sub>mod</sub> and signal fields H<sub>sig</sub>. (<b>g</b>) Voltage noise dependency on H<sub>mod</sub>, highlighting the sensitivity to modulation field strength. (<b>h</b>) and (<b>i</b>) show linearity plots of f<sub>res</sub> and magnetic frequency conversion (MFC) mode for a ME sensor with APEB and PEB phases, respectively. Noise floors and optimal H<sub>bias</sub> and H<sub>mod</sub> values for resonance and MFC modes are indicated, showing comparative sensor performance across configurations. Reproduced with permission from Ref. [<a href="#B181-micromachines-15-01471" class="html-bibr">181</a>]. Copyright 2019 AIP Publishing.</p>
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<p>Electrically modulated ME sensors with AlN layer for voltage output. (<b>a</b>) The schematic shows a magnetoelectric (ME) composite sample with three active layers: an exchange-biased FeCoSiB layer serving as the magnetostrictive phase, an AlN layer as the linear piezoelectric phase for readout, and an unpoled PZT layer as the nonlinear piezoelectric phase for excitation. (<b>b</b>) Displacement–voltage characteristic curve of the ME cantilever showing responses of both piezoelectric phases under a DC electric field. (<b>c</b>) The sensor output spectrum from the AlN layer when the PZT layer is excited at its mechanical resonance frequency of <span class="html-italic">f</span><sub>mod</sub> = 689 Hz. (<b>d</b>) Sensor output spectrum from the AlN layer with the carrier signal frequency <span class="html-italic">f</span><sub>res</sub> = <span class="html-italic">f</span><sub>mod</sub> = 669 Hz, applied at 20 Hz below the mechanical resonance. (<b>e</b>) A linearity test under a 10 Hz magnetic field demonstrates that the noise floor reaches approximately 10 nT/√Hz. Reproduced with permission from Ref. [<a href="#B11-micromachines-15-01471" class="html-bibr">11</a>]. Copyright 2016 AIP Publishing.</p>
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<p>Electrically modulated U-mode ME sensors with a picking-up coil for voltage output. (<b>a</b>) Schematic setup: a composite, embedded in a pickup coil, is shown. The piezoelectric (PE) plate capacitor functions as the input, while the tuned pickup coil, coupled with an amplifier, provides the output signal. (<b>b</b>) Circuit representation: the ME composite is modeled as a radiative capacitor. The pickup coil generates a signal that is buffered by a low-noise, unity-gain buffer amplifier, enhancing signal integrity. (<b>c</b>) Frequency response analysis: the self-resonant frequency of the pickup coil (with quality factor Q∼150) and the mechanical resonance frequency (with quality factor Q∼1000, labeled as UM) are shown. Tuning the system maximizes voltage output at resonance, with de-tuning options also analyzed. (<b>d</b>) Wide frequency response: a broad response shows coil resonance effects and two distinct voltage peaks correspond to mechanical resonances of the system. (<b>e</b>) MOKE microscopy image: the full cantilever length is captured after magnetic field decay, showing magnetization along the thermally induced magnetic easy axis (K<sub>u</sub>). Applied magnetic fields (H) align with the hard axis, while the left end of the cantilever is fixed to the PCB. (<b>f</b>) Vibrometry measurements showing the U-mode at 514.8 kHz. (<b>g</b>) Sensitivity at zero field showing a linear increase with rising carrier voltage amplitude. (<b>h</b>) Voltage noise characteristics versus carrier amplitude. At low frequencies (&lt;20 Hz), two regimes are identified based on carrier amplitude. Below 200 mV, noise increases only slightly, while above 200 mV, noise surges by nearly seven times for an additional 100 mV of excitation. Inset shows the noise spectra for 80 mV and 220 mV cases; the 220 mV excitation exhibits a noticeable pedestal and increased broadband noise. (<b>i</b>) LOD is assessed across different test frequencies, showing an exponential noise increase towards the carrier, which limits sensor performance. Reproduced from Ref. [<a href="#B10-micromachines-15-01471" class="html-bibr">10</a>].</p>
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<p>Low-noise inverse ME sensor based on electrically modulated U mode and exchange bias stack with a pickup coil. (<b>a</b>) Schematic of cantilever sensors in the inverse magnetoelectric configuration, featuring a simplified pickup coil covering the cantilever’s entire free length except where it connects to the circuit board. The measurement and bias field directions are shown by the blue arrow, while the orange arrow indicates the magnetic field direction applied during annealing. (<b>b</b>) Finite Element Method (FEM)-derived deflection of the cantilever in the U mode, depicted with amplified amplitude to illustrate bending. (<b>c</b>) Diagram of the advanced layer stack design for magnetic flux closure, showing Ta/Cu/MnIr layers, with each exchange-coupled to a FeCoSiB layer. The arrows represent potential magnetic flux closure and the preferred magnetization direction without cantilever excitation. (<b>d</b>) BH-Looper hysteresis curves for heat-treated single-layer (SL) and multi-layer (ML) samples (8 × 500 nm exchange bias layers) measured along the cantilever’s long axis, both with a total FeCoSiB thickness of 4 μm. (<b>e</b>) Magneto-optical Kerr micrographs of demagnetized domain patterns in SL and ML samples along the long axis, with sensitivity axis oriented along the cantilever’s short side. (<b>f</b>) Sideband amplitude response at several magnetic test signal amplitudes at 10 Hz, demonstrating extended linear behavior. (<b>g</b>) Equivalent magnetic noise density with limit of detection (LOD) calculated at 10 Hz (blue), 33 Hz (black), and 70 Hz (green), showing noise reduction and improved LOD at higher frequencies with a constant sensitivity of 85 kV/T across test fields from 10 to 70 Hz. Reproduced from Ref. [<a href="#B13-micromachines-15-01471" class="html-bibr">13</a>].</p>
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<p>Multimode delta-E effect magnetic field sensors with adapted electrodes. (<b>a</b>) Schematic cross-section of the cantilever beam, (<b>b</b>) top view of the cantilever showing the various electrode designs, (<b>c</b>) calculated deflection of the cantilever in the first and second transverse bending modes according to Euler–Bernoulli beam theory, and (<b>d</b>) photograph of the sensing cantilever mounted within a silicon frame. Effective noise level for the (<b>e</b>) first and (<b>f</b>) second modes. Reproduced with permission from Ref. [<a href="#B221-micromachines-15-01471" class="html-bibr">221</a>]. Copyright 2016 AIP Publishing.</p>
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<p>(<b>a</b>) Schematic and (<b>b</b>) layered structure of the ME sensor. Scanning electron microscopy images of the (<b>c</b>) fabricated MEMS ME sensor and the (<b>d</b>) cross-section. Reproduced from Ref. [<a href="#B180-micromachines-15-01471" class="html-bibr">180</a>].</p>
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<p>(<b>a</b>) MBVD model fitting for admittance curve of the ME sensor. (<b>b</b>) The equivalent MBVD circuit of the ME resonator. (<b>c</b>) Admittance curves of the ME resonator under different DC bias magnetic fields. (<b>d</b>) EMR frequency and peak admittance amplitude at the resonance frequency versus DC magnetic fields. Reproduced from Ref. [<a href="#B180-micromachines-15-01471" class="html-bibr">180</a>].</p>
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<p>Self-biased NPR array dual-band ME sensor/antenna. (<b>a</b>) A 3D schematic of the ME sensor/antenna. (<b>b</b>) Optical image of a fabricated smart ME antenna. (<b>c</b>) Power spectrum of the reflected signal from the ME antenna after demodulation and lowpass filtering. (<b>d</b>) Zoom-in modulation signal at 1 kHz. (<b>e</b>) Modulated voltage as a function of modulated signal magnetic flux density, showing a 470 pT LOD. (<b>f</b>) LOD as a function of modulation signal frequency. (<b>g</b>) Power transfer efficiency as a function of distance between transmission and receiving antennas. Reproduced from Ref. [<a href="#B14-micromachines-15-01471" class="html-bibr">14</a>].</p>
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<p>(<b>a</b>) Schematic of the wideband SAW-based magnetic sensor. The sensor is built on a ST–cut quartz substrate, with SiO<sub>2</sub> guiding layer, and FeCoBSi as a sensing layer. (<b>b</b>) The image shows the frequency vs. amplitude density. The authors report a LOD of 80 pT/Hz<sup>1/2</sup> at 100 Hz, a bandwidth of 50 kHz, and a dynamic range of 120 dB. Reprinted from Ref. [<a href="#B22-micromachines-15-01471" class="html-bibr">22</a>].</p>
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<p>(<b>a</b>) The illustration of a Love-Wave-based magnetic sensor based on a ST–cut quartz substrate. (<b>b</b>) The magnetization loops of different configurations of stacks. Note that the one deposited under the in-situ field has low anisotropy (red) compared to the one with post annealing after film deposition (blue). (<b>c</b>) The measured sensitivity as a function of the applied DC bias field for the configuration deposited with in-situ magnetic field. (<b>d</b>) LOD as a function of frequency for different magnetic orientation configurations. The lowest LOD is from the device with the magnetic stack deposited with an in situ magnetic field. Reprinted with permission from Ref. [<a href="#B23-micromachines-15-01471" class="html-bibr">23</a>]. Copyright 2020 AIP Publishing.</p>
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<p>(<b>a</b>) The SAW sensor design consisting of a ST–cut quartz substrate, a SiO<sub>2</sub> guiding layer and an anti-parallel exchange biased magnetostrictive layer (for sensing). (<b>b</b>) The layer stack of the magnetostrictive layer; it consists of two layers (Ta/FeCoSiB/NiFe/MnIr/Ta) that are antiparallel to each other. The NiFe/MnIr induces the exchange bias in the FeCoSiB layers of. (<b>c</b>) The magneto-optical Kerr effect microscope images from the top on a single FeCoSiB layer and a two-layer anti-parallel exchange bias stack. The image clearly shows the significant reduction in the domain wall density. (<b>d</b>) LOD plotted as a function of excitation power at 10 Hz and 100 Hz. Note that the LOD has the lowest value at 5 dBm for both frequencies. (<b>e</b>) Frequency spectrum of LOD with 5 dBm power. The LOD decreases as frequency increases, and an impressive LOD below 5 pT/Hz<sup>1/2</sup> is achieved at 1 kHz. Reprinted from Ref. [<a href="#B25-micromachines-15-01471" class="html-bibr">25</a>].</p>
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<p>(<b>a</b>) The illustration of the NPR antenna and the measurement setup. The high-frequency magnetic field is generated by the RF coil. On the bottom, a SEM picture of the antenna is shown with different individual layers (AlN, FeGaB, and Au). (<b>b</b>) The admittance curve and the Butterworth–van Dyke mode, and the inset shows the various parameters. (<b>c</b>) Admittance curve of a control device, where the magnetic layer is replaced with Cu. (<b>d</b>) The ME coefficient (right) and ME-induced voltage in the piezoelectric layer as a function of frequency. (<b>e</b>) Analog-induced voltage in the piezoelectric layer of the control device; the inset shows a zoomed-in view of the red circle. (<b>f</b>) The set-up of a FBAR antenna that uses a horn antenna to excite the magnetostrictive layer. At the bottom, a SEM picture of the close-up of the FBAR antenna highlighting the individual layers (AlN, FeGaB, and Au). (<b>g</b>) Return loss curve (S<sub>22</sub>) of the ME FBAR antenna. The inset shows the simulated displacement of the ME FBAR device at resonance. (<b>h</b>) Return loss curve (S<sub>22</sub>) of the control FBAR device when the magnetic layer is replaced with a non-magnetic Al layer. (<b>i</b>) The transmission (S<sub>12</sub>) and receiving (S<sub>21</sub>) behavior of the FBAR antenna. (<b>j</b>) Transmission (S<sub>12</sub>) and receiving (S<sub>21</sub>) curves of the control FBAR device; note the sharp reduction of the peaks compared to the ME FBAR. Reprinted from Ref. [<a href="#B15-micromachines-15-01471" class="html-bibr">15</a>].</p>
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<p>(<b>a</b>) Return loss curve (S<sub>11</sub>) of the ME FBAR antenna with a resonant frequency of 1.95 GHz and an 8.4 MHz bandwidth mounted on different sizes of ground planes (GP1–GP5). (<b>b</b>) Transmission (S<sub>21</sub>) curves of the ME FBAR antennas along with a control device (mounted on top of a 2 cm × 2 cm plastic substrate). Note the 3 dB gain enhancement of the ME FBAR mounted on GP vs. control device. (<b>c</b>) Optical images of four ME FBAR antenna array configurations. (<b>d</b>) Gain enhancement of different antenna configurations, showing a non-linear increase in gain as a function of antenna number. Reprinted from Ref. [<a href="#B19-micromachines-15-01471" class="html-bibr">19</a>].</p>
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<p>(<b>a</b>) Cross-sectional view of the SMR ME antenna showing the different layers. The Bragg reflector (3 × W/SiO<sub>2</sub>), Pt (bottom electrode), ZnO, and FeGaB layers are evident. (<b>b</b>) Optical image of the SMR ME antenna. The GSG pads are used to feed the signal during transmission mode or read out the signal in the receiving mode of the antenna. (<b>c</b>) The power-handling capability of the SMR ME antenna compared to the FBAR ME antenna. The SMR has a 1 dB compression point at 30.4 dBm while the FBAR has it at 7.1 dBm. Reprinted from Ref. [<a href="#B20-micromachines-15-01471" class="html-bibr">20</a>].</p>
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<p>(<b>a</b>) The illustration of the SAW-based ME antenna showing different layer configurations. (<b>b</b>) The optical image of the SAW-based ME antenna. (<b>c</b>,<b>d</b>) Device testing schematic and the associated radiation pattern of the SAW ME antenna. Reprinted with permission from Ref. [<a href="#B261-micromachines-15-01471" class="html-bibr">261</a>]. Copyright 2024 IEEE.</p>
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<p>The VLF ME antenna: (<b>a</b>) A 3D model showing each layer. (<b>b</b>) An optical top view photograph with the antenna’s dimensions. (<b>c</b>) The measured received signal at the resonance frequency along with the noise floor. (<b>d</b>) The measured output voltage as the bias field decreases, showing the limit of detection. (<b>e</b>) Predicted and measured magnetic field distribution as a function of distance. (<b>f</b>) Radiation field and power consumption of the ME transmitter under varying driving voltages. Reprinted with permission from Ref. [<a href="#B263-micromachines-15-01471" class="html-bibr">263</a>]. Copyright 2020 IEEE.</p>
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<p>Experimental results on the giant nonreciprocity effect of hybridized SAW/SW in the FeGaB/Al<sub>2</sub>O<sub>3</sub>/FeGaB multilayer stack on the piezoelectric lithium niobate substrate at the frequency of 1435 MHz when a growth field (<span class="html-italic">H<sub>G</sub></span>) was oriented at 60°. Acoustically Driven Ferromagnetic Resonance (ADFMR) plots were generated for hybridized SAW/SW traveling in the (<b>A</b>) +z direction and (<b>B</b>) −z direction. Resonance absorption, highlighted in blue on the color scale, was observed at the ADFMR frequency in directions orthogonal to the growth field, where strong magneto-acoustic interaction took place. (<b>C</b>) Field sweeps at <span class="html-italic">ϕ</span> = 150° for forward (blue) and reverse (orange) SAW propagation. (<b>D</b>) Field sweeps at <span class="html-italic">ϕ</span> = 330° for forward (blue) and reverse (orange) propagation. The isolation was determined by the difference between forward and reverse sweeps under identical static field conditions. The nonreciprocal power isolation of 48.4 dB was observed. Reprinted with permission from Ref. [<a href="#B294-micromachines-15-01471" class="html-bibr">294</a>]. Copyright 2020 The American Association for the Advancement of Science.</p>
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<p>Wideband and giant nonreciprocity experimentally demonstrated in CoFeB/Ru/CoFeB RKKY stack. (<b>a</b>) Schematics of magnetoacoustic device. (<b>b</b>) SAW and SW dispersive relation near wide-band resonance region. (<b>c</b>) Wideband non-reciprocity from 2 to 7 GHz realized in CoFeB (20 nm)/Ru (0.46 nm)/CoFeB (20 nm) stack. (<b>d</b>) A 250 dB/mm giant non-reciprocity achieved in CoFeB (16 nm)/Ru (0.55 nm)/CoFeB (5 nm) stack. Image (<b>a</b>–<b>c</b>) is reprinted with permission from Ref. [<a href="#B304-micromachines-15-01471" class="html-bibr">304</a>]. Copyright 2024 American Chemical Society; Image (<b>d</b>) is reprinted with permission from Ref. [<a href="#B295-micromachines-15-01471" class="html-bibr">295</a>]. Copyright 2023 American Chemical Society.</p>
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<p>Magnetoelectric control of NV<sup>−</sup> center by CoFeB/PMN-PT BAW resonator. (<b>a</b>,<b>d</b>) Schematic illustration of the quantum spin defects (QSD)-magnon hybrid sample fabricated by dispersing nanodiamonds containing ensembles of NV<sup>−</sup> centers on a thin ferromagnetic film of CoFeB on a 300 μm thick PMN-PT ferroelectric substrate. (<b>b</b>,<b>e</b>) Maps of normalized <span class="html-italic">B</span> as a function of <span class="html-italic">ω</span>−<span class="html-italic">k</span> for both <span class="html-italic">V</span><sub>on</sub> and <span class="html-italic">V</span><sub>off</sub>. The black lines enveloping the colormap are the calculated magnon dispersion lines for bulk modes (<span class="html-italic">k</span>∥M) and surface modes (<span class="html-italic">k</span>⊥M). The dashed colored lines represent the NV<sup>−</sup> ESR lines <span class="html-italic">ω</span><sub>NV</sub>. (<b>c</b>) FMR frequency (<math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>ω</mi> </mrow> <mrow> <mi>m</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msubsup> </mrow> </semantics></math>) (data in black lines) as a function of applied voltage extracted from the experimental results for a fixed external magnetic field <span class="html-italic">H</span><sub>ext</sub> = 57 G along <span class="html-italic">x</span>-axis. The color map represents the calculated values of the magnetic noise spectral density <span class="html-italic">G</span><sub>m</sub>(<span class="html-italic">ω</span>, <span class="html-italic">V</span>) for an effective NV<sup>−</sup> height <span class="html-italic">d</span><sub>NV</sub> = 77 nm. The dashed colored lines represent the maximum spread of the NV<sup>−</sup> ESR lines <span class="html-italic">ω</span><sub>NV</sub>. The inset shows the detailed measurements of the magnetic anisotropy field as a function of applied voltage. (<b>f</b>) Measured relaxation rates Γ<sub>1</sub> as a function of applied voltage for a fixed <span class="html-italic">H</span><sub>ext</sub> = 57 G along the <span class="html-italic">x</span>-axis. The inset shows a schematic illustration of the magnetic anisotropy field for the two different voltages for a fixed <span class="html-italic">H</span><sub>ext</sub>. The dashed line represents the theoretical fit of relaxation rates Γ<sub>1.</sub> These figures are reproduced from Ref. [<a href="#B333-micromachines-15-01471" class="html-bibr">333</a>].</p>
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<p>Energy-efficient and local control of NV<sup>−</sup> centers by SAW-driven magnon resonance. (<b>a</b>) Plot of power absorption as a function of applied magnetic field for a 20 nm nickel ADFMR device at 1429 MHz. The x component of the field is taken to be parallel to the direction of SAW propagation, and the y component is in-plane and perpendicular to the direction of SAW propagation. The color bar indicates absorption in decibels per millimeter. (<b>b</b>) Line-cut along the angle of highest absorption (45°) showing a large field-dependent attenuation at 287, 861, and 229 MHz. The insets show the photograph of IDTs, magnetoelastic film, and clusters of nanodiamonds on the measured device. (<b>c</b>) Change in PL normalized to the DC level for NV<sup>−</sup> centers located off the ferromagnetic pad (red), and NV<sup>−</sup> centers on the pad with zero field (blue) and a high (35.8 mT) applied bias field (green) (<b>d</b>) NV<sup>−</sup> PL change in a 20 nm nickel sample as a function of longitudinal position from the edge of the ferromagnet closest to the excitation IDT at zero applied magnetic field. These figures are reproduced with permission from [<a href="#B334-micromachines-15-01471" class="html-bibr">334</a>]. Copyright 2018 The American Association for the Advancement of Science.</p>
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