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19 pages, 18125 KiB  
Article
Phase Separation of FUS with Poly(ADP-ribosyl)ated PARP1 Is Controlled by Polyamines, Divalent Metal Cations, and Poly(ADP-ribose) Structure
by Maria V. Sukhanova, Rashid O. Anarbaev, Konstantin N. Naumenko, Loic Hamon, Anastasia S. Singatulina, David Pastré and Olga I. Lavrik
Int. J. Mol. Sci. 2024, 25(22), 12445; https://doi.org/10.3390/ijms252212445 - 20 Nov 2024
Viewed by 215
Abstract
Fused in sarcoma (FUS) is involved in the formation of nuclear biomolecular condensates associated with poly(ADP-ribose) [PAR] synthesis catalyzed by a DNA damage sensor such as PARP1. Here, we studied FUS microphase separation induced by poly(ADP-ribosyl)ated PARP1WT [PAR-PARP1WT] or its [...] Read more.
Fused in sarcoma (FUS) is involved in the formation of nuclear biomolecular condensates associated with poly(ADP-ribose) [PAR] synthesis catalyzed by a DNA damage sensor such as PARP1. Here, we studied FUS microphase separation induced by poly(ADP-ribosyl)ated PARP1WT [PAR-PARP1WT] or its catalytic variants PARP1Y986S and PARP1Y986H, respectively, synthesizing (short PAR)-PARP1Y986S or (short hyperbranched PAR)-PARP1Y986H using dynamic light scattering, fluorescence microscopy, turbidity assays, and atomic force microscopy. We observed that biologically relevant cations such as Mg2+, Ca2+, or Mn2+ or polyamines (spermine4+ or spermidine3+) were essential for the assembly of FUS with PAR-PARP1WT and FUS with PAR-PARP1Y986S in vitro. We estimated the range of the FUS-to-PAR-PARP1 molar ratio and the cation concentration that are favorable for the stability of the protein’s microphase-separated state. We also found that FUS microphase separation induced by PAR-PARP1Y986H (i.e., a PARP1 variant attaching short hyperbranched PAR to itself) can occur in the absence of cations. The dependence of PAR-PARP1-induced FUS microphase separation on cations and on the branching of the PAR structure points to a potential role of the latter in the regulation of the formation of FUS-related biological condensates and requires further investigation. Full article
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Figure 1
<p>Typical volume-weighted size distributions for FUS, PARP1<sup>WT</sup>, PAR-PARP1<sup>WT</sup>, and a FUS–PAR-PARP1<sup>WT</sup> mixture. The profiles were obtained by means of experimental autocorrelation functions in the Zetasizer Nano ZS software. Average hydrodynamic radii (R<sub>h</sub>) computed from the distributions are presented as well. R<sub>h</sub> is the average value estimated from at least three DLS experiments. Size measurement was performed on FUS, PARP1<sup>WT</sup>, PAR-PARP1, and the mixture of FUS with PAR-PARP1<sup>WT</sup> in reaction mixtures consisting of either 2.5 µM PARP1, 10 μM FUS, and 2.5 µM PAR-PARP1<sup>WT</sup> or 10 μM FUS and 60–540 nM PAR-PARP1. The R<sub>h</sub> values were measured directly after 3 min incubation of FUS with PAR-PARP1<sup>WT</sup>.</p>
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<p>Submillimolar concentration of a cation promotes FUS microphase separation at a high FUS-to-PAR-PARP1 molar ratio. R<sub>h</sub> of FUS–PAR-PARP1 mixtures is presented as a function of the FUS-to-PAR-PARP1 molar ratio. R<sub>h</sub> is the average value estimated from at least three DLS experiments. Analyses of FUS higher-order structure in the presence of PAR-PARP1<sup>WT</sup> were performed in reaction mixtures consisting of 10 μM FUS and 50–540 nM PAR-PARP1 as well as 0.5 mM Mg<sup>2+</sup> (<b>a</b>), 0.1 mM Mn<sup>2+</sup> (<b>b</b>), 0.5 mM Ca<sup>2+</sup> (<b>c</b>), 0.4 mM Spd<sup>3+</sup> (<b>d</b>), or 0.1 mM Spn<sup>4+</sup> (<b>e</b>), as indicated in the figure. The underlining shows the FUS-to-PAR-PARP1 molar ratio at which we observed bimodal particle size distributions (<a href="#app1-ijms-25-12445" class="html-app">Figure S1</a>).</p>
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<p>Millimolar concentration of a cation promotes FUS microphase separation at a low FUS-to-PAR-PARP1 molar ratio. FUS higher-order structure analyses in the presence of PAR-PARP1<sup>WT</sup> were performed in reaction mixtures consisting of 4–5 μM FUS and 1.5–1.8 µM PAR-PARP1. PAR-PARP1 was mixed with FUS, the samples were equilibrated for 1 min, and R<sub>h</sub> was measured next (<a href="#app1-ijms-25-12445" class="html-app">Figure S2</a>). After that, the reactions were supplemented with 2 mM Mn<sup>2+</sup>, 12.5 mM Mg<sup>2+</sup>, 7 mM Ca<sup>2+</sup>, 12 mM Spd<sup>3+</sup>, or 2.3 mM Spn<sup>4+</sup>, and R<sub>h</sub> was measured again (<a href="#app1-ijms-25-12445" class="html-app">Figure S2</a>). To disrupt FUS–PAR-PARP1 assemblies stabilized by a cation, EDTA (5–30 mM) was added as indicated in the figure, and R<sub>h</sub> was measured in the EDTA-treated samples (<a href="#app1-ijms-25-12445" class="html-app">Figure S2</a>).</p>
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<p>Coassembly of FUS and PAR-PARP1 in the presence of Mg<sup>2+</sup>. Fluorescence images of 10 µM AF488-FUS and 2.5 µM PARP1 in the presence of 15 mM Mg<sup>2+</sup> (<b>a</b>) or 10 µM AF488-FUS and 2.5 µM PARP1 in the presence of 15 mM Mg<sup>2+</sup> and 1 mM NAD<sup>+</sup> (<b>b</b>,<b>c</b>). The fluorescence photos were captured before and after the addition of NAD<sup>+</sup> to FUS–PARP1 mixtures and 30–60 min incubation at room temperature. The reaction mixtures (20 µL) contained a buffer (25 mM HEPES-NaOH pH 7.5, 200 mM NaCl, 300 nM urea, and 2 mM dithiothreitol [DTT]), 10 µM AF488-FUS, 2.5 µM Cy3-PARP1, 15 mM Mg<sup>2+</sup>, and 1 mM NAD<sup>+</sup> as indicated.</p>
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<p>The PAR-PARP1 mutant producing hyperbranched PAR is more effective in the seeding of higher-order assembly of FUS. R<sub>h</sub> is presented as a function of the FUS-to-PAR-PARP1 molar ratio. R<sub>h</sub> is the average value estimated from at least three DLS experiments (<a href="#app1-ijms-25-12445" class="html-app">Figure S5</a>). (<b>a</b>,<b>b</b>) Analyses of FUS higher-order structure in the presence of either PAR-PARP1<sup>Y986S</sup> or PAR-PARP1<sup>Y986H</sup> were performed in reaction mixtures consisting of 10 μM FUS and either 60–285 nM PAR-PARP1<sup>Y986S</sup> (<b>a</b>) or 50–1000 nM PAR-PARP1<sup>Y986H</sup> (<b>b</b>) in the presence of 0.5 mM Mg<sup>2+</sup> as indicated in the figure. (<b>c</b>) Analyses of FUS higher-order structure in the presence of PAR-PARP1<sup>Y986H</sup> were performed in reaction mixtures consisting of 10 μM FUS and 60–250 nM PAR-PARP1<sup>Y986H</sup>. (<b>d</b>) FUS higher-order structure analyses in the presence of either PAR-PARP1<sup>Y986S</sup> or PAR-PARP1<sup>Y986H</sup> were performed in reaction mixtures consisting of 1.8 μM FUS and 2 µM PAR-PARP1. PAR-PARP1 was mixed with FUS, the samples were equilibrated for 1 min, and R<sub>h</sub> was measured. After that, the reactions were supplemented with 12.5 mM Mg<sup>2+</sup>, and R<sub>h</sub> was measured again. To disrupt FUS–PAR-PARP1 assemblies stabilized by a cation, EDTA (30 mM) was introduced as indicated in the figure, and R<sub>h</sub> was measured in the EDTA-treated samples.</p>
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<p>In contrast to PARP1<sup>WT</sup>, mutant PAR-PARP1<sup>Y986H</sup> (producing hyperbranched PAR) seeds higher-order assembly of FUS at a lower concentration of Mg<sup>2+</sup>, and the assembly has appreciable susceptibility to 1,6-hexanediol (1,6-HD) treatment. Histograms of turbidity of a PAR-PARP1-and-FUS solution (OD at 600 nm) as determined in the presence of different concentrations of Mg<sup>2+</sup>, 1,6-HD, and EDTA. The mean ± SD of three independent measurements (<a href="#app1-ijms-25-12445" class="html-app">Figures S6 and S7</a>). *** <span class="html-italic">p</span> &lt; 0.001 and * <span class="html-italic">p</span> &lt; 0.05; <span class="html-italic">t</span> test.</p>
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<p>PAR structure affect the size of the higher-order assembly of FUS with PAR-PARP1. (<b>a</b>) AFM visualization of PAR-PARP1<sup>WT</sup> and PAR-PARP1<sup>Y986H</sup> and their higher-order assemblies with FUS. Scale bar: 300 nm; Z scale (green square): from −1 to 3 nm and from −3 to 6 nm as indicated. Blue dashed squares show the different Z scale for the same area (<b>b</b>,<b>c</b>) Measurement of the particle diameter by AFM (horizontal bars denote the mean); <span class="html-italic">n</span> = 100 particles from three independent samples; paired <span class="html-italic">t</span> test, **** <span class="html-italic">p</span> &lt; 0.00001.</p>
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<p>The proposed model of cation-dependent assembly of FUS with PAR-PARP1. Cations stabilize FUS association with PAR-PARP1; such assembly is sensitive to chelating agents such as EDTA and to 1,6-hexanediol, which disrupts hydrophobic interactions.</p>
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16 pages, 9492 KiB  
Article
WO3-Based Thin Films Grown by Pulsed Laser Deposition as Gas Sensors for NO2 Detection
by Alessandro Bellucci, Angela De Bonis, Mariangela Curcio, Antonio Santagata, Maria Lucia Pace, Eleonora Bolli, Matteo Mastellone, Riccardo Polini, Raffaella Salerno, Veronica Valentini and Daniele M. Trucchi
Sensors 2024, 24(22), 7366; https://doi.org/10.3390/s24227366 - 19 Nov 2024
Viewed by 216
Abstract
Thin films based on tungsten oxide (WO3) were grown by nanosecond pulsed laser deposition on alumina printed-circuit boards to fabricate electrochemical sensors for nitrogen dioxide (NO2) detection. Samples exposed to thermal annealing (400 °C for 3 h) were also [...] Read more.
Thin films based on tungsten oxide (WO3) were grown by nanosecond pulsed laser deposition on alumina printed-circuit boards to fabricate electrochemical sensors for nitrogen dioxide (NO2) detection. Samples exposed to thermal annealing (400 °C for 3 h) were also produced to compare the main properties and the sensor performance. Before gas testing, the morphology and structural properties were investigated. Scanning electron microscopy and atomic force microscopy showed the formation of granular films with a more compact structure before the thermal treatment. Features of the main WO3 phases were identified for both as-deposited and annealed samples by Raman spectroscopy, whereas X-ray diffraction evidenced the amorphous nature of the as-deposited samples and the formation of crystalline phases after thermal annealing. The as-deposited samples showed a higher W/O ratio, as displayed by energy-dispersive X-ray spectroscopy. An Arrhenius plot revealed a lower activation energy (0.11 eV) for the as-deposited thin films, which are the most electrically conductive samples, presenting a better gas response (30% higher than the response of the annealed ones) in the investigated NO2 concentration range of 5–20 ppm at the moderate device operating temperature of 75 °C. This behavior is explained by a larger quantity of oxygen vacancies, which enhances the sensing mechanism. Full article
(This article belongs to the Section Optical Sensors)
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<p>Design for the WO<sub>3</sub>-based NO<sub>2</sub> sensors on an alumina PCB. The WO<sub>3</sub> thin film is deposited on the metallic fingers (i.e., half of the PCB) by using a mechanical mask. The values shown in the sketch are reported in mm.</p>
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<p>Sketch of the experimental setup. The system is composed of a commercial glove box equipped with an RH monitor and control system. For the gas exposure and the chamber evacuation, two lines are connected, one to a gas mixing system and the other one to a membrane pump. The gas concentration is obtained by mixing the flows from a synthetic air cylinder and calibrated cylinders (certified by the company Nippon Gases, Anagni, Italy, which provided the gas mixture) that are regulated by mass flow controllers. The sensor is electrically connected to an electrometer (Keithley 487), and the data acquisition is performed via a PC with customized software able to control and register the gas exposure, the electrical signals, and the RH level.</p>
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<p>Optical images of (<b>a</b>) as-deposited and (<b>b</b>) annealed films acquired around a finger (Au) of the PCB by using a 20× objective coupled to a DM6 M LEICA optical microscope and the LEICA EL6000 UV-Vis fluorescent light source.</p>
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<p>SEM images of (<b>a</b>,<b>c</b>) as-deposited films and (<b>b</b>,<b>d</b>) annealed thin films.</p>
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<p>AFM topographies of as-deposited (<b>a</b>) and annealed (<b>b</b>) WO<sub>3</sub> samples deposited on Al<sub>2</sub>O<sub>3</sub>.</p>
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<p>Raman spectra of as-deposited and annealed WO<sub>3</sub>-based thin films on alumina substrates.</p>
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<p>XRD spectra of the as-deposited and annealed WO<sub>3</sub>-based thin films on alumina substrates in the range 2θ 20–60°. The peaks not labeled by the crystallographic orientation correspond to the Al<sub>2</sub>O<sub>3</sub> substrate.</p>
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<p>SEM maps and EDX spectra (based on the points highlighted in the SEM image) for the annealed (<b>a</b>) and as-deposited (<b>b</b>) samples.</p>
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<p>Arrhenius plot of WO<sub>3</sub>-based thin films’ electrical resistance in the temperature range RT–200 °C.</p>
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<p>(<b>a</b>) Gas response curves (left arrows) and variation in resistance R<sub>0</sub> (right arrows) for the WO<sub>3</sub> thin-film sensors as a function of the operating temperatures for 20 ppm concentration of NO<sub>2</sub>; (<b>b</b>) dynamic response curves for the gas sensors and different gas concentration values at the fixed temperature of 75 °C; (<b>c</b>) gas response curves as a function of concentration at the fixed temperature of 75 °C considering the saturation point taken from the dynamic curves.</p>
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<p>Comparison of gas responses of the as-deposited WO<sub>3</sub> thin-film sensor to different gases at 75 °C at fixed gas concentration (110 ppm for CO<sub>2</sub>, 5 ppm for NO<sub>2</sub> and SO<sub>2</sub>, 55 ppb for O<sub>3</sub>). The gas concentration for each gas is the minimum level achievable in the calibrated experimental setup used for this study (labelled on each column for every gas).</p>
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<p>(<b>a</b>) Gas response of the as-deposited sample measured at 20 ppm after twenty continuous cycles of gas in/out; (<b>b</b>) example of dynamic response curves (eight curves) for the gas sensors at a fixed gas concentration of 20 ppm and a fixed temperature of 75 °C; (<b>c</b>) Raman spectra before and after the gas testing; (<b>d</b>) gas response of the as-deposited sample measured at 20 ppm on different days of measurements spanned for 4 months.</p>
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15 pages, 4980 KiB  
Article
Sensorless Design and Analysis of a Brushed DC Motor Speed Regulation System for Branches Sawing
by Shangshang Cheng, Huijun Zeng, Zhen Li, Qingting Jin, Shilei Lv, Jingyuan Zeng and Zhou Yang
Agriculture 2024, 14(11), 2078; https://doi.org/10.3390/agriculture14112078 - 19 Nov 2024
Viewed by 276
Abstract
Saw rotational speed critically influences cutting force and surface quality yet is often destabilized by variable cutting resistance. The sensorless detection method for calculating rotational speed based on current ripple can prevent the contact of wood chips and dust with Hall sensors. This [...] Read more.
Saw rotational speed critically influences cutting force and surface quality yet is often destabilized by variable cutting resistance. The sensorless detection method for calculating rotational speed based on current ripple can prevent the contact of wood chips and dust with Hall sensors. This paper introduces a speed control system for brushed DC motors that capitalizes on the linear relationship between current ripple frequency and rotational speed. The system achieves speed regulation through indirect speed measurement and PID control. It utilizes an H-bridge circuit controlled by the EG2014S driver chip to regulate the motor direction and braking. Current ripple detection is accomplished through a 0.02 Ω sampling resistor and AMC1200SDUBR signal amplifier, followed by a wavelet transform and Savitzky–Golay filtering for refined signal extraction. Experimental results indicate that the system maintains stable speeds across the 2000–6000 RPM range, with a maximum error of 2.32% at 6000 RPM. The improved ripple detection algorithm effectively preserves critical signals while reducing noise. This enables the motor to quickly regain speed when resistance is encountered, ensuring a smooth cutting surface. Compared to traditional Hall sensor systems, this sensorless design enhances adaptability in agricultural applications. Full article
(This article belongs to the Special Issue New Energy-Powered Agricultural Machinery and Equipment)
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<p>Structural model of brushed DC motor.</p>
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<p>Original ripple signal of brushed DC motor.</p>
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<p>Noise reduction process for motor current ripple.</p>
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<p>Brushed DC motor speed stabilisation system design.</p>
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<p>H-bridge drive circuit for brushed DC motor.</p>
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<p>Ripple current detection circuit.</p>
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<p>Improved wavelet denoising of ripple signals.</p>
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<p>Sawing experimental platform.</p>
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<p>Variation of voltage, current, and speed during resistance and stabilization.</p>
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<p>Performance comparison of steady-speed system.</p>
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21 pages, 5645 KiB  
Article
Design, Testing, and Validation of a Soft Robotic Sensor Array Integrated with Flexible Electronics for Mapping Cardiac Arrhythmias
by Abdellatif Ait Lahcen, Michael Labib, Alexandre Caprio, Mohsen Annabestani, Lina Sanchez-Botero, Weihow Hsue, Christopher F. Liu, Simon Dunham and Bobak Mosadegh
Micromachines 2024, 15(11), 1393; https://doi.org/10.3390/mi15111393 - 18 Nov 2024
Viewed by 329
Abstract
Cardiac mapping is a crucial procedure for diagnosing and treating cardiac arrhythmias. Still, current clinical techniques face limitations including insufficient electrode coverage, poor conformability to complex heart chamber geometries, and high costs. This study explores the design, testing, and validation of a 64-electrode [...] Read more.
Cardiac mapping is a crucial procedure for diagnosing and treating cardiac arrhythmias. Still, current clinical techniques face limitations including insufficient electrode coverage, poor conformability to complex heart chamber geometries, and high costs. This study explores the design, testing, and validation of a 64-electrode soft robotic catheter that addresses these challenges in cardiac mapping. A dual-layer flexible printed circuit board (PCB) was designed and integrated with sensors into a soft robotic sensor array (SRSA) assembly. Design considerations included flex PCB layout, routing, integration, conformity to heart chambers, sensor placement, and catheter durability. Rigorous SRSA in vitro testing evaluated the burst/leakage pressure, block force for electrode contact, mechanical integrity, and environmental resilience. For in vivo validation, a porcine model was used to demonstrate the successful deployment, conformability, and acquisition of electrograms in both the ventricles and atria. This catheter-deployable SRSA represents a meaningful step towards translating the integration of soft robotic actuators and stretchable electronics for clinical use, showcasing the unique mechanical and electrical performance that these designs enable. The high-density electrode array enabled rapid 2 s data acquisition with detailed spatial and temporal resolution, as illustrated by the clear and consistent cardiac signals recorded across all electrodes. The future of this work will lie in enabling high-density, anatomically conformable devices for detailed cardiac mapping to guide ablation therapy and other interventions. Full article
(This article belongs to the Section B:Biology and Biomedicine)
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<p>Schematic illustration of the four-legged sensor array assembly.</p>
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<p>The SRSA device’s integration steps start with (<b>i</b>) SRSA distal hub insertion into the Oscor catheter inlet, (<b>ii</b>) the insertion of the 6.5 Fr inner catheter into the outer 13.8 Fr catheter, (<b>iii</b>) the successful insertion of the four-legged SRSA into the catheter, (<b>iv</b>) the deployment of the four-legged SRSA, and (<b>v</b>) the whole device showing the four-legged SRSA integrated with the catheter.</p>
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<p>Custom-made rigid PCB board. (<b>a</b>) The KiCAD design of the rigid PCB. (<b>b</b>) The custom-made rigid PCB used to connect the SRSA with the National Instruments readout.</p>
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<p>Soft robotic sensor array assembly that shows the final catheter-delivered design.</p>
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<p>Bench testing performance: (<b>a</b>) designed 3D printed mock, (<b>b</b>) experiment setup, (<b>c</b>) force vs electrode location on the linear actuator, (<b>d</b>) force vs actuator location by the width of PVA, and (<b>e</b>) linear actuator and location of electrodes shown as red boxes.</p>
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<p>(<b>a</b>) An evaluation of conformability for multiple actuations using a deflection analysis (scale bar is 1 cm), (<b>b</b>) the effect of the actuation on the radius of curvature, (<b>c</b>) the actuator’s block force before (peach color) and after (green color) the durability tests (<b>d</b>) the electrical response measurements for the 16 electrodes on the actuator before and after 100 actuations.</p>
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<p>(<b>a</b>) Electrical response measurements between (<b>i</b>) neighboring and (<b>ii</b>) cross electrodes, (<b>b</b>) flex PCB/extender junction, (<b>c</b>) (<b>i</b>) linear actuator immersed in a saline medium under 37 °C for 7 days (<b>ii</b>) flex PCB/extender junction immersed in a saline medium under 37 °C for 1 day, (<b>d</b>) electrical resistance measurements for the 16 electrodes on the actuators at dry conditions, (after 1 and 7 days in saline at 37 °C, and (<b>e</b>) electrical response measurements for the 16 electrodes on flex PCB/extender at dry conditions and after days in saline at 37 °C.</p>
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<p>(<b>a</b>) (<b>i</b>) flex PCB/extender pads before break; (<b>ii</b>) flex PCB/extender pads after break. (<b>b</b>) Load-extension curve for tensile strength of flex PCB/extender junction pads.</p>
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<p>Conformability in cardiac chambers. (<b>A</b>) 3D model of catheter delivery progressing from the (<b>i</b>) inferior vena cava (IVC), (<b>ii</b>) left atrium, and (<b>iii</b>) left ventricle. (<b>B</b>) Sensor-tissue contact inside the heart location using fluoroscopy after deployment. (<b>C</b>) ICE catheter image that shows deployment of SRSA device in LV heart chamber. (<b>D</b>) Electrograms acquired while device was in left ventricle. (<b>E</b>) Electrograms acquired with one single actuator. (<b>F</b>) Phase shift between electrodes at Actuator 1 and 3. (<b>G</b>) Signal to noise ratio analysis for acquired electrograms.</p>
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14 pages, 1875 KiB  
Article
Position–Force Control of a Lower-Limb Rehabilitation Robot Using a Force Feed-Forward and Compensative Gravity Proportional Derivative Method
by Le T. H. Gam, Dam Hai Quan, Pham Van Bach Ngoc, Bui Hong Quan and Bui Trung Thanh
Electronics 2024, 13(22), 4494; https://doi.org/10.3390/electronics13224494 - 15 Nov 2024
Viewed by 317
Abstract
The design and control of lower-limb rehabilitation robots for patients after a stroke has gained significant attention. This paper presents the dynamic analysis and control of a 3-degrees-of-freedom lower-limb rehabilitation robot using combined position–force control based on the force feed-forward and compensative gravity [...] Read more.
The design and control of lower-limb rehabilitation robots for patients after a stroke has gained significant attention. This paper presents the dynamic analysis and control of a 3-degrees-of-freedom lower-limb rehabilitation robot using combined position–force control based on the force feed-forward and compensative gravity proportional derivative methods. In the lower-limb rehabilitation robot, the interaction force between the patient with the joints and links of the robot is uncertain and nonlinear due to the disturbance effect of Coriolis force, centrifugal force, gravitational force, and friction force. During recovery stages, the forces exerted by the patient’s lower limbs are also considered disturbances. Therefore, to meet the quality requirements in using the rehabilitation robot with different recovery stages of patient training, combining position control and force control is essential. In this paper, we proposed a combination of proportional–derivative gravity compensation motion control and force feed-forward control to form an advanced combined controller (position–force feed-forward control—PFFC) for a 3 DOF lower-limb functional rehabilitation robot. The forces can be sensed using a 3-axis force sensor. In addition, the robot’s position parameters are also measured by encoders. The control algorithm is implemented on the STM32F4 Discovery board. A verified test of the proposed control method is shown in the experiments, showing the good performance of the system. Full article
(This article belongs to the Section Bioelectronics)
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<p>The schematic diagram of the 3 DOF rehabilitation robot.</p>
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<p>The structure diagram of the controller.</p>
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<p>The experiment model (<b>Left</b>—prototype, <b>Right</b>—device connection diagram).</p>
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<p>Tracking angles with different controller’s parameters ((<b>a</b>)—case 1, (<b>b</b>)—case 2, (<b>c</b>)—case 3 and (<b>d</b>)—case 4).</p>
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<p>Joint trajectories and corresponding forces ((<b>a</b>)—case 1, (<b>b</b>)—case 2, (<b>c</b>)—case 3 and (<b>d</b>)—case 4).</p>
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<p>The reference motion trajectory (<b>a</b>) and reference toque of the hip joint (<b>b</b>).</p>
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<p>Joint-angle trajectory when an external force acts on the joint in one direction (<b>a</b>); and when an external force of unknown value acts on the joints in two directions (<b>b</b>).</p>
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<p>The torque at the hip joint when external forces act in one direction with different external force values (<b>a</b>); and when an external force of unknown value acts in two directions (<b>b</b>).</p>
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25 pages, 8370 KiB  
Article
The Analysis of the ZnO/Por-Si Hierarchical Surface by Studying Fractal Properties with High Accuracy and the Behavior of the EPR Spectra Components in the Ordering of Structure
by Tatyana Seredavina, Rashid Zhapakov, Danatbek Murzalinov, Yulia Spivak, Nurzhan Ussipov, Tatyana Chepushtanova, Aslan Bolysbay, Kulzira Mamyrbayeva, Yerik Merkibayev, Vyacheslav Moshnikov, Aliya Altmyshbayeva and Azamat Tulegenov
Processes 2024, 12(11), 2541; https://doi.org/10.3390/pr12112541 - 14 Nov 2024
Viewed by 354
Abstract
A hierarchical surface that includes objects with different sizes, as a result of creating local fields, initiates a large number of effects. Micropores in the composition of macropores, as well as nanoclusters of the substance, were detected by scanning electron and atomic force [...] Read more.
A hierarchical surface that includes objects with different sizes, as a result of creating local fields, initiates a large number of effects. Micropores in the composition of macropores, as well as nanoclusters of the substance, were detected by scanning electron and atomic force microscopies on the surface of ZnO/Por-Si samples. An identical fractal dimension for all levels of the hierarchy was determined for these structures, which is associated with the same response to external excitation. Photoluminescence studies have shown the presence of localized levels in the band gap, with the probability of capturing both electrons and holes, which ensures charge transitions between energy bands. Decomposition of the electron paramagnetic resonance (EPR) signal into components made it possible to determine the manifestations of various types of interaction between paramagnetic particles, including the hyperfine structure of the spectrum. The ordering of the structure of the substance as a result of sequential annealing in the range from 300 to 500 °C was revealed in the EPR spectrum. This fact, as well as photo- and gas sensitivity for all types of samples studied, confirms the prospects of using these structures as sensors. Full article
(This article belongs to the Section Materials Processes)
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<p>Images of the sample surface without depositing ZnO layers: (<b>a</b>) SEM image taken at an angle of 12° to the horizontal axis, at magnification ×550, (<b>b</b>) SEM image taken at an angle of 12° to the horizontal axis, at magnification ×1200, (<b>c</b>) Optical microscope image of the surface of ground side of a silicon wafer.</p>
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<p>SEM image of a sample without depositing ZnO, taken vertically to the surface.</p>
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<p>Schematic representation of the structure of the porous layer of the sample without depositing ZnO layers.</p>
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<p>(<b>a</b>) SEM image of a macropore of a sample with 20 layers of ZnO; (<b>b</b>) The height distribution of structures at the boundary of macropores of a sample with 20 layers of ZnO, obtained by the Gwyddion program v2.64.</p>
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<p>(<b>a</b>) SEM image of a macropore of a sample with 25 layers of ZnO; (<b>b</b>) The height distribution of structures at the boundary of macropores of a sample with 25 layers of ZnO, obtained by the Gwyddion program v2.64.</p>
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<p>Microscopy images of the sample with 25 ZnO layers: (<b>a</b>) SEM image of the macroporous structure of the sample; (<b>b</b>) SEM image of the surface inside the macro pores; (<b>c</b>) AFM image of the microporous structure of the sample; (<b>d</b>) AFM image of the structure of nanocrystals formed between micropores, transformed in the Gwyddion program v2.64.</p>
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<p>Microscopy images of the sample with 25 ZnO layers: (<b>a</b>) SEM image of the macroporous structure of the sample; (<b>b</b>) SEM image of the surface inside the macro pores; (<b>c</b>) AFM image of the microporous structure of the sample; (<b>d</b>) AFM image of the structure of nanocrystals formed between micropores, transformed in the Gwyddion program v2.64.</p>
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<p>AFM images of the microporous structure of the sample with 25 layers of ZnO: (<b>a</b>) 10 × 10 µm, (<b>b</b>) 200 nm resolution.</p>
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<p>Dependence of the logarithm of the number of pores N(δ) on the scale δ for (<b>a</b>) macroporous level of surface hierarchy, (<b>b</b>) microporous level of surface hierarchy.</p>
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<p>A percentage error matrix for determining the number of pores of porous silicon using YOLOv8 neural network.</p>
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<p>(<b>a</b>) AFM image of nanoclusters located between micropores; (<b>b</b>) Dependence of the logarithm of the number of pores N(δ) on the scale δ for nanoscale level of surface hierarchy.</p>
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<p>The photoluminescence spectrum, decomposed by Gaussian for a sample of porous silicon without ZnO.</p>
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<p>Photoluminescence spectrum decomposed into Gaussians for a sample: (<b>a</b>) with 20 layers of ZnO, (<b>b</b>) with 25 layers of ZnO.</p>
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<p>The comparison of photoluminescence peak intensities for samples with 20 and 25 ZnO layers.</p>
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<p>The dependence of the resistance of the samples on the number of deposited layers of ZnO.</p>
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<p>EPR spectrum of the sample with 25 ZnO layers before annealing.</p>
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<p>Comparison of EPR spectra for extreme points at signal saturation (P<sub>1</sub>= 1 mW, P<sub>2</sub> = 7.4 mW).</p>
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<p>Changing the signal parameters for the components of the right doublet at microwave powers from 3.4 to 6.6 mW: (<b>a</b>) changing the signal intensity from microwave power; (<b>b</b>) changing the signal width from microwave power.</p>
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<p>The EPR spectrum for the sample without ZnO deposition, obtained by subtracting the spectra at 5.8 mW and 5.4 mW: 1—signal in the middle of the magnetic field sweep, 2—left doublet signal, 3—right doublet signal.</p>
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<p>The dependence of the intensity of the fourth component of the spectrum on the sequential increase in microwave power for a sample with 25 ZnO layers.</p>
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<p>Comparison of the dependences of the intensity of the fourth component of the spectrum on the sequential increase in microwave power for samples: 1—25 layers of ZnO, 2—without deposition ZnO.</p>
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<p>EPR spectrum decomposed into components for a sample with 25 ZnO layers: (<b>a</b>) after annealing at 300 °C, (<b>b</b>) after annealing at 400 °C, (<b>c</b>) after annealing at 500 °C.</p>
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26 pages, 6588 KiB  
Article
A Coverage Hole Recovery Method for 3D UWSNs Based on Virtual Force and Energy Balance
by Luoheng Yan and Zhongmin Huangfu
Electronics 2024, 13(22), 4446; https://doi.org/10.3390/electronics13224446 - 13 Nov 2024
Viewed by 290
Abstract
Underwater wireless sensor networks (UWSNs) have been applied in lots of fields. However, coverage holes are usually caused by complex underwater environment. Coverage holes seriously affect UWSNs’ performance and quality of service; thus, their recovery is crucial for 3D UWSNs. Although most of [...] Read more.
Underwater wireless sensor networks (UWSNs) have been applied in lots of fields. However, coverage holes are usually caused by complex underwater environment. Coverage holes seriously affect UWSNs’ performance and quality of service; thus, their recovery is crucial for 3D UWSNs. Although most of the current research recovery algorithms demand hole detection, the number of additional mobile nodes is too large, the communication and computing costs are high, and the coverage and energy balance are poor. Therefore, these methods are not suitable for UWSN hole repairing. In order to enhance the performance of hole recovery, a coverage hole recovery method for 3D UWSNs in complex underwater environments based on virtual force guidance and energy balance is proposed. The proposed method closely combines the node energy and considers complex environmental factors. A series of multi-dimensional virtual force models are established based on energy between nodes, area boundaries, zero-energy holes, low-energy coverage holes, underwater terrain, and obstacle forces. Then, a coverage hole recovery method for 3D UWSNs based on virtual force guidance and energy balance (CHRVE) is proposed. In this method, the direction and step size of mobile repairing node movement is guided by distributed computation of virtual forces, and the nodes are driven towards the target location by means of AUV or other carrier devices. The optimal position to improve coverage rate and node force balance is obtained. Simulation experiments show good adaptability and robustness to complex underwater terrain and different environments. The algorithm does not require precise coverage hole boundary detection. Furthermore, it balances network energy distribution significantly. Therefore, this method reduces the frequency of coverage hole emergence and network maintenance costs. Full article
(This article belongs to the Section Networks)
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<p>The virtual repulsive force.</p>
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<p>The virtual attractive force.</p>
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<p>The virtual repulsion forces at the boundary of the monitoring area.</p>
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<p>The virtual attractive force of hole grid point <span class="html-italic">Q<sub>j</sub></span> on <span class="html-italic">Ns<sub>i.</sub></span></p>
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<p>The force on the bottom or obstacle.</p>
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<p>Coverage hole recovery with CHRVE.</p>
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<p>The variation of network coverage rate with number of iterations.</p>
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<p>Multiple non-closed coverage holes and their initial coverage state.</p>
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<p>The coverage rate variation diagram for recovery of multiple open holes with different patching mode and number of nodes.</p>
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<p>Central closure coverage holes and their initial coverage state.</p>
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<p>The coverage rate variation diagram for recovery of central closure holes with different patching mode and number of nodes.</p>
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<p>The coverage holes formed by the remaining 38 nodes.</p>
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<p>The analyses for coverage rate and energy density variance.</p>
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<p>The analyses for coverage rate and energy density variance.</p>
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<p>Experiment on water bottom with complex terrain or obstacles.</p>
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<p>The coverage rate and energy density variance with number of iteration rounds for coverage holes recovery with underwater curved surfaces and obstacles.</p>
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<p>The movement energy consumption variance with number of iteration rounds for coverage holes recovery.</p>
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<p>The comparison of coverage rates for different algorithms.</p>
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<p>The comparison of energy density variance for different algorithms.</p>
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15 pages, 3407 KiB  
Article
Minimalist Design for Multi-Dimensional Pressure-Sensing and Feedback Glove with Variable Perception Communication
by Hao Ling, Jie Li, Chuanxin Guo, Yuntian Wang, Tao Chen and Minglu Zhu
Actuators 2024, 13(11), 454; https://doi.org/10.3390/act13110454 - 13 Nov 2024
Viewed by 255
Abstract
Immersive human–machine interaction relies on comprehensive sensing and feedback systems, which enable transmission of multiple pieces of information. However, the integration of increasing numbers of feedback actuators and sensors causes a severe issue in terms of system complexity. In this work, we propose [...] Read more.
Immersive human–machine interaction relies on comprehensive sensing and feedback systems, which enable transmission of multiple pieces of information. However, the integration of increasing numbers of feedback actuators and sensors causes a severe issue in terms of system complexity. In this work, we propose a pressure-sensing and feedback glove that enables multi-dimensional pressure sensing and feedback with a minimalist design of the functional units. The proposed glove consists of modular strain and pressure sensors based on films of liquid metal microchannels and coin vibrators. Strain sensors located at the finger joints can simultaneously project the bending motion of the individual joint into the virtual space or robotic hand. For subsequent tactile interactions, the design of two symmetrically distributed pressure sensors and vibrators at the fingertips possesses capabilities for multi-directional pressure sensing and feedback by evaluating the relationship of the signal variations between two sensors and tuning the feedback intensities of two vibrators. Consequently, both dynamic and static multi-dimensional pressure communication can be realized, and the vibrational actuation can be monitored by a liquid-metal-based sensor via a triboelectric sensing mechanism. A demonstration of object interaction indicates that the proposed glove can effectively detect dynamic force in varied directions at the fingertip while offering the reconstruction of a similar perception via the haptic feedback function. This device introduces an approach that adopts a minimalist design to achieve a multi-functional system, and it can benefit commercial applications in a more cost-effective way. Full article
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<p>Multi-dimensional pressure-sensing and feedback glove and its intelligent interaction system. Schematic diagram of the glove’s application in enhanced spatial immersive interaction, including (i) the structural diagram of the pressure sensor, (ii) the components of the vibration haptic feedback module, and (iii) the structural diagram of the bending sensor.</p>
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<p>Sensors of the multi-dimensional pressure-sensing and feedback glove. (<b>a</b>) Optical image of the pressure sensor; (<b>b</b>) optical image of the bending sensor; and (<b>c</b>) optical image of the interactive glove and the corresponding components.</p>
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<p>Working mechanism of the pressure sensor and the bending sensor. (<b>a</b>) The (i) schematic diagram of the pressure sensor, (ii) dimensional changes of the liquid metal electrodes in the normal and pressurized states, and (iii) changes in the A-A’ cross-section of the liquid metal electrodes; and (<b>b</b>) the (i) schematic diagram of the bending sensor, (ii) changes in the liquid metal electrodes in the normal and bending states, and (iii) dimensional changes in the bending sensors observed from view B.</p>
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<p>Characterization of the pressure sensor. (<b>a</b>) Schematic of the characterization method; (<b>b</b>) relationship between the sensor’s output signal and the pressure under loading conditions; (<b>c</b>) relationship between the pressure sensor’s output signal and the pressure under loading and unloading conditions; (<b>d</b>) real-time monitoring of the output signal changes during one cycle of pressure increase and decrease; (<b>e</b>) response and recovery times of the sensor; (<b>f</b>) repeatability test over 2000 cycles at 55 kPa; (<b>g</b>) relationship between the driven voltage of a coin vibration and the collected triboelectric voltage signal of the sensor; and (<b>h</b>) real-time triboelectric voltage signal as the driven voltage continues to increase.</p>
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<p>Characterization of the bending sensor. (<b>a</b>) Schematic of the characterization method; (<b>b</b>) relationship between the sensor’s output signal and the strain under tensile conditions; (<b>c</b>) relationship between the bending sensor’s output signal and the pressure under loading and unloading conditions; (<b>d</b>) response and recovery times of the sensor; (<b>e</b>) repeatability test over 2000 cycles at 20% strain; (<b>f</b>) response of the sensor to strain with a given initial torsion angle; and (<b>g</b>) response of the sensor to strain with a given initial curvature.</p>
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<p>Demonstration application of the multi-dimensional pressure-sensing and feedback glove. (<b>a</b>) Schematic of fingertip pressing status including (i) left side contact, (ii) right side contact, (iii) intermediate contact and (iv) rolling from left to right; (<b>b</b>) real-time output signals of the pressure sensor at different pressing angles; (<b>c</b>) feedback from the coin vibrators at different pressing angles with single vibrator running condition marked by grey and both vibrators running condition marked by pale yellow; (<b>d</b>) output signals from the bending sensor measure the stepped bending of the finger at an angle of 10 degrees each time up to 90 degrees; (<b>e</b>) response of the bending sensor under different bending methods; (<b>f</b>) various hand gestures labelled from ① to ⑧ used to test the bending sensor; (<b>g</b>) output signals corresponding to different hand gestures labelled from ② to ⑧; (<b>h</b>) demonstration of grasping a test tube; (<b>i</b>) feedback from coin vibrators during the grasping process; (<b>j</b>) real-time signal output during the grasp; and (<b>k</b>) snapshot of pressure and bending angles before and after grasping.</p>
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28 pages, 10542 KiB  
Article
Heat Transfer Efficiency While Cooling with a Water Spray, Air-Assisted Water Spray and Water Jet Under Boiling and Single-Phase Forced Convection Conditions
by Elżbieta Jasiewicz, Beata Hadała, Agnieszka Cebo-Rudnicka, Zbigniew Malinowski, Kamil Jasiewicz and Dmytro Svyetlichnyy
Appl. Sci. 2024, 14(22), 10428; https://doi.org/10.3390/app142210428 - 13 Nov 2024
Viewed by 347
Abstract
The main purpose of this paper was to determine and compare the boundary conditions of heat transfer on the cooled surface of a cylindrical sensor made of Inconel 600 alloy while cooling with a water jet, water spray and air-assisted water spray under [...] Read more.
The main purpose of this paper was to determine and compare the boundary conditions of heat transfer on the cooled surface of a cylindrical sensor made of Inconel 600 alloy while cooling with a water jet, water spray and air-assisted water spray under high-temperature conditions. The inverse method for the heat conduction equation was used to determine the boundary conditions. Experimental tests were carried out, including temperature measurements at several points inside the cylinder while cooling with all the tested systems from a temperature of 900 °C for three values of water pressure: 0.05 MPa, 0.1 MPa and 0.2 MPa. Temperature measurements were used as the input data to identify the heat transfer boundary conditions. The temperature field of the axially symmetric sensor was determined using the finite element method. The boundary conditions were determined as average values of the heat transfer coefficient and heat flux and local values of the heat transfer coefficient. A comparison of the amount of thermal energy dissipating from the sensor surface as a result of boiling and a forced single-phase convection is also presented in the paper. The highest uniformity of cooling was obtained during air-assisted water spray-cooling. Full article
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<p>Schematic diagram of the sensor construction; JET cooling system.</p>
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<p>Schematic diagram of the sensor construction; WS cooling system.</p>
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<p>A diagram of them experimental stand: 1—water tank, 2—water pump, 3—air compressor, 4—electric resistance furnace, 5—furnace door, 6—nozzle, 7—sensor, 8—automatic feeder, 9—furnace control system, 10—data acquisition system, 11—computer.</p>
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<p>JET-cooling of the sensor.</p>
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<p>WS-cooling of the sensor.</p>
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<p>Thermocouple locations.</p>
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<p>Scheme of the system for measuring the amount of water: 1—nozzle, 2—hollow sleeve, 3—rubber hose, 4—feeder, 5—cooling chamber, 6—measuring cylinder.</p>
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<p>System for measuring the amount of water.</p>
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<p>The volume of water collected in a measuring cylinder at times (<span class="html-italic">τ<sub>w</sub></span>) during the six measurements, AAS, <span class="html-italic">p</span> = 0.2 MPa.</p>
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<p>Time of collection of the volume of water (<span class="html-italic">V</span>) in the measuring cylinder during the six measurements, AAS, <span class="html-italic">p</span> = 0.2 MPa.</p>
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<p>Finite element mesh with the location of thermocouples.</p>
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<p>Simulated temperature errors resulted from the temperature measurement for the thermocouple located at point P2.</p>
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<p>Comparison of the measured and calculated temperatures at points P1, P2, P3 and P4.</p>
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<p>Comparison of the inverse solution to the HTC with the referenced HTC described by Equation (33).</p>
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<p>The <span class="html-italic">A<sub>1</sub></span> and <span class="html-italic">A<sub>2</sub></span> areas used for the comparison of average HF and HTC variation.</p>
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<p>Comparison of the temperature changes between the measured and calculated temperatures, AAS, <span class="html-italic">p</span> = 0.1 MPa.</p>
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<p>Comparison of the temperature changes between the measured and calculated temperatures, WS, <span class="html-italic">p</span> = 0.1 MPa.</p>
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<p>Comparison of the temperature changes between the measured and calculated temperatures, JET, <span class="html-italic">p</span> = 0.1 MPa.</p>
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<p>Comparison of the change in average HTC values from the surface temperature (<b>A</b>) and time (<b>B</b>) during cooling using three systems of cooling, <span class="html-italic">A<sub>1</sub></span>.</p>
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<p>Comparison of the change in average HF values from the surface temperature (<b>A</b>) and time (<b>B</b>) during cooling using three systems of cooling, <span class="html-italic">A<sub>1</sub></span>.</p>
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<p>Comparison of the change in average HTC values from the surface temperature (<b>A</b>) and time (<b>B</b>) during cooling using three systems of cooling, <span class="html-italic">A<sub>2</sub></span>.</p>
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<p>Comparison of the change in average HF values from the surface temperature (<b>A</b>) and time (<b>B</b>) during cooling using three systems of cooling, <span class="html-italic">A<sub>2</sub></span>.</p>
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<p>Thermal characteristics of the coolant during cooling with the three cooling systems, <span class="html-italic">A<sub>2</sub></span>.</p>
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<p>The local HTC values depending on the surface temperature, AAS, <span class="html-italic">p</span> = 0.1 MPa.</p>
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<p>The local HTC values depending on the surface temperature, WS, <span class="html-italic">p</span> = 0.1 MPa.</p>
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<p>The local HTC values depending on the surface temperature, JET, <span class="html-italic">p</span> = 0.1 MPa.</p>
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<p>Cooling non-uniformity during cooling with the three tested cooling systems.</p>
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<p>The ranges of air cooling, boiling and forced single-phase convection, AAS, <span class="html-italic">A<sub>2</sub></span>, <span class="html-italic">p</span> = 0.1 MPa.</p>
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<p>Comparison of the amount of energy dissipating from the sensor surface during cooling using the three systems as a result of boiling and forced single-phase convection, <span class="html-italic">A<sub>2</sub></span>.</p>
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18 pages, 7562 KiB  
Article
Reliable and Resilient Wireless Communications in IoT-Based Smart Agriculture: A Case Study of Radio Wave Propagation in a Corn Field
by Blagovest Nikolaev Atanasov, Nikolay Todorov Atanasov and Gabriela Lachezarova Atanasova
Telecom 2024, 5(4), 1161-1178; https://doi.org/10.3390/telecom5040058 - 12 Nov 2024
Viewed by 577
Abstract
In the past few years, one of the largest industries in the world, the agriculture sector, has faced many challenges, such as climate change and the depletion of limited natural resources. Smart Agriculture, based on IoT, is considered a transformative force that will [...] Read more.
In the past few years, one of the largest industries in the world, the agriculture sector, has faced many challenges, such as climate change and the depletion of limited natural resources. Smart Agriculture, based on IoT, is considered a transformative force that will play a crucial role in the further advancement of the agri-food sector. Furthermore, in IoT-based Smart Agriculture systems, radio wave propagation faces unique challenges (such as attenuation in vegetation and soil and multiple reflections) because of sensor nodes deployed in agriculture fields at or slightly above the ground level. In our study, we present, for the first time, several models (Multi-slope, Weissberger, and COST-235) suitable for planning radio coverage in a cornfield for Smart Agriculture applications. We received signal level measurements as a function of distance in a corn field (R3 corn stage) at 0.9 GHz and 2.4 GHz using two transmitting and two receiving antenna heights, with both horizontal and vertical polarization. The results indicate that radio wave propagation in a corn field is influenced not only by the surrounding environment (i.e., corn), but also by the antenna polarization and the positions of the transmitting and receiving antennas relative to the ground. Full article
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<p>Measurements in a corn field in the agricultural area near Dabravata Village, Yablanitsa Municipality, Bulgaria: (<b>a</b>) Google Earth image; (<b>b</b>) photo from the corn field.</p>
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<p>Configuration of the measurement setup.</p>
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<p>Measurement site: (<b>a</b>) Google Earth image with Tx and Rx antenna locations in the corn field; (<b>b</b>) photo of Rx antenna placed below the corn height; (<b>c</b>) photo of Rx antenna placed above the corn height; (<b>d</b>) direction of measurement at the experimental corn field.</p>
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<p>Measured reflection coefficients for the two dipoles: (<b>a</b>) reference dipole used for measurements at 0.9 GHz; (<b>b</b>) reference dipole used for measurements at 2.4 GHz.</p>
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<p>Received signal level variation with distance at 0.9 GHz for co-polarized H-H and V-V antennas: (<b>a</b>) transmitting antenna is placed at a height of λ/3 m above ground (hTx = 0.11 m); (<b>b</b>) transmitting antenna is placed at a height of 0.5 m above ground (hTx = 0.5 m).</p>
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<p>Received signal level variation with distance at 2.4 GHz for co-polarized H-H and V-V antennas: (<b>a</b>) transmitting antenna is placed at a height of λ/3 m above ground (h<sub>Tx</sub> = 0.04 m); (<b>b</b>) transmitting antenna is placed at a height of 0.5 m above ground (h<sub>Tx</sub> = 0.5 m).</p>
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<p>Received signal level variation with distance at 0.9 GHz for co-polarized H-H and V-V antennas: (<b>a</b>) receiving antenna height below the corn height (h<sub>Rx</sub> = 2.0 m); (<b>b</b>) receiving antenna height above the corn height (h<sub>Rx</sub> = 3.4 m).</p>
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<p>Received signal level variation with distance at 2.4 GHz for co-polarized H-H and V-V antennas: (<b>a</b>) receiving antenna height below the corn height (h<sub>Rx</sub> = 2.0 m); (<b>b</b>) receiving antenna height above the corn height (h<sub>Rx</sub> = 3.4 m).</p>
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<p>Comparison between losses for co-polarized H-H antennas at transmitting antenna height λ/3 m with existing models: (<b>a</b>) 0.9 GHz, h<sub>Rx</sub> = 2.0 m; (<b>b</b>) 0.9 GHz, h<sub>Rx</sub> = 3.4 m; (<b>c</b>) 2.4 GHz, h<sub>Rx</sub> = 2.0 m; (<b>d</b>) 2.4 GHz, h<sub>Rx</sub> = 3.4 m.</p>
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<p>Comparison between losses for co-polarized V-V antennas at transmitting antenna height λ/3 m with existing models: (<b>a</b>) 0.9 GHz, h<sub>Rx</sub> = 2.0 m; (<b>b</b>) 0.9 GHz, h<sub>Rx</sub> = 3.4 m; (<b>c</b>) 2.4 GHz, h<sub>Rx</sub> = 2.0 m; (<b>d</b>) 2.4 GHz, h<sub>Rx</sub> = 3.4 m.</p>
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<p>Comparison between losses for co-polarized H-H antennas at transmitting antenna height 0.5 m with existing models: (<b>a</b>) 0.9 GHz, h<sub>Rx</sub> = 2.0 m; (<b>b</b>) 0.9 GHz, h<sub>Rx</sub> = 3.4 m; (<b>c</b>) 2.4 GHz, h<sub>Rx</sub> = 2.0 m; (<b>d</b>) 2.4 GHz, h<sub>Rx</sub> = 3.4 m.</p>
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<p>Comparison between losses for co-polarized V-V antennas at transmitting antenna height 0.5 m with existing models: (<b>a</b>) 0.9 GHz, h<sub>Rx</sub> = 2.0 m; (<b>b</b>) 0.9 GHz, h<sub>Rx</sub> = 3.4 m; (<b>c</b>) 2.4 GHz, h<sub>Rx</sub> = 2.0 m; (<b>d</b>) 2.4 GHz, h<sub>Rx</sub> = 3.4 m.</p>
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23 pages, 6035 KiB  
Article
A Study of Downlink Power-Domain Non-Orthogonal Multiple Access Performance in Tactile Internet Employing Sensors and Actuators
by Vaibhav Fanibhare, Nurul I. Sarkar and Adnan Al-Anbuky
Sensors 2024, 24(22), 7220; https://doi.org/10.3390/s24227220 - 12 Nov 2024
Viewed by 413
Abstract
The Tactile Internet (TI) characterises the transformative paradigm that aims to support real-time control and haptic communication between humans and machines, heavily relying on a dense network of sensors and actuators. Non-Orthogonal Multiple Access (NOMA) is a promising enabler of TI that enhances [...] Read more.
The Tactile Internet (TI) characterises the transformative paradigm that aims to support real-time control and haptic communication between humans and machines, heavily relying on a dense network of sensors and actuators. Non-Orthogonal Multiple Access (NOMA) is a promising enabler of TI that enhances interactions between sensors and actuators, which are collectively considered as users, and thus supports multiple users simultaneously in sharing the same Resource Block (RB), consequently offering remarkable improvements in spectral efficiency and latency. This article proposes a novel downlink power domain Single-Input Single-Output (SISO) NOMA communication scenario for TI by considering multiple users and a base station. The Signal-to-Interference Noise Ratio (SINR), sum rate and fair Power Allocation (PA) coefficients are mathematically derived in the SISO-NOMA system model. The simulations are performed with two-user and three-user scenarios to evaluate the system performance in terms of Bit Error Rate (BER), sum rate and latency between SISO-NOMA and traditional Orthogonal Multiple Access (OMA) schemes. Moreover, outage probability is analysed with varying fixed Power Allocation (PA) coefficients in the SISO-NOMA scheme. In addition, we present the outage probability, sum rate and latency analyses for fixed and derived fair PA coefficients, thus promoting dynamic PA and user fairness by efficiently utilising the available spectrum. Finally, the performance of 4 × 4 Multiple-Input Multiple-Output (MIMO) NOMA incorporating zero forcing-based beamforming and a round-robin scheduling process is compared and analysed with SISO-NOMA in terms of achievable sum rate and latency. Full article
(This article belongs to the Special Issue Wireless Sensor Network and IoT Technologies for Smart Cities)
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<p>Illustrating of OMA and NOMA schemes.</p>
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<p>Downlink power-domain communication scenario in TI.</p>
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<p>BER comparison between SISO-NOMA and OMA with <math display="inline"><semantics> <mi>η</mi> </semantics></math> = 2 and 4, and fixed PA coefficient pairs as (<math display="inline"><semantics> <mrow> <msub> <mi>α</mi> <mn>1</mn> </msub> <mo>=</mo> <mn>0.70</mn> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <msub> <mi>α</mi> <mn>2</mn> </msub> <mo>=</mo> <mn>0.30</mn> </mrow> </semantics></math>) and (<math display="inline"><semantics> <mrow> <msub> <mi>α</mi> <mn>1</mn> </msub> <mo>=</mo> <mn>0.80</mn> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <msub> <mi>α</mi> <mn>2</mn> </msub> <mo>=</mo> <mn>0.20</mn> </mrow> </semantics></math>). (<b>a</b>) BER comparison between SISO-NOMA and OMA with <math display="inline"><semantics> <mi>η</mi> </semantics></math> as 2. (<b>b</b>) BER comparison between SISO-NOMA and OMA with <math display="inline"><semantics> <mi>η</mi> </semantics></math> as 4.</p>
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<p>BER comparison between SISO-NOMA and OMA with <math display="inline"><semantics> <mi>η</mi> </semantics></math> = 2 and 4, and fixed PA coefficient pairs as (<math display="inline"><semantics> <mrow> <msub> <mi>α</mi> <mn>1</mn> </msub> <mo>=</mo> <mn>0.70</mn> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mi>α</mi> <mn>2</mn> </msub> <mo>=</mo> <mn>0.20</mn> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <msub> <mi>α</mi> <mn>3</mn> </msub> <mo>=</mo> <mn>0.10</mn> </mrow> </semantics></math>) and (<math display="inline"><semantics> <mrow> <msub> <mi>α</mi> <mn>1</mn> </msub> <mo>=</mo> <mn>0.76</mn> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mi>α</mi> <mn>2</mn> </msub> <mo>=</mo> <mn>0.16</mn> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <msub> <mi>α</mi> <mn>3</mn> </msub> <mo>=</mo> <mn>0.08</mn> </mrow> </semantics></math>). (<b>a</b>) BER comparison between SISO-NOMA and OMA with <math display="inline"><semantics> <mi>η</mi> </semantics></math> as 2. (<b>b</b>) BER comparison between SISO-NOMA and OMA with <math display="inline"><semantics> <mi>η</mi> </semantics></math> as 4.</p>
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<p>Achievable sum rate comparison between SISO-NOMA and OMA.</p>
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<p>Outage probability of SISO-NOMA scheme.</p>
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<p>Outage probability of fair PA with a two-user scenario. (<b>a</b>) Outage probability of fair PA. (<b>b</b>) Improved outage probability of fair PA.</p>
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<p>Achievable sum rate comparison between fair and fixed PAs.</p>
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<p>Latency comparison between SISO-NOMA and OMA with <math display="inline"><semantics> <mi>η</mi> </semantics></math> = 2 and fixed PA coefficient (<math display="inline"><semantics> <mrow> <msub> <mi>α</mi> <mn>1</mn> </msub> <mo>=</mo> <mn>0.70</mn> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mi>α</mi> <mn>2</mn> </msub> <mo>=</mo> <mn>0.20</mn> </mrow> </semantics></math> &amp; <math display="inline"><semantics> <mrow> <msub> <mi>α</mi> <mn>3</mn> </msub> <mo>=</mo> <mn>0.10</mn> </mrow> </semantics></math>).</p>
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<p>Latency comparison between fair and fixed PAs in SISO-NOMA.</p>
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<p>Achievable sum rate comparison between 4 × 4 MIMO-NOMA and SISO-NOMA.</p>
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<p>Latency comparison between 4 × 4 MIMO-NOMA and SISO-NOMA.</p>
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21 pages, 5673 KiB  
Article
HaptiScan: A Haptically-Enabled Robotic Ultrasound System for Remote Medical Diagnostics
by Zoran Najdovski, Siamak Pedrammehr, Mohammad Reza Chalak Qazani, Hamid Abdi, Sameer Deshpande, Taoming Liu, James Mullins, Michael Fielding, Stephen Hilton and Houshyar Asadi
Robotics 2024, 13(11), 164; https://doi.org/10.3390/robotics13110164 - 10 Nov 2024
Viewed by 685
Abstract
Medical ultrasound is a widely used diagnostic imaging modality that provides real-time imaging at a relatively low cost. However, its widespread application is hindered by the need for expert operation, particularly in remote regional areas where trained sonographers are scarce. This paper presents [...] Read more.
Medical ultrasound is a widely used diagnostic imaging modality that provides real-time imaging at a relatively low cost. However, its widespread application is hindered by the need for expert operation, particularly in remote regional areas where trained sonographers are scarce. This paper presents the development of HaptiScan, a state-of-the-art telerobotic ultrasound system equipped with haptic feedback. The system utilizes a commercially available robotic manipulator, the UR5 robot from Universal Robots, integrated with a force/torque sensor and the Phantom Omni haptic device. This configuration enables skilled sonographers to remotely conduct ultrasound procedures via an internet connection, addressing both the geographic and ergonomic limitations faced in traditional sonography. Key innovative features of the system include real-time force feedback, ensuring that sonographers can precisely control the ultrasound probe from a remote location. The system is further enhanced by safety measures such as over-force sensing, patient discomfort monitoring, and emergency stop mechanisms. Quantitative indicators of the system’s performance include successful teleoperation over long distances with time delays, as demonstrated in simulations. These simulations validate the system’s control methodologies, showing stable performance with force feedback under varying time delays and distances. Additionally, the UR5 manipulator’s precision, kinematic, and dynamic models are mathematically formulated to optimize teleoperation. The results highlight the effectiveness of the proposed system in overcoming the technical challenges of remote ultrasound procedures, offering a viable solution for real-world telemedicine applications. Full article
(This article belongs to the Special Issue Development of Biomedical Robotics)
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<p>The graphical abstract representation of the proposed methodology in this research.</p>
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<p>(<b>a</b>) Haptically-Enabled Robotic Ultrasound Platform; (<b>b</b>) CAD model of the HaptiScan platform.</p>
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<p>The kinematics representation of Phantom Omni.</p>
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<p>Vectorial representation of Phantom Omni: (<b>a</b>) top view; (<b>b</b>) side view.</p>
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<p>UR5 robot model with the DH coordinate frames assignments.</p>
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<p>(<b>a</b>) Signostics Signos RT handheld ultrasound device [<a href="#B45-robotics-13-00164" class="html-bibr">45</a>], (<b>b</b>) ultrasound probe support mechanism with ATI Nano 17 sensor.</p>
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<p>UR5 robot model with the DH coordinate frames assignments.</p>
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<p>Teleoperation system scheme.</p>
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<p>The SimMechanics model of Phantom Omni.</p>
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<p>Time delay.</p>
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<p>Cartesian position and orientation of the slave manipulator.</p>
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<p>(<b>a</b>) Cartesian velocity of both manipulators; (<b>b</b>) Cartesian velocity error of the manipulators.</p>
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<p>(<b>a</b>) Joints’ angle and velocity of the master manipulator; (<b>b</b>) Joints’ angle and velocity of the slave manipulator.</p>
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<p>Force error observed during the teleoperation under varying time delays.</p>
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13 pages, 2712 KiB  
Article
External Validation of Accelerometry-Based Mechanical Loading Prediction Equations
by Lucas Veras, Daniela Oliveira, Florêncio Diniz-Sousa, Giorjines Boppre, Ana Resende-Coelho, José Oliveira and Hélder Fonseca
Appl. Sci. 2024, 14(22), 10292; https://doi.org/10.3390/app142210292 - 8 Nov 2024
Viewed by 432
Abstract
Accurately predicting physical activity-associated mechanical loading is crucial for developing and monitoring exercise interventions that improve bone health. While accelerometer-based prediction equations offer a promising solution, their external validity across different populations and activity contexts remains unclear. This study aimed to validate existing [...] Read more.
Accurately predicting physical activity-associated mechanical loading is crucial for developing and monitoring exercise interventions that improve bone health. While accelerometer-based prediction equations offer a promising solution, their external validity across different populations and activity contexts remains unclear. This study aimed to validate existing mechanical loading prediction equations by applying them to a sample and testing conditions distinct from the original validation studies. A convenience sample of 49 adults performed walking, running, and jumping activities on a force plate while wearing accelerometers at their hip, lower back, and ankle. Peak ground reaction force (pGRF) and peak loading rate (pLR) predictions were assessed for accuracy. Substantial variability in prediction accuracy was found, with pLR showing the highest errors. These findings highlight the need to improve prediction models to account for individual biomechanical differences, sensor placement, and high-impact activities. Such refinements are essential for ensuring the models’ reliability in real-world applications, particularly in clinical and biomechanical research contexts, where accurate assessments of mechanical loading are critical for designing rehabilitation programs, injury prevention strategies, and optimizing bone health interventions. Full article
(This article belongs to the Section Mechanical Engineering)
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<p>Bland–Altman plots displaying the level of agreement between actual and predicted pGRF for accelerometers worn at the ankle (panels <b>A</b>,<b>D</b>), lower back (panels <b>B</b>,<b>E</b>), and hip (panels <b>C</b>,<b>F</b>). These plots cover both the resultant vector (panels <b>A</b>–<b>C</b>) and its vertical component (panels <b>D</b>–<b>F</b>). Predictions of pGRF during walking and running were calculated using the equations from Veras et al. (2022) [<a href="#B20-applsci-14-10292" class="html-bibr">20</a>]. The solid lines represent the bias (the mean difference between actual and predicted values), while the dashed lines mark the limits of agreement (bias ±1.96 standard deviations). Abbreviations: pGRF, peak ground reaction force.</p>
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<p>Bland–Altman plots displaying the level of agreement between actual and predicted pL for accelerometers worn at the ankle (panels <b>A</b>,<b>D</b>), lower back (panels <b>B</b>,<b>E</b>), and hip (panels <b>C</b>,<b>F</b>). These plots cover both the resultant vector (panels <b>A</b>–<b>C</b>) and its vertical component (panels <b>D</b>–<b>F</b>). Predictions of pLR during walking and running were calculated using the equations from Veras et al. (2022) [<a href="#B20-applsci-14-10292" class="html-bibr">20</a>]. The solid lines represent the bias (the mean difference between actual and predicted values), while the dashed lines mark the limits of agreement (bias ±1.96 standard deviations). Abbreviations: pLR, peak loading rate.</p>
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<p>Bland–Altman plot displaying the level agreement between actual and predicted pGRF for accelerometers worn at the hip for the vertical vector. Predictions of pGRF during walking and running were calculated using the equation from Neugebauer et al. (2014) [<a href="#B17-applsci-14-10292" class="html-bibr">17</a>]. The solid line represents the bias (the mean difference between actual and predicted values), while the dashed lines mark the limits of agreement (bias ±1.96 standard deviations). Abbreviations: pGRF, peak ground reaction force.</p>
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<p>Bland–Altman plots displaying the level of agreement between actual and predicted pGRF for accelerometers worn at the ankle (panels <b>A</b>,<b>D</b>), lower back (panels <b>B</b>,<b>E</b>), and hip (panels <b>C</b>,<b>F</b>). These plots cover both the resultant vector (panels <b>A</b>–<b>C</b>) and its vertical component (panels <b>D</b>–<b>F</b>). Predictions of pGRF during jumping were calculated using the equations from Veras et al. (2023) [<a href="#B21-applsci-14-10292" class="html-bibr">21</a>]. The solid lines represent the bias (the mean difference between actual and predicted values), while the dashed lines mark the limits of agreement (bias ±1.96 standard deviations). Abbreviations: pGRF, peak ground reaction force.</p>
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<p>Bland–Altman plots displaying the level of agreement between actual and predicted pL for accelerometers worn at the ankle (panels <b>A</b>,<b>D</b>), lower back (panels <b>B</b>,<b>E</b>), and hip (panels <b>C</b>,<b>F</b>). These plots cover both the resultant vector (panels <b>A</b>–<b>C</b>) and its vertical component (panels <b>D</b>–<b>F</b>). Predictions of pLR during jumping were calculated using the equations from Veras et al. (2023) [<a href="#B21-applsci-14-10292" class="html-bibr">21</a>]. The solid lines represent the bias (the mean difference between actual and predicted values), while the dashed lines mark the limits of agreement (bias ±1.96 standard deviations). Abbreviations: pLR, peak loading rate.</p>
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24 pages, 5699 KiB  
Article
Synthetic Wind Estimation for Small Fixed-Wing Drones
by Aman Sharma, Gabriel François Laupré, Pasquale Longobardi and Jan Skaloud
Atmosphere 2024, 15(11), 1339; https://doi.org/10.3390/atmos15111339 - 8 Nov 2024
Viewed by 422
Abstract
Wind estimation is crucial for studying the atmospheric boundary layer. Traditional methods such as weather balloons offer limited in situ capabilities; besides an Air Data System (ADS) combined with inertial measurements and satellite positioning is required to estimate the wind on fixed-wing drones. [...] Read more.
Wind estimation is crucial for studying the atmospheric boundary layer. Traditional methods such as weather balloons offer limited in situ capabilities; besides an Air Data System (ADS) combined with inertial measurements and satellite positioning is required to estimate the wind on fixed-wing drones. As pressure probes are an important constituent of an ADS, they are susceptible to malfunctioning or failure due to blockages, thus affecting the capability of wind sensing and possibly the safety of the drone. This paper presents a novel approach, using low-fidelity aerodynamic models of drones to estimate wind synthetically. In our work, the aerodynamic model parameters are derived from post-processed flight data, in contrast to existing approaches that use expensive wind tunnel calibration for identifying the same. In sum, our method integrates aerodynamic force and moment models into a Vehicle Dynamic Model (VDM)-based navigation filter to yield a synthetic wind estimate without relying on an airspeed sensor. We validate our approach using two geometrically distinct drones, each characterized by a unique aerodynamic model and different quality of inertial sensors, altogether tested across several flights. Experimental results demonstrate that the proposed cross-platform method provides a synthetic wind velocity estimate, thus offering a practical backup to traditional techniques. Full article
(This article belongs to the Section Atmospheric Techniques, Instruments, and Modeling)
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<p>VDM-based navigation system. Image courtesy: Ref. [<a href="#B71-atmosphere-15-01339" class="html-bibr">71</a>].</p>
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<p>Aerodynamic calibration procedure. Image courtesy: Ref. [<a href="#B4-atmosphere-15-01339" class="html-bibr">4</a>].</p>
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<p>TP2 payload: (<b>left</b>) CAD model; (<b>right</b>) practical realization.</p>
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<p>Drones: (<b>top</b>) <span class="html-italic">TP2</span>; (<b>bottom</b>) <span class="html-italic">Concorde S</span>.</p>
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<p>Comparison of wind estimated by VDM and INS/GNSS/Pitot fusion for <span class="html-italic">TP-2</span>.</p>
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<p>Comparison of wind estimated by VDM and INS/GNSS/Pitot fusion for <span class="html-italic">TP-2</span>.</p>
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<p>Wind residual between VDM and INS/GNSS/Pitot fusion for <span class="html-italic">TP-2</span>.</p>
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<p>Zoomed-in view of the residual error.</p>
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<p>Comparison of wind estimated by VDM and INS/GNSS/Pitot fusion for <span class="html-italic">Concorde S</span>.</p>
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<p>Wind residual between VDM and INS/GNSS/Pitot fusion for <span class="html-italic">Concorde S</span>.</p>
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<p>Wind estimated using incorrect VDM parameters for <span class="html-italic">TP2</span>—STIM13.</p>
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<p>eBeeX drone.</p>
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<p>Wind estimated by eBeex.</p>
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14 pages, 4579 KiB  
Article
Development and Evaluation of Thread Transistor Based on Carbon-Nanotube Composite Thread with Ionic Gel and Its Application to Logic Gates
by Hiroki Kodaira and Takahide Oya
J. Compos. Sci. 2024, 8(11), 463; https://doi.org/10.3390/jcs8110463 - 8 Nov 2024
Viewed by 398
Abstract
We propose a new type of flexible transistor based on carbon-nanotube (CNT) composite thread (CNTCT), i.e., a thread transistor, with ionic gel. In our previous study, we demonstrated that transistor operation was possible by combining metallic and semiconducting CNTCTs as gate and channel [...] Read more.
We propose a new type of flexible transistor based on carbon-nanotube (CNT) composite thread (CNTCT), i.e., a thread transistor, with ionic gel. In our previous study, we demonstrated that transistor operation was possible by combining metallic and semiconducting CNTCTs as gate and channel with an insulating material. However, its performance was not sufficient. Therefore, we here aim to improve it. For this, we tried to apply ionic gel as a dielectric layer to it. With this, the transistor was expected to be an electric-double-layer transistor. The transistor performance was improved, and the on/off ratio of the transistor increased by more than 4. This is a large value compared to our previous work. In addition, we not only evaluated the performance of the transistors, but also investigated whether they could be used as logic circuits. It was confirmed that the logic circuit composed of the thread transistor also operated correctly and stably for a long period of time. It was also confirmed that the output changed in response to weak external forces. These results indicate that it is a flexible transistor that can be used in a wide range of applications such as logic circuits and sensors. Full article
(This article belongs to the Special Issue Recent Progress in Hybrid Composites)
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<p>Structure of proposed thread transistor.</p>
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<p>Behavior of charge in extracted three layers from gate electrode to channel parts of proposed thread transistor. (<b>a</b>) Before applying gate voltage, ions are in random position. (<b>b</b>) When gate voltage is applied, ions begin to move to electrodes. (<b>c</b>) After applying gate voltage, ions align near the electrodes to form EDL.</p>
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<p>Proposed thread transistor is fabricated by combining the above materials.</p>
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<p>Schematic of method for making CNT composite thread.</p>
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<p>Schematic of method for making ionic gel.</p>
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<p>Prepared thread transistor and details of its structure.</p>
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<p>Ratio of resistance change of CNT composite thread under applied tension. (<b>a</b>) Tension was continuously applied from 0 N to 2.0 N. (<b>b</b>) Tension was applied from 0 N to 0.2 N and the released. (<b>c</b>) Operation (<b>b</b>) was repeated five times.</p>
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<p>Transfer and I-V curve of thread transistor.</p>
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<p>Measurement of NOT circuit using thread transistor. (<b>a</b>) Schematic of <span class="html-italic">p</span>-type NOT circuit with thread transistor, (<b>b</b>) observed operation of constructed NOT circuit, (<b>c</b>) repeatability of operation, and (<b>d</b>) comparison of output amplitude at different frequencies. In (<b>c</b>), the time axis is partially enlarged by about one cycle just after 1000 and 9000 s to check the operation. In (<b>d</b>), the horizontal axis is set to one cycle to make it easier to compare the differences in amplitude.</p>
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<p>(<b>a</b>) Photograph of thread transistor fixed for evaluation of response to bending, (<b>b</b>) change in drain current when bending in channel direction, and (<b>c</b>) when bending in gate direction.</p>
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<p>Photographs of thread transistor fixed on breadboard to evaluate response to tension for (<b>a</b>) channel direction described as red-colored arrow and (<b>b</b>) gate direction described as red-colored arrow. Measured responses obtained from (<b>c</b>) transistor described in <a href="#jcs-08-00463-f011" class="html-fig">Figure 11</a>(a), and (<b>d</b>) in <a href="#jcs-08-00463-f011" class="html-fig">Figure 11</a>(b).</p>
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