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Search Results (3,181)

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17 pages, 6962 KiB  
Article
Magnetic Field Meter Based on CMR-B-Scalar Sensor for Measurement of Microsecond Duration Magnetic Field Pulses
by Pavel Piatrou, Voitech Stankevic, Nerija Zurauskiene, Skirmantas Kersulis, Mindaugas Viliunas, Algirdas Baskys, Martynas Sapurov, Vytautas Bleizgys, Darius Antonovic, Valentina Plausinaitiene, Martynas Skapas, Vilius Vertelis and Borisas Levitas
Sensors 2025, 25(6), 1640; https://doi.org/10.3390/s25061640 - 7 Mar 2025
Viewed by 57
Abstract
This study presents a system for precisely measuring pulsed magnetic fields with high amplitude and microsecond duration with minimal interference. The system comprises a probe with an advanced magnetic field sensor and a measurement unit for signal conversion, analysis, and digitization. The sensor [...] Read more.
This study presents a system for precisely measuring pulsed magnetic fields with high amplitude and microsecond duration with minimal interference. The system comprises a probe with an advanced magnetic field sensor and a measurement unit for signal conversion, analysis, and digitization. The sensor uses a thin nanostructured manganite La-Sr-Mn-O film exhibiting colossal magnetoresistance, which enables precise magnetic field measurement independent of its orientation. Films with different compositions were optimized and tested in pulsed magnetic fields. The measurement unit includes a pulsed voltage generator, an ADC, a microcontroller, and an amplifier unit. Two versions of the measurement unit were developed: one with a separate amplifier unit configured for the sensor positioned more than 1 m away from the measurement unit, and the other with an integrated amplifier for the sensor positioned at a distance of less than 0.5 m. A bipolar pulsed voltage supplying the sensor minimized the parasitic effects of the electromotive force induced in the probe circuit. The data were transmitted via a fiber optic cable to a PC equipped with a special software for processing and recording. Tests with 20–30 μs pulses up to 15 T confirmed the effectiveness of the system for measuring high pulsed magnetic fields. Full article
(This article belongs to the Special Issue Magnetic Field Sensing and Measurement Techniques)
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Figure 1

Figure 1
<p>(<b>a</b>) Resistivity vs. temperature dependences of LSMO films with different Mn contents. <span class="html-italic">MR</span> dependences on magnetic flux density for films with Mn excess <span class="html-italic">y</span> = 1.15 (<b>b</b>) and <span class="html-italic">y</span> = 1.10 (<b>c</b>) contents at various ambient temperatures. Cross-sectional bright-field TEM image of the film with <span class="html-italic">y</span> = 1.10 (<b>d</b>) and <span class="html-italic">y</span> = 1.15 (<b>e</b>).</p>
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<p>Image of the sensors after photolithography (<b>a</b>). Image (<b>b</b>) and cross-sectional drawing (<b>c</b>) of a single sensor.</p>
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<p>(<b>a</b>) Flexible magnetic field probe with length of 25 cm and wire diameter of 1 mm. (<b>b</b>) Rigid magnetic field probe in plastic housing with diameter of 3 mm.</p>
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<p>The block diagram of the first version of the magnetic field meter.</p>
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<p>Circuit diagrams of the sensor’s signal amplifier and interference protection circuit of the first version meter. The resistors with the asterisk (∗) are chosen depending on the sensor resistance. The amplifier and protection circuit are located in a separate unit (see <a href="#sensors-25-01640-f004" class="html-fig">Figure 4</a>).</p>
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<p>Circuit diagrams of interference protection circuit and bipolar pulsed voltage supply source of the first version of the meter. The bipolar pulse generator and input protection circuit are located in the measurement unit (see <a href="#sensors-25-01640-f004" class="html-fig">Figure 4</a>).</p>
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<p>The first version of the magnetic field meter.</p>
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<p>The block diagram of the second version of the pulsed magnetic field meter.</p>
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<p>Circuit diagrams of interference protection circuit, bipolar pulsed voltage supply source, and sensor signal amplifier of the second version of the meter. The resistors with the asterisk (∗) are chosen depending on the sensor resistance. The input protection circuit, signal amplifier, and bipolar pulse generator are located in the measurement unit (see <a href="#sensors-25-01640-f008" class="html-fig">Figure 8</a>).</p>
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<p>Second version of the measurement unit of the magnetic field meter: (<b>a</b>) front side; (<b>b</b>) rear side.</p>
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<p>Magnetic field meter and picture of main window of a personal computer interface.</p>
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<p>Transients of bipolar pulsed supply voltage across the sensor for the first (<b>a</b>,<b>c</b>) and second (<b>b</b>,<b>d</b>) versions of magnetic field meter at various pulsed voltage frequencies.</p>
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<p>(<b>a</b>) Circuit diagram of microsecond magnetic pulse generator which consists of a capacitor bank, a Bitter coil, and a spark gap. (<b>b</b>) General view of the experimental setup for testing the magnetic field meter (second version).</p>
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<p>Transients of sensor signal using first (<b>a</b>) and second (<b>b</b>) versions of magnetic field meter, when sensors are placed in a Bitter coil and magnetic pulse generator capacitors are discharged through it when the capacitors’ voltage is 12.5 kV. (<b>c</b>) Transients of sensor signal are detected when useful signal, and EMF is also detected. (<b>d</b>) Magnetic flux density in the Bitter coil as a function of time, measured with the second version of the magnetic field meter when the capacitors were charged to 12.5 kV.</p>
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17 pages, 1705 KiB  
Article
Exploring Positional Performance and Force Control in a Bimanual Lifting Task Among Children with Neurodevelopmental Disabilities: A Cross-Sectional Study
by Haowei Guo, Caroline H. G. Bastiaenen, Jeanine A. M. C. F. Verbunt and Eugene A. A. Rameckers
Appl. Sci. 2025, 15(6), 2872; https://doi.org/10.3390/app15062872 - 7 Mar 2025
Viewed by 178
Abstract
Children with neurodevelopmental disabilities often struggle with motor control and stability, impacting their ability to perform functional tasks such as lifting and carrying objects. This study explores positional performance during bimanual box-lifting tasks in children aged 9–18 years with neurodevelopmental disabilities. A total [...] Read more.
Children with neurodevelopmental disabilities often struggle with motor control and stability, impacting their ability to perform functional tasks such as lifting and carrying objects. This study explores positional performance during bimanual box-lifting tasks in children aged 9–18 years with neurodevelopmental disabilities. A total of 83 participants, including 62 with unilateral spastic cerebral palsy and 21 with non-unilateral spastic cerebral palsy, performed tasks using the Activity of Daily Living Testing and Training Device. Tasks were conducted at maximal (80–100% force) and submaximal (40–80% force) levels of force control, with positional performance measured in six directions using Inertial Measurement Unit sensors. Statistical analyses included the Wilcoxon signed-rank test for levels of force control comparisons, Kruskal–Wallis tests for group differences, and Spearman correlations to assess relationships between maximal and submaximal performance. The results revealed that four of six positional parameters were worse in the maximal zone than in the submaximal zone (p<0.05), highlighting the challenges of higher force demands. Additionally, positive correlations between maximal and submaximal performance suggest consistency across levels of force control. Maximal levels of force control increased variability, with submaximal performance proven to be a reliable predictor of maximal capabilities. This finding offers a safer and more efficient method for assessing motor performance. Overall, these results underscore the importance of targeted rehabilitation strategies focused on improving stability and precision in children with neurodevelopmental disabilities so they can perform daily tasks more independently. Full article
(This article belongs to the Special Issue Advanced Physical Therapy for Rehabilitation)
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<p>The parts of an ADL-TTD.</p>
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<p>Six directions of tilt across the x-, y-, and z axes for the box. (In this figure, the right hand is the AH.)</p>
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<p>Measurement position when using ADL-TTD.</p>
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<p>Box specification and simulated water fill levels.</p>
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<p>Water spilling angles with different tilt directions. Note: The calculation was not made for the AH/NAH forward rotation because movement in the horizontal plane is not very relevant as parameter causing spilling.</p>
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<p>Scatter plot for individual subjects in all directions in the Max and SubMax zones. Note: Red dash lines mean different water levels below the top of the box.</p>
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<p>Scatter plot of all the position variables between the Max and SubMax zones.</p>
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30 pages, 14392 KiB  
Article
High-Quality Perovskite Thin Films for NO2 Detection: Optimizing Pulsed Laser Deposition of Pure and Sr-Doped LaMO3 (M = Co, Fe)
by Lukasz Cieniek, Agnieszka Kopia, Kazimierz Kowalski and Tomasz Moskalewicz
Materials 2025, 18(5), 1175; https://doi.org/10.3390/ma18051175 - 6 Mar 2025
Viewed by 87
Abstract
This study investigates the structural and catalytic properties of pure and Sr-doped LaCoO3 and LaFeO3 thin films for potential use as resistive gas sensors. Thin films were deposited via pulsed laser deposition (PLD) and characterized using X-ray diffraction (XRD), X-ray photoelectron [...] Read more.
This study investigates the structural and catalytic properties of pure and Sr-doped LaCoO3 and LaFeO3 thin films for potential use as resistive gas sensors. Thin films were deposited via pulsed laser deposition (PLD) and characterized using X-ray diffraction (XRD), X-ray photoelectron spectroscopy (XPS), scanning electron microscopy (SEM), atomic force microscopy (AFM), nanoindentation, and scratch tests. XRD analysis confirmed the formation of the desired perovskite phases without secondary phases. XPS revealed the presence of La3+, Co3+/Co4+, Fe3+/Fe4+, and Sr2+ oxidation states. SEM and AFM imaging showed compact, nanostructured surfaces with varying morphologies (shape and size of surface irregularities) depending on the composition. Sr doping led to surface refinement and increased nanohardness and adhesion. Transmission electron microscopy (TEM) analysis confirmed the columnar growth of nanocrystalline films. Sr-doped LaCoO3 demonstrated enhanced sensitivity and stability in the presence of NO2 gas compared to pure LaCoO3, as evidenced by electrical resistivity measurements within 230 ÷ 440 °C. At the same time, it was found that Sr doping stabilizes the catalytic activity of LaFeO3 (in the range of 300 ÷ 350 °C), although its behavior in the presence of NO2 differs from that of LaCo(Sr)O3—especially in terms of response and recovery times. These findings highlight the potential of Sr-doped LaCoO3 and LaFeO3 thin films for NO2 sensing applications. Full article
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<p>A representative example of the ABX<sub>3</sub> perovskite structure (<b>a</b>), along with its characteristic symmetry (<b>b</b>). The structural transformation scheme for LaMO<sub>3</sub> (M = Co, Fe) as a function of temperature is illustrated in (<b>c</b>). This transformation often leads to the formation of twin domains within the material, as depicted in (<b>d</b>).</p>
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<p>SEM images illustrating the surface topography of the targets used in the study; (<b>a</b>) LaCoO<sub>3</sub>, (<b>b</b>) La(Sr)CoO<sub>3</sub>, (<b>c</b>) LaFeO<sub>3</sub>, (<b>d</b>) La(Sr)FeO<sub>3</sub>; and (<b>e</b>) macro image of targets ready for microscopic examination and (<b>f</b>) the surface of the LaFeO<sub>3</sub> target after laser ablation.</p>
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<p>Laser ablation system (PLD) built with an Nd:YAG laser and the Neocera vacuum chamber, connected by an optical system (<b>a</b>). Schematic of the PLD process (<b>b</b>) and a view inside the process chamber (<b>c</b>).</p>
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<p>XRD phase analysis of (<b>a</b>) Sr-doped LaCoO<sub>3</sub> and (<b>b</b>) Sr-doped LaFeO<sub>3</sub> thin films, with JCPDS pattern cards and average crystallite sizes (estimated using the Williamson–Hall method).</p>
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<p>XPS detection/verification of chemical states of elements for La(Sr)CoO<sub>3</sub> thin films.</p>
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<p>XPS detection/verification of chemical states of elements for La(Sr)FeO<sub>3</sub> thin films.</p>
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<p>SEM images of the topography of perovskite thin films grown on monocrystalline Si substrates [001] with the result of EDS analysis of the chemical composition for (<b>a</b>) LaCoO<sub>3</sub> and (<b>b</b>) LaFeO<sub>3</sub>.</p>
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<p>SEM images of the topography of perovskite thin films grown on monocrystalline Si substrates [001] with the result of EDS analysis of the chemical composition for (<b>a</b>) Sr-doped LaCoO<sub>3</sub>, (<b>b</b>) Sr-doped LaFeO<sub>3</sub>.</p>
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<p>Surface topography images of perovskite thin films by atomic force microscopy (AFM) technique for (<b>a</b>) LaCoO<sub>3</sub> and (<b>b</b>) LaFeO<sub>3</sub>.</p>
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<p>Surface topography images of perovskite thin films by atomic force microscopy (AFM) technique for (<b>a</b>) Sr-doped LaCoO<sub>3</sub> and (<b>b</b>) Sr-doped LaFeO<sub>3</sub>.</p>
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<p>Examples of (<b>a</b>) indentation curve and (<b>b</b>) penetration depth and normal force plots obtained from nanohardness measurements of LaFeO<sub>3</sub> thin film on Si substrate.</p>
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<p>TEM analysis of LaCoO<sub>3</sub> thin films: (<b>a</b>) low-magnification bright-field image with selected area electron diffraction pattern, (<b>b</b>,<b>c</b>) high-resolution TEM images, and (<b>d</b>) SAED solved with TEM/EDS analysis.</p>
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<p>TEM analysis of Sr-doped LaCoO<sub>3</sub> thin films: (<b>a</b>,<b>b</b>,<b>d</b>,<b>e</b>) low-magnification bright- and (<b>c</b>,<b>f</b>) dark-field image with selected area electron diffraction patterns, and (<b>g</b>) SAED solved with TEM/EDS analysis.</p>
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<p>TEM analysis of LaFeO<sub>3</sub> thin films: (<b>a</b>,<b>b</b>) low-magnification bright- and (<b>c</b>) dark-field image with selected area electron diffraction pattern, (<b>d</b>,<b>e</b>) high-resolution TEM images, and (<b>f</b>) SAED solved with TEM/EDS analysis.</p>
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<p>TEM analysis of Sr-doped LaFeO<sub>3</sub> thin films: (<b>a</b>,<b>d</b>) low-magnification bright- and (<b>b</b>,<b>e</b>) dark-field image with selected area electron diffraction patterns, (<b>c</b>,<b>f</b>) high-resolution TEM images and (<b>g</b>) SAED pattern solved with TEM/EDS analysis.</p>
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<p>LaCoO<sub>3</sub> response at 500 °C exposed to 50 ppm of NO<sub>2</sub> using different currents: (<b>a</b>) 0.1 nA, (<b>b</b>) 1 nA, and (<b>c</b>) 10nA.</p>
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<p>Response of La(Sr)CoO<sub>3</sub> exposed to 50 ppm NO<sub>2</sub> at temperatures in the range of 230 ÷ 440 °C: (<b>a</b>) LaCoO<sub>3</sub>, (<b>b</b>) La<sub>0.9</sub>Sr<sub>0.1</sub>CoO<sub>3</sub>, and (<b>c</b>) La<sub>0</sub>.<sub>9</sub>Sr<sub>0.1</sub>CoO<sub>3</sub>.</p>
Full article ">Figure 17 Cont.
<p>Response of La(Sr)CoO<sub>3</sub> exposed to 50 ppm NO<sub>2</sub> at temperatures in the range of 230 ÷ 440 °C: (<b>a</b>) LaCoO<sub>3</sub>, (<b>b</b>) La<sub>0.9</sub>Sr<sub>0.1</sub>CoO<sub>3</sub>, and (<b>c</b>) La<sub>0</sub>.<sub>9</sub>Sr<sub>0.1</sub>CoO<sub>3</sub>.</p>
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<p>Response of LaFeO<sub>3</sub> exposed to 50 ppm NO<sub>2</sub> for a range of temperatures: (<b>a</b>) 230 °C, (<b>b</b>) 300 °C, (<b>c</b>) 350 °C, (<b>d</b>) 400 °C, and (<b>e</b>) 440 °C.</p>
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<p>Response of La<sub>0</sub>.<sub>9</sub>Sr<sub>0</sub>.<sub>1</sub>FeO<sub>3</sub> exposed to 50 ppm NO<sub>2</sub> (summary chart) and for a range of temperatures: (<b>a</b>) 230 °C, (<b>b</b>) 300 °C, (<b>c</b>) 350 °C, and (<b>d</b>) 440 °C.</p>
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<p>Response of La<sub>0</sub>.<sub>8</sub>Sr<sub>0</sub>.<sub>2</sub>FeO<sub>3</sub> exposed to 50 ppm NO<sub>2</sub> (summary chart) and for a range of temperatures: (<b>a</b>) 230 °C, (<b>b</b>) 300 °C, (<b>c</b>) 350 °C, and (<b>d</b>) 440 °C.</p>
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20 pages, 11640 KiB  
Article
The Influence of Sample Microfabrication and Annealing on the Mechanical Strain–Stress Behavior of Stainless Steels and Corrosion Resistant Aluminum Alloys in Micro-Tensile Tests
by Janko Auerswald, Joel Tenisch, Christoph Fallegger and Markus Seifert
Micromachines 2025, 16(3), 309; https://doi.org/10.3390/mi16030309 - 6 Mar 2025
Viewed by 85
Abstract
Miniaturized components for enhanced integrated functionality or thin sheets for lightweight applications often consist of face-centered cubic metals. They exhibit good strength, corrosion resistance, formability and recyclability. Microfabrication technologies, however, may introduce cold work or detrimental heat-induced lattice defects into the material, with [...] Read more.
Miniaturized components for enhanced integrated functionality or thin sheets for lightweight applications often consist of face-centered cubic metals. They exhibit good strength, corrosion resistance, formability and recyclability. Microfabrication technologies, however, may introduce cold work or detrimental heat-induced lattice defects into the material, with consequences for the mechanical properties. Austenitic stainless steels (1.4310, 1.4301) and aluminum alloys (EN AW-5005-H24, EN AW-6082-T6) were selected for this study. The influence of pulsed fiber laser cutting, microwaterjet cutting, and annealing on the strain–stress behavior was investigated. The micro-tensile test setup comprised a flex-structure force sensor, a laser extensometer, and a dedicated sample holder. Fiber laser cut 1.4310 samples exhibited early failure at low fracture strain in narrow shear band zones. The shear band zones were detectable on the sample surface, in the laser extensometer images, in the horizontal sections of the stress–strain curves, and in the microstructure. Inside the shear band zones, grains were strongly elongated and exhibited numerous parallel planar defects. Heat-induced chromium carbides, in combination with low stacking fault energy (SFE) and elevated carbon content, favored shear band zone formation in 1.4310. In contrast, microwaterjet cut high SFE materials EN AW-5005-H24 and EN AW-6082-T6, as well as low-carbon austenitic stainless steel 1.4301, exhibited uniform plastic deformation. Full article
(This article belongs to the Section D:Materials and Processing)
Show Figures

Figure 1

Figure 1
<p>(<b>a</b>) An example of a micromechanical spring component made of 1.4310. (<b>b</b>) The micro-tensile test setup. (<b>c</b>) A typical micro-tensile test sample (here, stainless steel 1.4310, 100 μm thick).</p>
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<p>(<b>a</b>) The schematic design of the micro-tensile test sample geometry. (<b>b</b>) Mounted, polished, and etched 1.4310 sample after failure in micro-tensile test with 1—fracture zone, 2—deformation zone (large amount of plastic deformation) and 3—clamping area (larger width, little plastic deformation).</p>
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<p>Micro-tensile tests of 100 μm thin 1.4310 steel. All laser cut samples failed due to the pronounced shear band zone formation at a low fracture strain, as shown in (<b>a</b>–<b>c</b>). The samples cut by the microwaterjet process exhibited local shear band zone formation only at the beginning of the plastic deformation (horizontal stress plateau), which evolved into a more homogeneous strain distribution over the entire measurement length and work hardening before the final fracture (<b>d</b>).</p>
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<p>(<b>a</b>) Microstructure of the laser cut 1.4310 sample with polygonal, non-elongated grains, not deformed in a micro-tensile test. (<b>b</b>) Fracture zone of the laser cut 1.4310 sample with characteristic ductile fracture dimples after fracture in a micro-tensile test inside a shear band zone. (<b>c</b>) Microstructure of a microwaterjet cut 1.4310 sample with polygonal, non-elongated grains, not deformed in a micro-tensile test. (<b>d</b>) Fracture zone of a microwaterjet cut 1.4310 sample with characteristic ductile fracture dimples, after the fracture in a micro-tensile test.</p>
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<p>Microstructure of 1.4310 inside shear band zone. (<b>a</b>) Overview, grains strongly elongated by plastic deformation. (<b>b</b>) Detail with overlapping parallel planar defects in elongated grains.</p>
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<p>Microstructure of 1.4310 outside shear band zone; (<b>a</b>) overview and (<b>b</b>) in more detail.</p>
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<p>(<b>a</b>) Fracture strain A<sub>10mm</sub>, as well as (<b>b</b>) 0.2% yield strength R<sub>p0.2</sub> (proof stress) and tensile strength R<sub>m</sub> of 100 μm thin 1.4310 micro-tensile test samples microfabricated by pulsed fiber laser cutting and by cold microwaterjet cutting.</p>
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<p>Comparison of the microstructure of the 1.4310 samples in the deformation zone (not in the shear band zones). Samples were cut with (<b>a</b>) hot, (<b>b</b>) medium, and (<b>c</b>) mild laser parameters, and with (<b>d</b>) microwaterjet. The laser cut samples (<b>a</b>–<b>c</b>) exhibited pronounced chromium carbide formation at the grain boundaries.</p>
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<p>Strain–stress behavior and representative shear fracture images of 1.4310 micro-tensile test samples cut with microwaterjet and annealed at 100 °C (<b>a</b>), 200 °C (<b>b</b>), 400 °C (<b>c</b>) and 600 °C (<b>d</b>) for one hour, respectively.</p>
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<p>Deformation zone of 1.4310 samples cut by microwaterjet and annealed (<b>a</b>) at 600 °C, (<b>b</b>) at 400 °C, (<b>c</b>) at 200 °C, and (<b>d</b>) at 100 °C for 1 h, respectively.</p>
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<p>(<b>a</b>) Young’s modulus E, (<b>b</b>) 0.2% yield strength R<sub>p0.2</sub> (proof stress), (<b>c</b>) tensile strength R<sub>m</sub>, and (<b>d</b>) fracture strain A<sub>10mm</sub> of 100 μm thin 1.4310 micro-tensile test samples, produced by microwaterjet cutting, without and with annealing heat treatment.</p>
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<p>Micro-tensile tests curves of microwaterjet cut 1.4301 samples. No horizontal stress plateaus at beginning of plastic deformation. (<b>a</b>) No annealing. (<b>b</b>) After annealing at 600 °C for 1 h.</p>
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<p>Microwaterjet cut 1.4301 samples (2.5 mm in width, 100 μm in thickness) of different annealing conditions, after failure in micro-tensile tests. All 1.4301 samples failed due to ductile fractures. Necking occurred mainly in the form of specimen thickness reduction at the fracture site.</p>
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<p>(<b>a</b>) Young’s modulus E, (<b>b</b>) 0.2% yield strength R<sub>p0.2</sub> (proof stress), (<b>c</b>) tensile strength R<sub>m</sub>, and (<b>d</b>) fracture strain A<sub>10mm</sub> of 100 μm thin 1.4301 micro-tensile test samples, produced by microwaterjet cutting, without and with annealing heat treatment.</p>
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<p>Micro-tensile test stress–strain curves of microwaterjet cut EN AW-5005-H24 samples. (<b>a</b>) No heat treatment; elevated R<sub>p0.2</sub> due to significant work hardening effect after cold rolling. (<b>b</b>) After annealing at 400 °C for 1 h; low R<sub>p0.2</sub> with subsequent work hardening.</p>
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<p>Microwaterjet cut EN AW-5005-H24 samples (3 mm in width, 500 μm in thickness) of different annealing conditions, after failure in micro-tensile tests. All samples failed by ductile fracture. Necking occurred in the form of pronounced thickness and width reduction at the fracture site.</p>
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<p>Mechanical properties of 500 μm thin microwaterjet cut EN AW-5005-H24 samples, without and with annealing (<b>a</b>–<b>d</b>). The decrease in 0.2% yield strength and tensile strength, and the increase in fracture strain after annealing at 400 °C were due to the removal of work hardening. The H24 partial annealing temperature of 260 °C is marked by the dashed red line in graphs (<b>b</b>–<b>d</b>).</p>
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<p>(<b>a</b>) Strain–stress behavior of the high-strength aluminum alloy EN AW-6082-T6, precipitation-hardened (artificial aging) and cut by microwaterjet. (<b>b</b>) The sample (3 mm in width, 1 mm in thickness) after a ductile failure in micro-tensile test.</p>
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21 pages, 6656 KiB  
Article
A Flexible PVDF Sensor for Forcecardiography
by Salvatore Parlato, Jessica Centracchio, Eliana Cinotti, Gaetano D. Gargiulo, Daniele Esposito, Paolo Bifulco and Emilio Andreozzi
Sensors 2025, 25(5), 1608; https://doi.org/10.3390/s25051608 - 6 Mar 2025
Viewed by 160
Abstract
Forcecardiography (FCG) uses force sensors to record the mechanical vibrations induced on the chest wall by cardiac and respiratory activities. FCG is usually performed via piezoelectric lead-zirconate titanate (PZT) sensors, which simultaneously record the very slow respiratory movements of the chest, the slow [...] Read more.
Forcecardiography (FCG) uses force sensors to record the mechanical vibrations induced on the chest wall by cardiac and respiratory activities. FCG is usually performed via piezoelectric lead-zirconate titanate (PZT) sensors, which simultaneously record the very slow respiratory movements of the chest, the slow infrasonic vibrations due to emptying and filling of heart chambers, the faster infrasonic vibrations due to movements of heart valves, which are usually recorded via Seismocardiography (SCG), and the audible vibrations corresponding to heart sounds, commonly recorded via Phonocardiography (PCG). However, PZT sensors are not flexible and do not adapt very well to the deformations of soft tissues on the chest. This study presents a flexible FCG sensor based on a piezoelectric polyvinylidene fluoride (PVDF) transducer. The PVDF FCG sensor was compared with a well-assessed PZT FCG sensor, as well as with an electro-resistive respiratory band (ERB), an accelerometric SCG sensor, and an electronic stethoscope for PCG. Simultaneous recordings were acquired with these sensors and an electrocardiography (ECG) monitor from a cohort of 35 healthy subjects (16 males and 19 females). The PVDF sensor signals were compared in terms of morphology with those acquired simultaneously via the PZT sensor, the SCG sensor and the electronic stethoscope. Moreover, the estimation accuracies of PVDF and PZT sensors for inter-beat intervals (IBIs) and inter-breath intervals (IBrIs) were assessed against reference ECG and ERB measurements. The results of statistical analyses confirmed that the PVDF sensor provides FCG signals with very high similarity to those acquired via PZT sensors (median cross-correlation index of 0.96 across all subjects) as well as with SCG and PCG signals (median cross-correlation indices of 0.85 and 0.80, respectively). Moreover, the PVDF sensor provides very accurate estimates of IBIs, with R2 > 0.99 and Bland–Altman limits of agreement (LoA) of [−5.30; 5.00] ms, and of IBrIs, with R2 > 0.96 and LoA of [−0.510; 0.513] s. The flexibility of the PVDF sensor makes it more comfortable and ideal for wearable applications. Unlike PZT, PVDF is lead-free, which increases safety and biocompatibility for prolonged skin contact. Full article
(This article belongs to the Special Issue Sensors for Heart Rate Monitoring and Cardiovascular Disease)
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<p>A 3D rendering of the flexible PVDF FCG sensor.</p>
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<p>(<b>a</b>) Actual view of the sensors assembly; (<b>b</b>) 3D rendering of sensors assembly with an exploded view of its components and a typical placement onto a subject’s chest.</p>
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<p>An example of a subject equipped with the measurement setup.</p>
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<p>Excerpt of FCG sensors signals acquired from subject #3, displayed together with the reference ECG signal. Raw signals from PZT sensor and PVDF sensor were depicted with blue and red lines, respectively. Black dots mark the R-peaks detected on the ECG signal.</p>
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<p>Excerpt of cardiac components extracted from FCG signals, with FRG, and ECG signals from subject #3: (<b>a</b>) PZT sensor signals; (<b>b</b>) PVDF sensor signals.</p>
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<p>Excerpt of cardiac components extracted from FCG signals, with FRG, and ECG signals from subject #3: (<b>a</b>) PZT sensor signals; (<b>b</b>) PVDF sensor signals.</p>
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<p>Heartbeats detection on dHF-FCG and HS-FCG, compared with the reference ECG signal: (<b>a</b>) heartbeats localization on dHF-FCG from subject #3; (<b>b</b>) heartbeats localization on HS-FCG from subject #32.</p>
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<p>Comparison between the FRG extracted from the PVDF sensor signal from subject #3 and the reference ERB signal. The respiratory acts are marked with black dots.</p>
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<p>Illustration of the ECG-triggered ensemble averages (computed on approximately 230 heartbeats) of the raw FCG signals provided by the two sensors, along with ECG ensemble averages and limits of the ±SD. The ensemble averages are depicted with solid lines, while the limits of ±SD are depicted with dotted lines and normalized to the maximum of the ensemble average.</p>
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<p>Excerpts of ECG, SCG, PCG, and FCG signals acquired simultaneously from two subjects involved in the experiment: (<b>a</b>) ECG, SCG, PCG, dHF-FCG, and HS-FCG of subject #3; (<b>b</b>) ECG, SCG, PCG, dHF-FCG, and HS-FCG of subject #32.</p>
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<p>Comparison of aligned ECG-triggered ensemble averages of SCG (orange line) and dHF-FCG (dark blue line) signals, along with the ensemble average of the ECG (green line): (<b>a</b>) aligned ensemble averages of SCG and dHF-FCG signals from subject #3; (<b>b</b>) aligned ensemble averages of SCG and dHF-FCG signals from subject #32.</p>
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<p>Comparison of aligned ECG-triggered ensemble averages of PCG (black line) and HS-FCG (red line) signals, along with the ensemble average of the ECG (green line): (<b>a</b>) aligned ensemble averages of PCG and HS-FCG signals from subject #3; (<b>b</b>) aligned ensemble averages of PCG and HS-FCG signals from subject #32.</p>
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<p>Statistical analyses on the inter-beat intervals (IBIs) obtained from dHF-FCG, HS-FCG (extracted from the PVDF sensor signal), and reference ECG signals: (<b>a</b>) results of regression and correlation analysis achieved from dHF-FCG signal; (<b>b</b>) results of Bland–Altman analysis achieved from dHF-FCG signal; (<b>c</b>) results of regression and correlation analysis achieved from HS-FCG signal; (<b>d</b>) results of Bland–Altman analysis achieved from HS-FCG signal.</p>
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<p>Statistical analyses on the inter-beat intervals (IBIs) obtained from dHF-FCG, HS-FCG (extracted from the PZT sensor signal) and reference ECG signals: (<b>a</b>) results of regression and correlation analysis achieved from dHF-FCG signal; (<b>b</b>) results of Bland–Altman analysis achieved from dHF-FCG signal; (<b>c</b>) results of regression and correlation analysis achieved from HS-FCG signal; (<b>d</b>) results of Bland–Altman analysis achieved from HS-FCG signal.</p>
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<p>Statistical analyses on the inter-breath intervals (IBrIs) obtained from ERB and FRG signal provided by PVDF sensor signals: (<b>a</b>) results of regression and correlation analyses; (<b>b</b>) results of Bland–Altman analysis.</p>
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<p>Statistical analyses on the inter-breath intervals (IBrIs) obtained from ERB and FRG signal provided by PZT sensor signals: (<b>a</b>) results of regression and correlation analyses; (<b>b</b>) results of Bland–Altman analysis.</p>
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13 pages, 5387 KiB  
Article
Thrust Measurement of an Integrated Multi-Sensor Micro-Newton Cold Gas Thruster
by Songcai Lu, Yong Gao, Haibo Tu, Xudong Wang, Xinju Fu, Gang Meng, Jun Long, Xuhui Liu and Yong Li
Aerospace 2025, 12(3), 210; https://doi.org/10.3390/aerospace12030210 - 6 Mar 2025
Viewed by 71
Abstract
In recent years, cold gas thrusters have been successfully deployed in numerous missions, showcasing their exceptional reliability and enabling ultra-precise space operations across a broad thrust range. This article introduces an integrated cold gas thruster that integrates flow, pressure, and displacement sensors. The [...] Read more.
In recent years, cold gas thrusters have been successfully deployed in numerous missions, showcasing their exceptional reliability and enabling ultra-precise space operations across a broad thrust range. This article introduces an integrated cold gas thruster that integrates flow, pressure, and displacement sensors. The thrust range of this thruster can exceed 1000 μN at most, and the resolution can reach up to 0.1 μN at low thrust. The results of the high-precision displacement sensor are good, showing that the thruster performs well in terms of flow control accuracy and thrust output sensitivity. The measurement accuracy of the force frame itself is also excellent, and it can detect small thrust changes of 0.1 μN. The thrust noise level of the thruster is good, comparable to the standard noise levels of the experimental environment. Full article
(This article belongs to the Section Aeronautics)
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<p>Diagram of needle valve nozzle and nozzle throat.</p>
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<p>Structural diagram (<b>a</b>) and photograph (<b>b</b>) of thruster.</p>
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<p>Schematic diagram of the control algorithm principle.</p>
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<p>Thrust test bench principle (<b>a</b>) and installation diagram (<b>b</b>).</p>
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<p>Schematic diagram of gravity calibration principle.</p>
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<p>Bench calibration curve.</p>
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<p>High-thrust test (1200 μN), corresponding to flow of 2200 μg/s.</p>
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<p>Thrust–flow comparison chart in the flow range of 150 μg/s to 550 μg/s.</p>
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<p>Experimental results and linear fitting diagram of thrust and flow rate.</p>
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<p>Experimental results and linear fitting diagram of thrust and displacement.</p>
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<p>Flow rate step change diagram (flow rate started at 2ug/s and changed by 0.2 μg/s/step and 0.3 μg/s/step).</p>
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<p>Thrust noise power spectrum density under different conditions.</p>
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23 pages, 9777 KiB  
Article
Integrated Lower Limb Robotic Orthosis with Embedded Highly Oriented Electrospinning Sensors by Fuzzy Logic-Based Gait Phase Detection and Motion Control
by Ming-Chan Lee, Cheng-Tang Pan, Jhih-Syuan Huang, Zheng-Yu Hoe and Yeong-Maw Hwang
Sensors 2025, 25(5), 1606; https://doi.org/10.3390/s25051606 - 5 Mar 2025
Viewed by 212
Abstract
This study introduces an integrated lower limb robotic orthosis with near-field electrospinning (NFES) piezoelectric sensors and a fuzzy logic-based gait phase detection system to enhance mobility assistance and rehabilitation. The exoskeleton incorporates embedded pressure sensors within the insoles to capture ground reaction forces [...] Read more.
This study introduces an integrated lower limb robotic orthosis with near-field electrospinning (NFES) piezoelectric sensors and a fuzzy logic-based gait phase detection system to enhance mobility assistance and rehabilitation. The exoskeleton incorporates embedded pressure sensors within the insoles to capture ground reaction forces (GRFs) in real-time. A fuzzy logic inference system processes these signals, classifying gait phases such as stance, initial contact, mid-stance, and pre-swing. The NFES technique enables the fabrication of highly oriented nanofibers, improving sensor sensitivity and reliability. The system employs a master–slave control framework. A Texas Instruments (TI) TMS320F28069 microcontroller (Texas Instruments, Dallas, TX, USA) processes gait data and transmits actuation commands to motors and harmonic drives at the hip and knee joints. The control strategy follows a three-loop methodology, ensuring stable operation. Experimental validation assesses the system’s accuracy under various conditions, including no-load and loaded scenarios. Results demonstrate that the exoskeleton accurately detects gait phases, achieving a maximum tracking error of 4.23% in an 8-s gait cycle under no-load conditions and 4.34% when tested with a 68 kg user. Faster motion cycles introduce a maximum error of 6.79% for a 3-s gait cycle, confirming the system’s adaptability to dynamic walking conditions. These findings highlight the effectiveness of the developed exoskeleton in interpreting human motion intentions, positioning it as a promising solution for wearable rehabilitation and mobility assistance. Full article
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<p>The experimental process of this integrated system in this study.</p>
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<p>Rotation angles and DOFs of the robotic orthosis. (<b>a</b>) Range of motion of the hip (<b>b</b>) Range of motion of the knee.</p>
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<p>Gaits of the hip and knee.</p>
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<p>Tests of the possible stress points of the feet.</p>
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<p>Stress points of the feet.</p>
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<p>Schematic of NFES.</p>
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<p>Positions of the sensors on the insole.</p>
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<p>Fuzzy logic structure.</p>
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<p>The fuzzy membership functions of ground reaction forces.</p>
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<p>The fuzzy membership functions of gait phases.</p>
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<p>The schematic diagram of the area of fuzzy sets.</p>
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<p>Flowchart of the gait phase detection.</p>
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<p>The schematic diagram of the designed three-loop control.</p>
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<p>The signals of the piezoresistive sensors.</p>
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<p>PVDF-based NFES sensors work with gait phase detection.</p>
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<p>The total system communication and computation time is approximately 5.09 ms.</p>
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<p>Comparison of fuzzy logic gait detection and traditional gait detection.</p>
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<p>CNC machining.</p>
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<p>Assembled orthosis.</p>
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<p>Results of 8-s walking cycle. (<b>a</b>) Tracking results of the hip (<b>b</b>) Tracking results of the knee.</p>
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<p>Comparison of the maximum error and RMSE.</p>
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<p>The action decomposition diagram of the robotic orthosis operation.</p>
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<p>Results of the first experiment. (<b>a</b>) Tracking results of the hip (<b>b</b>) Tracking results of the knee.</p>
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<p>Results of the first experiment. (<b>a</b>) Tracking results of the hip (<b>b</b>) Tracking results of the knee.</p>
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<p>Results of the second experiment. (<b>a</b>) Tracking results of the hip (<b>b</b>) Tracking results of the knee.</p>
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<p>Results of the second experiment. (<b>a</b>) Tracking results of the hip (<b>b</b>) Tracking results of the knee.</p>
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17 pages, 12958 KiB  
Article
Investigation of the Mechanical and Magnetic Property Changes in Austenitic Stainless Steel AISI 304 After Cold Rolling Under Various Heat Treatment Conditions
by Milan Smetana, Daniela Gombarska, Martin Slezak, Ladislav Janousek and Peter Palcek
Appl. Sci. 2025, 15(5), 2810; https://doi.org/10.3390/app15052810 - 5 Mar 2025
Viewed by 199
Abstract
This study systematically investigates the influence of heat treatment on the mechanical and magnetic properties of AISI 304 austenitic stainless steel following cold rolling. Experimental analyses were conducted on samples annealed at 50 °C to 1200 °C in 25 °C increments. The mechanical [...] Read more.
This study systematically investigates the influence of heat treatment on the mechanical and magnetic properties of AISI 304 austenitic stainless steel following cold rolling. Experimental analyses were conducted on samples annealed at 50 °C to 1200 °C in 25 °C increments. The mechanical properties were characterized through chemical and metallographic analyses, microhardness testing, hardness measurements, and tear-off force evaluations. Magnetic properties were assessed using a fluxgate sensor to analyze the intrinsic magnetic field variations. The findings reveal that the magnetic field intensity peaks at an annealing temperature of 100 °C, followed by a progressive decline up to 700 °C. A pronounced reduction in magnetic properties was observed at 500 °C, with stabilization beyond 700 °C. Notably, the increase in magnetic field intensity at 100 °C suggests a potential transformation of deformation-induced martensite back into austenite. These results provide insights into the thermal stability of cold-rolled AISI 304 stainless steel and its structural evolution, contributing to a deeper understanding of its mechanical and magnetic behavior under varying heat treatment conditions. Full article
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<p>Prepared samples after heat treatment at different temperatures (IS = initial state).</p>
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<p>Measuring instruments used to examine the samples (mechanical testing laboratory, department of material engineering): (<b>a</b>) Zwick/Roell ZHµ micro-hardness tester; (<b>b</b>) Vickers manual hardness tester; (<b>c</b>) tear-off measuring device.</p>
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<p>The intrinsic magnetic field of the sample measurements: (<b>a</b>) diagram of the connection of measuring equipment (1: material specimen, 2: XYZ positioning system, 3: fluxgate sensor, 4: lock-in amplifier, 5: digital acquisition card, 6: PC workstation, 7: LabVIEW and MATLAB console, 8: XYZ stage controller, 9: synchronization device, 10: PTFE table, 11: EM-shielded chamber); (<b>b</b>) realization of the experiments in laboratory of electromagnetic nondestructive evaluation, University of Zilina.</p>
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<p>Fluxgate sensor used for magnetic field mapping: (<b>a</b>) geometry and placement of the single-axis sensor on the printed circuit board; (<b>b</b>) sensor’s calibration curve.</p>
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<p>Magnetic field mapping experimental arrangement: (<b>a</b>) an example of the scanning procedure; (<b>b</b>) comb scanning procedure.</p>
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<p>Experimental results: microstructure of AISI 304 in the initial state, induced by G + HF + HNO<sub>3</sub> etchant: (<b>a</b>) general microstructure; (<b>b</b>) microstructure detail.</p>
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<p>Microstructure of the inspected material: (<b>a</b>) AISI 304 at initial state indicating important features; (<b>b</b>) AISI 304 after annealing at 1100 °C at 400<math display="inline"><semantics> <mrow> <mo>×</mo> </mrow> </semantics></math> magnification.</p>
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<p>EDX mapping and analysis: detail of non-metallic manganese sulfide intrusions: (<b>a</b>) native SEM image; (<b>b</b>) SEM image with highlighted presence of sulfur and manganese; (<b>c</b>) SEM image with highlighted sulfur K-alpha emission line; (<b>d</b>) SEM image with highlighted manganese K-alpha emission line.</p>
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<p>Experimental results: microhardness of AISI 304 in the initial condition; (<b>a</b>) measurement from the proximal to the distal part; (<b>b</b>) measurement to the core of the sample.</p>
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<p>Experimental results: HV 10 of AISI 304 steel as a function of annealing temperature.</p>
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<p>Experimental results: intrinsic magnetic field of the selected samples for different annealing temperatures, L (left side): (<b>a</b>) <span class="html-italic">T</span> = 100 °C; (<b>b</b>) <span class="html-italic">T</span> = 200 °C; (<b>c</b>) <span class="html-italic">T</span> = 300 °C; (<b>d</b>) <span class="html-italic">T</span> = 400 °C; (<b>e</b>) <span class="html-italic">T</span> = 500 °C; (<b>f</b>) <span class="html-italic">T</span> = 600 °C; (<b>g</b>) <span class="html-italic">T</span> = 700 °C; (<b>h</b>) <span class="html-italic">T</span> = 800 °C; (<b>i</b>) <span class="html-italic">T</span> = 900 °C; (<b>j</b>) <span class="html-italic">T</span> = 1000 °C; (<b>k</b>) <span class="html-italic">T</span> = 1100 °C; (<b>l</b>) <span class="html-italic">T</span> = 1200 °C. The dashed lines indicate the location of the sample during the investigation.</p>
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<p>Experimental results: intrinsic magnetic field of the selected samples for different annealing temperatures, R (right side): (<b>a</b>) <span class="html-italic">T</span> = 100 °C; (<b>b</b>) <span class="html-italic">T</span> = 200 °C; (<b>c</b>) <span class="html-italic">T</span> = 300 °C; (<b>d</b>) <span class="html-italic">T</span> = 400 °C; (<b>e</b>) <span class="html-italic">T</span> = 500 °C; (<b>f</b>) <span class="html-italic">T</span> = 600 °C; (<b>g</b>) <span class="html-italic">T</span> = 700 °C; (<b>h</b>) <span class="html-italic">T</span> = 800 °C; (<b>i</b>) <span class="html-italic">T</span> = 900 °C; (<b>j</b>) <span class="html-italic">T</span> = 1000 °C; (<b>k</b>) <span class="html-italic">T</span> = 1100 °C; (<b>l</b>) <span class="html-italic">T</span> = 1200 °C. The dashed lines indicate the location of the sample during the investigation.</p>
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<p>Experimental results: intrinsic magnetic field as a function of annealing temperature.</p>
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<p>Experimental results: tear-off force of the samples depending on annealing temperature.</p>
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26 pages, 5407 KiB  
Article
Forced Dynamics of Elastically Connected Nano-Plates and Nano-Shells in Winkler-Type Elastic Medium
by Marija Stamenković Atanasov, Ivan R. Pavlović, Julijana Simonović, Cristina Borzan, Ancuţa Păcurar and Răzvan Păcurar
Appl. Sci. 2025, 15(5), 2765; https://doi.org/10.3390/app15052765 - 4 Mar 2025
Viewed by 204
Abstract
Nano-structures play a crucial role in advancing technology due to their unique properties and applications in various fields. This study examines the forced vibration behavior of an orthotropic nano-system consisting of an elastically connected nanoplate and a doubly curved shallow nano-shell. Both nano-elements [...] Read more.
Nano-structures play a crucial role in advancing technology due to their unique properties and applications in various fields. This study examines the forced vibration behavior of an orthotropic nano-system consisting of an elastically connected nanoplate and a doubly curved shallow nano-shell. Both nano-elements are simply supported and embedded in a Winkler-type elastic medium. Utilizing the Eringen constitutive elastic relation, Kirchhoff–Love plate theory, and Novozhilov’s linear shallow shell theory, we derive a system of four coupled nonhomogeneous partial differential equations (PDEs) describing the forced transverse vibrations of the system. We perform forced vibration analysis using modal analysis. The developed model is a novel approach that has not been extensively researched by other authors. Therefore, we provide insights into the nano-system of an elastically connected nanoplate and a doubly curved shallow nano-shell, offering a detailed analytical and numerical analysis of the PDEs describing transverse oscillations. This includes a clear insight into natural frequency analysis and the effects of the nonlocal parameter. Additionally, damping proportional coefficients and external excitation significantly influence the transverse displacements of both the nanoplate and nano-shell. The proposed mathematical model of the ECSNPS aids in developing new nano-sensors that respond to transverse vibrations based on the geometry of the nano-shell element. These sensors are often used to adapt to curved surfaces in medical practice and gas sensing. Full article
(This article belongs to the Section Nanotechnology and Applied Nanosciences)
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<p>The double graphene nano-system is composed of a nanoplate and a nano-shell and coupled by a Winkler-type elastic layer: (<b>a</b>) physical model; (<b>b</b>) mechanical model.</p>
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<p>Flow chart illustrates the procedures for obtaining the solutions of the presented nano-model.</p>
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<p>The nano-systems coupled by a Winkler-type elastic layer: (<b>a</b>) elastically connected system composed of nanoplate and nano-shell (ECSNPS); (<b>b</b>) elastically connected system from two nanoplates (ECSTNP).</p>
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<p>Comparison of the amplitude values of the forced vibrations of the ECSNPS and the ECSTNP: (<b>a</b>) the upper nanoplate of the ECSNPS with the upper nanoplate of the ECSTNP; (<b>b</b>) the lower nano-shell of the ECSNPS with the lower nanoplate of the ECSTNP.</p>
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<p>Effect of the radius of curvature R<sub>2</sub> on the transverse displacement for the first three modes of the ECSNPS: (<b>a</b>) nanoplate; (<b>b</b>) nano-shell.</p>
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<p>Effect of the one-sided- and double-sided-curved nano-shell on the transverse displacement for the first three modes of the ECSNPS: (<b>a</b>) nanoplate; (<b>b</b>) nano-shell.</p>
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<p>Effect of the external excitation on the transverse displacement for the first three modes of the ECSNPS: (<b>a</b>) nanoplate; (<b>b</b>) nano-shell.</p>
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<p>Effect of the nonlocal parameter on the transverse displacement for the first three modes of the ECSNPS: (<b>a</b>) nanoplate; (<b>b</b>) nano-shell.</p>
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<p>Effect of the damping proportional coefficients on the transverse displacement for the first three modes of the ECSNPS: (<b>a</b>) nanoplate; (<b>b</b>) nano-shell.</p>
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34 pages, 5540 KiB  
Article
The Use of Biomass-Derived Chitosan for Colorimetric pH Detection
by Ezekiel Edward Nettey-Oppong, Riaz Muhammad, Dohyun Yoo, Sun-Hyeop Hwang, Ahmed Ali, Chacha Saidi Mwita, Hyun-Woo Jeong, Seong-Wan Kim, Young-Seek Seok and Seung Ho Choi
Photonics 2025, 12(3), 231; https://doi.org/10.3390/photonics12030231 - 4 Mar 2025
Viewed by 102
Abstract
This study developed a sustainable colorimetric pH sensor using chitosan derived from mealworm (Tenebrio molitor) biomass and anthocyanin extracted from red cabbage (Brassica oleracea). Chitosan was used as the substrate material, and anthocyanin served as the pH indicator dye, [...] Read more.
This study developed a sustainable colorimetric pH sensor using chitosan derived from mealworm (Tenebrio molitor) biomass and anthocyanin extracted from red cabbage (Brassica oleracea). Chitosan was used as the substrate material, and anthocyanin served as the pH indicator dye, collectively forming the basis of the pH sensor. The resulting pH-responsive film effectively measures pH levels from 1 to 13, with a distinct color shift from pink to green. The sensor demonstrated remarkable stability, maintaining color fidelity after prolonged exposure to aqueous environments, and its practical functionality was confirmed through an ammonia detection assay, underscoring its utility in monitoring food freshness. Mechanistic investigations using Fourier-transform infrared spectroscopy (FTIR) and molecular modeling identified electrostatic and hydrophobic forces as key factors in anthocyanin binding to the chitosan matrix. Molecular modeling further revealed a minimal binding energy of −3 kcal/mol and an RMSD of 0 Å, indicating a strong interaction stability. The film exhibited high structural integrity, with tensile strength and elongation values of 8.8 MPa and 8.4%, respectively, and its flexibility suggests its suitability for diverse applications, including biomedical devices. The eco-friendly production process and the biocompatibility of this sensor provide a sustainable alternative to conventional pH measurement technologies. This innovation not only addresses ecological challenges but also expands the capabilities of colorimetric sensors for use in scientific research, biomedical applications, and other fields. Full article
(This article belongs to the Section Lasers, Light Sources and Sensors)
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<p>Schematic representation of the extraction process of chitosan from mealworm shells. The process involves pretreatment, demineralization with acetic acid, deproteinization with sodium hydroxide, and deacetylation to convert chitin into chitosan. Digital images at the center illustrate the key stages of extraction.</p>
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<p>Schematic representation of the extraction of anthocyanin and fabrication of the chitosan-based pH sensor. (<b>a</b>) Stepwise process for extracting anthocyanin from red cabbage. The fresh leaves of the red cabbage are cut into small pieces and mixed with water for a specified period. Subsequently, the resulting extract undergoes filtration, followed by centrifugation. The central portion of the figure presents the chemical structure of anthocyanin, with each constituent element of the structure appropriately labeled. (<b>b</b>) pH sensor fabrication via casting. The as-synthesized chitosan solution was mixed with the anthocyanin solution and cast onto a Petri dish, resulting in the formation of a chitosan-based pH sensor. The fabricated sensor displays a discernible color transition from pink to green, corresponding to acidic and basic conditions, respectively.</p>
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<p>Molecular modeling of chitosan. The modeling of the chitosan structure begins with a long-chain chitin structure model (<b>top</b>), followed by the deacetylation process in which N-acetyl groups within the chitin structure are converted into amino (NH<sub>2</sub>) groups (<b>middle</b>), resulting in a long-chain chitosan structure (<b>bottom</b>). The atom representations include green, white, blue, and red for carbon, hydrogen, nitrogen, and oxygen, respectively.</p>
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<p>Molecular changes in red cabbage anthocyanin with pH variations. The structural transformations of red cabbage anthocyanin across different pH ranges. The sequence includes changes from (<b>a</b>) flavylium cation (pH: &lt;2) to (<b>b</b>) quinoidal base, (<b>c</b>) anionic quinoidal base, and (<b>d</b>) carbinol pseudo-base (pH: 2–6), and (<b>e</b>) chalcone (pH: &gt;7) structures as pH transitions from acidic to basic regions. (<b>f</b>) UV-Vis absorption spectra from pH 1 to pH 13 of the extracted red cabbage anthocyanin.</p>
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<p>pH-induced color changes in anthocyanin- and chitosan-based pH sensor films. (<b>a</b>) Color transitions of the extracted anthocyanin, starting from its original plum color and changing to red or pink in strongly acidic regions to green or yellow in strongly basic regions when buffer solutions of varying pH are added. (<b>b</b>) Color changes of the fabricated chitosan-based pH sensor films, originally brown, transforming from pink in strongly acidic regions to green in strongly basic regions upon exposure to buffer solutions of different pH values. (<b>c</b>) Plot illustrating the variation in L* a* b* values in response to changing pH levels and (<b>d</b>) visualization of colors associated with specific pH values, plotted on the CIE XYZ color space for chitosan-based pH sensor films.</p>
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<p>pH-induced color changes in bleached chitosan-based pH sensor films. (<b>a</b>) Comparative images showing the difference between unbleached (brownish) and bleached (nearly transparent) solutions and the resulting films. The bleaching process significantly lightened the chitosan, resulting in a more transparent substrate for the pH sensor. (<b>b</b>) Visual representation of the color changes observed in the bleached chitosan-based pH sensor upon exposure to buffer solutions with pH values ranging from 1 to 13. (<b>c</b>) L* a* b* color space analysis of the bleached sensor, highlighting the clear individual domains corresponding to each pH value. The distinct separation of points illustrates the sensor’s enhanced ability to differentiate between pH levels compared to the unbleached sensor. (<b>d</b>) CIE XYZ color space mapping of the sensor’s response, showing the distribution of chromatic transitions across different pH levels.</p>
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<p>Color-fastness, ammonia assay, and sensitivity of chitosan-based pH sensor films. (<b>a</b>) The chitosan-based pH sensor film was immersed in water for 90 min, and the process was visually depicted at 30 min intervals. This figure captures the observed behavior and changes in the film over time. (<b>b</b>) Assessment of the durability of the chitosan-based pH sensor in water over time. UV-Vis absorption spectra of the extracted anthocyanin (stock) and the surrounding solution after immersing the chitosan-based pH sensor for intervals of 0, 30, 60, and 90 min. (<b>c</b>) Sequential images capturing the color changes of the chitosan-based pH sensor at 5 min intervals for 30 min when exposed to ammonia. The progression from brown to vivid green is visually represented. (<b>d</b>) A plot of the computed sensitivity of the chitosan-based pH sensor over time when exposed to ammonia, providing quantitative insights into the responsiveness of the sensor ammonia with the final film after exposure (insert).</p>
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<p>FTIR characterization. FTIR spectra of chitosan, anthocyanin, and the chitosan−based pH sensor (CPS) films, with their respective characteristic peaks indicated.</p>
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<p>Molecular configuration and interactions between chitosan and anthocyanin. Illustration of molecular interactions between chitosan and anthocyanin. The molecular docking of anthocyanin on the chitosan chain is displayed, highlighting the configuration of the lowest binding affinity and lowest root mean square deviation. The zoomed section provides a detailed view of the intermolecular interactions between chitosan and the rings of anthocyanin. These interactions are categorized as π-cation, representing electrostatic interactions between the protonated amino groups of chitosan and the π-electrons of anthocyanin’s aromatic rings, and π-sigma, depicting hydrophobic interactions between the aromatic π-orbitals of anthocyanin and the C-H bonds of chitosan.</p>
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<p>Contact angle and water vapor permeability measurements. (<b>a</b>) Contact angle measurements of the fabricated films: chitosan and chitosan-based pH sensor. Water vapor permeability plot illustrating the relationship between weight loss and time for (<b>b</b>) chitosan and (<b>c</b>) chitosan-based pH sensor films.</p>
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<p>Mechanical properties of chitosan-based pH sensor films. (<b>a</b>) Visual representation demonstrating the flexibility of both the chitosan and chitosan-based pH sensor films. The stress-strain curves elucidate the mechanical properties of (<b>b</b>) chitosan and (<b>c</b>) chitosan-based pH sensors.</p>
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12 pages, 470 KiB  
Article
Effects of Inertial Measurement Unit Location on the Validity of Vertical Acceleration Time-Series Data and Jump Height in Countermovement Jumping
by Dianne Althouse, Cassidy Weeks, Steven B. Spencer, Joonsun Park, Brennan J. Thompson and Talin Louder
Signals 2025, 6(1), 11; https://doi.org/10.3390/signals6010011 - 3 Mar 2025
Viewed by 341
Abstract
Inertial measurement units (IMUs) are an example of practical technology for measuring countermovement jump (CMJ) performance, but there is a need to enhance their validity. One potential strategy to achieve this is advancing the literature on IMU placement. Many studies opt to position [...] Read more.
Inertial measurement units (IMUs) are an example of practical technology for measuring countermovement jump (CMJ) performance, but there is a need to enhance their validity. One potential strategy to achieve this is advancing the literature on IMU placement. Many studies opt to position a single IMU on anatomical landmarks rather than determining placement based on anthropometric principles, despite the knowledge that linear mechanics act through the segmental centers of mass of the human body. The purpose of this study was to evaluate the impact of positioning IMU sensors to approximate the trunk and lower-extremity segmental centers of mass on the validity of vertical acceleration measurements and jump height (JH) estimation during CMJs. Thirty young adults (female n = 10, 21.3 (3.8) years, 166.1 (4.1) cm, 67.6 (11.3) kg; male n = 20, 22.0 (2.6) years, 179.2 (6.4) cm, 83.5 (17.1) kg) from a university setting participated in the study. Seven IMUs were positioned at the approximate centers of mass of the trunk, thighs, shanks, and feet. Using data from these sensors, 15 whole-body center of mass models were developed, including 1-, 2-, 3-, and 4-segment configurations derived from the trunk and three lower-body segments. The root mean square error (RMSE) of vertical acceleration was calculated for each IMU model by comparing its data against vertical acceleration measurements obtained from a force platform. JH estimates were calculated using the take-off velocity method and compared across IMU models and the force platform to evaluate for systematic bias. RMSE and JH values from the best-performing 1-, 2-, 3-, and 4-segment IMU models were analyzed for main effects using one-way analyses of variance. The best performing 2-segment (trunk and shanks; RMSE = 2.1 ± 1.3 m × s−2) and 3-segment (trunk, thighs, and feet; RMSE = 2.0 ± 1.2 m × s−2) IMU models returned significantly lower RMSE values compared to the 1- segment (trunk; RMSE = 3.0 ± 1.4 m × s−2) model (p = 0.021–0.041). No systematic bias was detected between the JH estimates derived from the best-performing IMU models and those obtained from the force platform (p = 0.91–0.99). Positioning multiple IMU sensors to approximate segmental centers of mass significantly improved the validity of vertical acceleration time-series data from CMJs. The findings highlight the importance of anthropometric-based IMU placement for enhancing measurement accuracy without introducing systematic bias. Full article
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<p>Linear relationship between countermovement jump heights derived from a 2-segment IMU model and a force platform criterion.</p>
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24 pages, 9546 KiB  
Article
Physiological Evaluation of User Experience in Unstable Automated Driving: A Comparative Study
by Sooncheon Hwang and Dongmin Lee
Appl. Sci. 2025, 15(5), 2683; https://doi.org/10.3390/app15052683 - 3 Mar 2025
Viewed by 260
Abstract
While automated-driving technology is advancing rapidly, human-centered research is still in its early stages. Research on negative user responses to automated driving is particularly limited in complex roadway environments such as roundabouts, where driving decisions typically depend on driver judgment and traffic conditions. [...] Read more.
While automated-driving technology is advancing rapidly, human-centered research is still in its early stages. Research on negative user responses to automated driving is particularly limited in complex roadway environments such as roundabouts, where driving decisions typically depend on driver judgment and traffic conditions. In these environments, automated-driving vehicles may exhibit unstable behaviors, such as sudden stops or forced intersection entries. Since successful interaction between users and automated systems is critical for widespread adoption, understanding when and how automated driving negatively affects users is essential. This study investigated user psychological responses and corresponding physiological changes during unstable automated-driving situations. Using a virtual environment driving simulator, we compared two scenarios: sensor-only automated driving (A.D(S)), which exhibited unstable driving patterns; and cooperative automated driving (A.D(C)), which achieved more stable performance through infrastructure communication. We analyzed the responses of 30 participants using electromyography (EMG) measurements and pupil diameter tracking, supplemented by qualitative evaluations. Results showed that A.D(S) participants experienced higher levels of frustration during prolonged waiting times compared to A.D(C) participants. In addition, sudden braking events elicited startle responses characterized by pupil dilation and elevated arm-muscle EMG readings. This research advances our understanding of how automated-driving behaviors affect user experience and emphasizes the importance of human factors in the development of automated-driving technologies. Full article
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<p>The driving simulator used in the experiment.</p>
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<p>EMG measurement device (<b>a</b>), eye-tracking device (<b>b</b>), and measurement target (<b>c</b>) used in the experiment.</p>
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<p>Overview of virtual road design and implementation of key sections.</p>
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<p>Distribution of driving experience of participants in the experiment.</p>
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<p>The scene of experiment.</p>
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<p>Changes in EMG (leg) activation values of participants according to A.D styles at different segmentations of roundabout.</p>
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<p>EMG (leg) activation values per roundabout segmentation.</p>
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<p>Changes in EMG (arm) activation values of participants according to A.D styles at different segmentations of merging.</p>
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<p>EMG (arm) activation values per segmentation of merging.</p>
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<p>Changes in EMG (leg) activation values of participants according to A.D styles at different segmentation of unsignalized intersection.</p>
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<p>Error bars of EMG (leg) activation values per segmentation of unsignalized intersection.</p>
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<p>Changes in pupil diameter of participants according to A.D styles at different segmentation of unsignalized intersection.</p>
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<p>Error bars of pupil diameter per segmentation of the unsignalized intersection.</p>
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<p>Changes in pupil diameter of participants according to A.V styles at different segmentation of crosswalk.</p>
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<p>Error bars of pupil diameter per segmentation of crosswalk.</p>
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<p>Evaluation results of participant frustration levels at roundabouts by automated-driving styles.</p>
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20 pages, 6759 KiB  
Article
Structural and Experimental Study of a Multi-Finger Synergistic Adaptive Humanoid Dexterous Hand
by Shengke Cao, Guanjun Bao, Lufeng Pan, Bangchu Yang and Xuanyi Zhou
Biomimetics 2025, 10(3), 155; https://doi.org/10.3390/biomimetics10030155 - 3 Mar 2025
Viewed by 190
Abstract
As the end-effector of a humanoid robot, the dexterous hand plays a crucial role in the process of robot execution. However, due to the complicated and delicate structure of the human hand, it is difficult to replicate human hand functionality, balancing structural complexity, [...] Read more.
As the end-effector of a humanoid robot, the dexterous hand plays a crucial role in the process of robot execution. However, due to the complicated and delicate structure of the human hand, it is difficult to replicate human hand functionality, balancing structural complexity, and cost. To address the problem, the article introduces the design and development of a multi-finger synergistic adaptive humanoid dexterous hand with underactuation flexible articulated fingers and integrated pressure sensors. The proposed hand achieves force feedback control, minimizes actuator use while enabling diverse grasping postures, and demonstrates the capability to handle everyday objects. It combines advanced bionics with innovative design to optimize flexibility, ease of manufacturing, and cost-effectiveness. Full article
(This article belongs to the Special Issue Bionic Wearable Robotics and Intelligent Assistive Technologies)
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<p>Scheme of the underactuated humanoid hand.</p>
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<p>Modules and tendons distribution of the underactuated humanoid hand.</p>
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<p>Exploded view of the finger model.</p>
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<p>Design of moving pulley. (<b>a</b>) Exploded view of the moving pulley model. (<b>b</b>) Top view of assembled moving pulley. (<b>c</b>) Motion trajectory of the pulley in the palm.</p>
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<p>Modeling of the movable pulley.</p>
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<p>The universal relationship between force transmission ratio and tendon angles for movable pulley.</p>
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<p>The relationship between force transmission ratio and symmetrical tendon angles for movable pulley.</p>
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<p>Structure design of the wrist.</p>
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<p>Structure design of the forearm.</p>
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<p>The outline of the circuit.</p>
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<p>Calibration curve and fitting curve of force sensor.</p>
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<p>Geometric diagram of the index finger.</p>
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<p>Static equilibrium diagram of the index finger in a bent state.</p>
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<p>Motion trajectory of index fingertip.</p>
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<p>Test of grasping posture. (<b>a</b>) Orange. (<b>b</b>) Egg. (<b>c</b>) Pen. (<b>d</b>) Tube. (<b>e</b>) Plastic bottle. (<b>f</b>) Spectacle case. (<b>g</b>) Medicine bottle. (<b>h</b>) Adhesive tape. (<b>i</b>) Pen. (<b>j</b>) Ruler. (<b>k</b>) Student card.</p>
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<p>Grasping process. (<b>a</b>) Lifting tennis. (<b>b</b>) Lifting peach. (<b>c</b>) Lifting shell. (<b>d</b>) Lifting card. (<b>e</b>) Lifting sprinkling bottle.</p>
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<p>Test of passive grasping force.</p>
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<p>Test of active grasping force.</p>
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<p>Test of grab–weight Ratio.</p>
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17 pages, 5038 KiB  
Article
Motion Gait Recognition of Lower Limb Exoskeleton Based on Particle Swarm Optimization-Based Extreme Learning Machine Algorithm
by Ting Liu, Kai Liu, Wuyi Luo, Jiange Kou, Haoran Zhan, Guangkai Yu, Qing Guo and Yan Shi
Actuators 2025, 14(3), 120; https://doi.org/10.3390/act14030120 - 2 Mar 2025
Viewed by 211
Abstract
A human gait recognition method based on the PSO-ELM algorithm is proposed in order to achieve coordinated movement between humans and lower limb exoskeletons. Ground reaction force (GRF) from the foot, and motion capture data (MCD) from two joints were collected through the [...] Read more.
A human gait recognition method based on the PSO-ELM algorithm is proposed in order to achieve coordinated movement between humans and lower limb exoskeletons. Ground reaction force (GRF) from the foot, and motion capture data (MCD) from two joints were collected through the exoskeleton device. The sample data were obtained through multiple experiments in different action scenarios, including standing still, walking on the flat, climbing up and down stairs, traveling up and down slopes, in addition to squatting down and standing up. The algorithm utilizes short-term posture data to recognize different posture movement patterns, with two advantages: (1) A user-friendly wearable device was constructed based on multi-source sensors distributed throughout the body, addressing multiple subjects with varying weights and heights, while being cost-effective and reliably and easily collecting data. (2) The PSO-ELM algorithm identifies key features of gait data, achieving a higher recognition accuracy than other advanced recognition methods, especially during arbitrary gait transition duration. Full article
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<p>Exoskeleton device.</p>
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<p>Config interface.</p>
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<p>IK interface.</p>
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<p>Motion capture.</p>
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<p>The gait acquisitions experiments under different motion patterns.</p>
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<p>The position of the left and right legs, knees, hips, and the soles of the left and right feet during walking.</p>
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<p>The smoothing effect of the left heel GRF signal: (<b>a</b>) original GRF signal; (<b>b</b>) processed GRF signal.</p>
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<p>The MCD before and after processing: (<b>a</b>) the original MCD signal; (<b>b</b>) the processed MCD signal.</p>
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<p>The structure of ELM.</p>
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<p>The flow of the PSO-ELM model.</p>
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<p>The training process and results of the PSO-ELM model of Subject 1: (<b>a</b>) the training process; (<b>b</b>) the confusion matrix.</p>
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<p>The training process and results of the FNN and the LSTM models of Subject 1: (<b>a</b>) the training process of the FNN; (<b>b</b>) the confusion matrix of the FNN; (<b>c</b>) the training process of the LSTM model; (<b>d</b>) the confusion matrix of the LSTM model.</p>
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<p>The recognition precision of the PSO-ELM model for each gait phase of Subject 1.</p>
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<p>The recognition precision for each gait phase of Subject 1: (<b>a</b>) the FNN; (<b>b</b>) the LSTM model.</p>
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<p>The recognition precision of the PSO-ELM model for each gait phase of Subject 1.</p>
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<p>The recognition precision for each gait phase of Subject 1: (<b>a</b>) the FNN; (<b>b</b>) the LSTM model.</p>
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26 pages, 3217 KiB  
Article
Fault-Tolerant Collaborative Control of Four-Wheel-Drive Electric Vehicle for One or More In-Wheel Motors’ Faults
by Han Feng, Yukun Tao, Jianbo Feng, Yule Zhang, Hongtao Xue, Tiansi Wang, Xing Xu and Peng Chen
Sensors 2025, 25(5), 1540; https://doi.org/10.3390/s25051540 - 1 Mar 2025
Viewed by 410
Abstract
A fault-tolerant collaborative control strategy for four-wheel-drive electric vehicles is proposed to address hidden safety issues caused by one or more in-wheel motor faults; the basic design scheme is that the control system is divided into two layers of motion tracking and torque [...] Read more.
A fault-tolerant collaborative control strategy for four-wheel-drive electric vehicles is proposed to address hidden safety issues caused by one or more in-wheel motor faults; the basic design scheme is that the control system is divided into two layers of motion tracking and torque distribution, and three systems, including driving, braking, and front-wheel steering are controlled collaboratively for four-wheel torque distribution. In the layer of motion tracking, a vehicle model with two-degree-of-freedom is employed to predict the control reference values of the longitudinal force and additional yaw moment required; four types of sensors, such as wheel speed, acceleration, gyroscope, and steering wheel angle, are used to calculate the actual values. At the torque distribution layer, SSOD and MSCD distribution schemes are designed to cope with two operating conditions, namely sufficient and insufficient output capacity after local hub motor failure, respectively, focusing on the objective function, constraints, and control variables of the MSCD control strategy. Finally, two operating environments, a straight-line track, and a DLC track, are set up to verify the effectiveness of the proposed control method. The results indicate that, compared with traditional methods, the average errors of the center of mass sideslip angle and yaw rate are reduced by at least 12.9% and 5.88%, respectively, in the straight-line track environment. In the DLC track environment, the average errors of the center of mass sideslip angle and yaw rate are reduced by at least 6% and 4.5%, respectively. The proposed fault-tolerant controller ensures that the four-wheel-drive electric vehicle meets the requirements of handling stability and safety under one or more hub motor failure conditions. Full article
(This article belongs to the Special Issue Intelligent Maintenance and Fault Diagnosis of Mobility Equipment)
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<p>Dynamics model of 4WDEV.</p>
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<p>Fault-tolerant control policies of 4WDEV with one or more in-wheel motors’ faults.</p>
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<p>Schematic of the simulation environment.</p>
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<p>Stability indicators of two torque distribution schemes in the first test scenario: (<b>a</b>) Sideslip angle, (<b>b</b>) Yaw rate.</p>
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<p>Actual vehicle velocity of 4WDEV in the first test scenario.</p>
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<p>Actual driving forces of four in-wheel motors in the first test scenario.</p>
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<p>Vehicle stability indicators of three torque distribution schemes in the second test scenario and a straight-line track: (<b>a</b>) Sideslip angle (<b>b</b>) Yaw rate.</p>
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<p>Actual vehicle velocity of three torque distribution schemes in the second test scenario and a straight-line track.</p>
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<p>Actual driving forces of four in-wheel motors in the second test scenario and a straight-line track.</p>
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<p>Vehicle stability indicators of three torque distribution schemes in the second test scenario and a DLC track: (<b>a</b>) Sideslip angle, (<b>b</b>) Yaw rate.</p>
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<p>Actual vehicle velocity of three torque distribution schemes in the second test scenario and a DLC track.</p>
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<p>Actual driving forces of four in-wheel motors in the second test scenario and a DLC track.</p>
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