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13 pages, 4058 KiB  
Article
Development of a Cable-Driven Bionic Spherical Joint for a Robot Wrist
by Zixun He, Yutaka Ito, Shotaro Saito, Sakura Narumi, Yousun Kang and Duk Shin
Biomimetics 2025, 10(1), 52; https://doi.org/10.3390/biomimetics10010052 (registering DOI) - 14 Jan 2025
Abstract
Wrist movements play a crucial role in upper-limb motor tasks. As prosthetic and robotic hand technologies have evolved, increasing attention has been focused on replicating the anatomy and functionality of the wrist. Closely imitating the biomechanics and movement mechanisms of human limbs is [...] Read more.
Wrist movements play a crucial role in upper-limb motor tasks. As prosthetic and robotic hand technologies have evolved, increasing attention has been focused on replicating the anatomy and functionality of the wrist. Closely imitating the biomechanics and movement mechanisms of human limbs is expected to enhance the overall performance of bionic robotic hands. This study presents the design of a tendon-driven bionic spherical robot wrist, utilizing two pairs of cables that mimic antagonist muscle pairs. The cables are actuated by pulleys driven by servo motors, allowing for two primary wrist motions: flexion–extension and ulnar–radial deviation. The performance Please confirm if the “1583 Iiyama” is necessary. Same as belowof the proposed robot wrist is validated through manipulation experiments using a prototype, demonstrating its capability to achieve a full range of motion for both ulnar and radial deviation. This wrist mechanism is expected to be integrated into robotic systems, enabling greater flexibility and more human-like movement capabilities. Full article
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Figure 1

Figure 1
<p>(<b>a</b>) The eight carpal bones of the wrist. H: hamate; C: capitate; Td: trapezoid; T: trapezium; P: pisiform; Q: triquetrum; L: lunate; and S: scaphoid. (<b>b</b>) The three types of rotational movements of the wrist and the range of movement.</p>
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<p>(<b>a</b>) Prototype of robot wrist using 3D printing; (<b>b</b>,<b>c</b>) CAD model of carpal bones and hand.</p>
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<p>(<b>a</b>) The robot wrist was split into two parts and assembled with the spherical joint after the 3D printing of these two parts. (<b>b</b>) CAD model of the socket joint.</p>
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<p>(<b>a</b>) Kinematic analysis of the proposed robot wrist mechanism. (<b>b</b>) The motion of the wrist joint, represented as rotations of <math display="inline"><semantics> <mrow> <mi>α</mi> <mo>,</mo> <mi>β</mi> <mo>,</mo> <mi>γ</mi> </mrow> </semantics></math> degrees along the <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>X</mi> </mrow> <mrow> <mi>w</mi> </mrow> </msub> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Y</mi> </mrow> <mrow> <mi>w</mi> </mrow> </msub> </mrow> </semantics></math>, and <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Z</mi> </mrow> <mrow> <mi>w</mi> </mrow> </msub> </mrow> </semantics></math> axes, respectively.</p>
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<p>Experimental setup of the robot wrist.</p>
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<p>Measured angle data of three dimensions of FE movement. Angle from <math display="inline"><semantics> <mrow> <mn>0</mn> <mo>°</mo> </mrow> </semantics></math> to <math display="inline"><semantics> <mrow> <mn>45</mn> <mo>°</mo> </mrow> </semantics></math> correspond to the flexion of the wrist, and those from <math display="inline"><semantics> <mrow> <mn>0</mn> <mo>°</mo> </mrow> </semantics></math> to <math display="inline"><semantics> <mrow> <mo>−</mo> <mn>45</mn> <mo>°</mo> </mrow> </semantics></math> correspond to the extension of the wrist.</p>
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<p>Measured angle data of three dimensions of UR movement. Angles from <math display="inline"><semantics> <mrow> <mn>0</mn> <mo>°</mo> </mrow> </semantics></math> to <math display="inline"><semantics> <mrow> <mn>20</mn> <mo>°</mo> </mrow> </semantics></math> correspond to the ulnar deviation of the wrist, and those from <math display="inline"><semantics> <mrow> <mn>0</mn> <mo>°</mo> </mrow> </semantics></math> to <math display="inline"><semantics> <mrow> <mo>−</mo> <mn>20</mn> <mo>°</mo> </mrow> </semantics></math> correspond to the radial deviation of the wrist.</p>
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<p>Measured angle data of rotation movements.</p>
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15 pages, 6878 KiB  
Article
Finite Element Analysis of Electromagnetic Characteristics of a Single-Phase Permanent Magnet Linear Oscillation Actuator
by Hongbin Zhang, Zhaoxin Wang, Minshuo Chen, Zhan Shen, Haitao Yu and Zhike Xu
Sensors 2025, 25(2), 452; https://doi.org/10.3390/s25020452 - 14 Jan 2025
Abstract
The electromagnetic characteristics of a single-phase permanent magnet linear oscillation actuator are analyzed by the finite element method. Firstly, the basic structure and operation principle of the linear oscillation actuator are introduced. The internal stator slot and arc tooth are used to reduce [...] Read more.
The electromagnetic characteristics of a single-phase permanent magnet linear oscillation actuator are analyzed by the finite element method. Firstly, the basic structure and operation principle of the linear oscillation actuator are introduced. The internal stator slot and arc tooth are used to reduce the detent force. According to the principle of electromagnetic fields, the electromagnetic field equation is listed and the function of the motor is deduced. At the same time, the eight-node hexahedral element is used to calculate the listed universal functions, and the inductance, flux linkage, induced electromotive force and electromagnetic force of the motor are deduced. The electromagnetic field of the motor is simulated by two-dimensional and three-dimensional finite element methods, and the accuracy of the calculation results of the electromagnetic characteristics of the cylindrical linear oscillation motor by the two methods is compared and analyzed. Finally, an experimental prototype was developed and the no-load characteristics of the motor were tested using the existing linear motor towing method. By comparing the experimental and simulation results, the accuracy of the theoretical analysis and the rationality of the motor design are verified. Full article
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Figure 1

Figure 1
<p>Structures of the two SPMLOAs: (<b>a</b>) traditional LOA; (<b>b</b>) novel LOA.</p>
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<p>Hexahedral isoperimetric element.</p>
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<p>Finite element models of the novel SPMLOA: (<b>a</b>) 2-D; (<b>b</b>) 3-D.</p>
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<p>Magnetic field distribution of the SPMLOA at maximum displacement: (<b>a</b>) 2-D magnetic field density; (<b>b</b>) 2-D magnetic circuit; (<b>c</b>) 3-D magnetic field density; (<b>d</b>) 3-D magnetic field density.</p>
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<p>Flux linkage waveform of open-circuit.</p>
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<p>Back EMF waveform of open-circuit.</p>
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<p>Comparison of detent forces.</p>
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<p>Assembly process of the prototype: (<b>a</b>) outer stator tooth silicon steel sheet; (<b>b</b>) s winding coil; (<b>c</b>) mover with PMs; (<b>d</b>) overall structure of the LOA.</p>
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<p>Test platform of the proposed novel SPMOA.</p>
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<p>Comparison results of testing and 3-D simulation of detent force waveform under no-load conditions.</p>
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<p>Comparison results of testing and 3-D simulation of back electromotive force waveform under no-load conditions.</p>
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<p>Relationship between displacement current ratio and frequency under no-load state.</p>
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<p>Efficiency waveform of the prototype at different frequencies.</p>
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18 pages, 1464 KiB  
Article
Static Output-Feedback Path-Tracking Controller Tolerant to Steering Actuator Faults for Distributed Driven Electric Vehicles
by Miguel Meléndez-Useros, Fernando Viadero-Monasterio, Manuel Jiménez-Salas and María Jesús López-Boada
World Electr. Veh. J. 2025, 16(1), 40; https://doi.org/10.3390/wevj16010040 - 14 Jan 2025
Viewed by 95
Abstract
The steering system plays a critical role in the vehicle’s handling and directly influences its lateral dynamics. Faults or abnormal behavior in this system can affect performance, cause vehicle instability, and even lead to accidents. Therefore, considering these potential events is essential for [...] Read more.
The steering system plays a critical role in the vehicle’s handling and directly influences its lateral dynamics. Faults or abnormal behavior in this system can affect performance, cause vehicle instability, and even lead to accidents. Therefore, considering these potential events is essential for designing robust controllers for autonomous vehicles. For this reason, in this work, a fault-tolerant path-tracking Static Output-Feedback controller is designed to handle steering actuator faults in autonomous vehicle steering systems. The controller adopts a Linear Parameter Varying approach to effectively handle nonlinearities associated with varying vehicle speeds and tire behavior. Furthermore, it only uses information from sensors, avoiding estimation stages. This controller can operate in two modes: a no-fault mode where only the steering is controlled to follow the reference path and a fault mode where the controller manages both the steering and torque vectoring. In fault mode, torque vectoring compensates for faults in the steering actuator. The design of the controller is completed considering gain faults in the steering system. The simulation results show that the proposed controller successfully maintains vehicle stability and significantly reduces tracking errors during high-risk maneuvers, achieving reductions of up to 50.65% in lateral error and 47.26% in heading error under worst-case fault scenarios. Full article
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Figure 1
<p>Cornering stiffnesses limits for tire lateral force.</p>
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<p>Vehicle path-tracking model.</p>
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<p>Control scheme of the proposed fault-tolerant controller.</p>
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<p>Lateral error for Case A.</p>
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<p>Heading error for Case A.</p>
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<p>Control inputs for Case A. (<b>a</b>) Front steering angle. (<b>b</b>) In-wheel motor torque when <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.3</mn> </mrow> </semantics></math>.</p>
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<p>Path for Case A.</p>
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<p>Lateral error for Case B.</p>
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<p>Heading error for Case B.</p>
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<p>Control inputs for Case B. (<b>a</b>) Front steering angle. (<b>b</b>) In-wheel motor torque for <math display="inline"><semantics> <mrow> <mrow> <mo>|</mo> </mrow> <msub> <mi>δ</mi> <mrow> <mi>m</mi> <mi>a</mi> <mi>x</mi> </mrow> </msub> <mrow> <mo>|</mo> <mo>=</mo> </mrow> <msup> <mn>3</mn> <mo>∘</mo> </msup> </mrow> </semantics></math>.</p>
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<p>Path for Case B.</p>
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22 pages, 6604 KiB  
Review
Application of Soft Grippers in the Field of Agricultural Harvesting: A Review
by Daode Zhang, Wei Zhang, Hualin Yang and Haibing Yang
Machines 2025, 13(1), 55; https://doi.org/10.3390/machines13010055 - 14 Jan 2025
Viewed by 137
Abstract
This review summarizes the important properties required for applying soft grippers to agricultural harvesting, focusing on their actuation methods and structural types. The purpose of the review is to address the challenges of limited load capacity and stiffness, which significantly hinder the broader [...] Read more.
This review summarizes the important properties required for applying soft grippers to agricultural harvesting, focusing on their actuation methods and structural types. The purpose of the review is to address the challenges of limited load capacity and stiffness, which significantly hinder the broader application of soft grippers in agriculture. This paper examines the research progress on variable stiffness methods for soft grippers over the past five years. We categorize various variable stiffness techniques and analyze their advantages and disadvantages in enhancing load capacity, stiffness, dexterity, degree of integration, responsiveness, and energy consumption of soft grippers. The applicability and limitations of these techniques in the context of agricultural harvesting are also discussed. This paper concludes that combined material variable stiffness technology with a motor actuation claw structure in soft grippers is better suited for agricultural harvesting operations of woody crops (e.g., apples, citrus) and herbaceous crops (e.g., tomatoes, cucumbers) in unstructured environments. Full article
(This article belongs to the Section Robotics, Mechatronics and Intelligent Machines)
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Figure 1
<p>Summary of classification methods of soft grippers.</p>
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<p>Pneumatic soft gripper with claw structure for use in agricultural harvesting. (<b>a</b>) The three-finger pneumatic soft gripper. (<b>b</b>) Demonstration of different gripping and picking strategies for apples. (<b>c</b>) The soft gripper with gripping and adsorption. (<b>d</b>) The soft gripper based on collective mechanics. Figure taken from [<a href="#B12-machines-13-00055" class="html-bibr">12</a>,<a href="#B26-machines-13-00055" class="html-bibr">26</a>,<a href="#B27-machines-13-00055" class="html-bibr">27</a>,<a href="#B28-machines-13-00055" class="html-bibr">28</a>].</p>
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<p>Motor actuation soft grippers with claw structure for use in agricultural harvesting. (<b>a</b>) The three-finger Fin-Ray structure soft gripper. (<b>b</b>) The four-finger and six-finger Fin-Ray structure soft grippers. (<b>c</b>) The two-finger Fin-Ray structure soft gripper. Figure taken from [<a href="#B31-machines-13-00055" class="html-bibr">31</a>,<a href="#B32-machines-13-00055" class="html-bibr">32</a>,<a href="#B33-machines-13-00055" class="html-bibr">33</a>].</p>
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<p>Tendon actuation soft gripper with claw structure for use in agricultural harvesting. (<b>a</b>) The three-finger tendon actuation soft gripper. (<b>b</b>) The soft gripper made of steel wire and silicone material. (<b>c</b>) The soft grippers powered by tendon made of 3D printed materials. Figure taken from [<a href="#B37-machines-13-00055" class="html-bibr">37</a>,<a href="#B38-machines-13-00055" class="html-bibr">38</a>,<a href="#B39-machines-13-00055" class="html-bibr">39</a>].</p>
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<p>Closed structure friction gripping soft grippers. (<b>a</b>) The bionic eel pneumatic soft gripper. (<b>b</b>) The soft gripper with friction gripping. (<b>c</b>) The bionic winding soft gripper. (<b>d</b>) The hybrid gripping soft gripper with suction and friction gripping. Figure taken from [<a href="#B55-machines-13-00055" class="html-bibr">55</a>,<a href="#B56-machines-13-00055" class="html-bibr">56</a>,<a href="#B57-machines-13-00055" class="html-bibr">57</a>,<a href="#B58-machines-13-00055" class="html-bibr">58</a>].</p>
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<p>Soft gripper of the suction gripping type. (<b>a</b>) The suction gripping structure of soft gripper for apple picking. (<b>b</b>) The closed soft gripper with variable stiffness via particle obstruction. (<b>c</b>) The suction gripping structure of soft gripper for cucumber picking. Figure taken from [<a href="#B59-machines-13-00055" class="html-bibr">59</a>,<a href="#B60-machines-13-00055" class="html-bibr">60</a>,<a href="#B61-machines-13-00055" class="html-bibr">61</a>].</p>
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<p>Performance requirements for soft grippers applied to agricultural harvesting.</p>
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<p>Summary of load capacity of soft grippers with different structural forms.</p>
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<p>Structural design of clawed soft grippers for agricultural harvesting operations. Figure taken from. (<b>a</b>) The pneumatic three-finger soft gripper. (<b>b</b>) The pneumatic three-finger soft gripper with improved obstruction variable stiffness. (<b>c</b>) The pneumatic five-finger soft gripper. (<b>d</b>) The three-finger gripper. (<b>e</b>) The four-finger soft gripper. (<b>f</b>) The high-load three-finger soft gripper. (<b>g</b>) The one-finger soft gripper. (<b>h</b>) The pneumatic three-finger soft gripper. (<b>i</b>) The three-finger soft gripper. (<b>j</b>) The four-finger soft gripper. (<b>k</b>) The pneumatic four-finger soft gripper. (<b>l</b>) The tendon-actuated three-finger soft gripper. (<b>m</b>) The soft gripper with improved combined material variable stiffness. (<b>n</b>) The four-finger soft gripper. (<b>o</b>) The three-finger soft gripper. (<b>p</b>) The two-finger soft gripper. (<b>q</b>) The two-finger soft gripper. (<b>r</b>) The pneumatic three-finger soft gripper. (<b>s</b>) The two-finger soft gripper with improved antagonistic variable stiffness [<a href="#B74-machines-13-00055" class="html-bibr">74</a>,<a href="#B75-machines-13-00055" class="html-bibr">75</a>,<a href="#B76-machines-13-00055" class="html-bibr">76</a>,<a href="#B77-machines-13-00055" class="html-bibr">77</a>,<a href="#B78-machines-13-00055" class="html-bibr">78</a>,<a href="#B79-machines-13-00055" class="html-bibr">79</a>,<a href="#B80-machines-13-00055" class="html-bibr">80</a>,<a href="#B81-machines-13-00055" class="html-bibr">81</a>,<a href="#B82-machines-13-00055" class="html-bibr">82</a>,<a href="#B83-machines-13-00055" class="html-bibr">83</a>,<a href="#B84-machines-13-00055" class="html-bibr">84</a>,<a href="#B85-machines-13-00055" class="html-bibr">85</a>,<a href="#B86-machines-13-00055" class="html-bibr">86</a>,<a href="#B87-machines-13-00055" class="html-bibr">87</a>,<a href="#B88-machines-13-00055" class="html-bibr">88</a>,<a href="#B89-machines-13-00055" class="html-bibr">89</a>,<a href="#B90-machines-13-00055" class="html-bibr">90</a>,<a href="#B91-machines-13-00055" class="html-bibr">91</a>,<a href="#B92-machines-13-00055" class="html-bibr">92</a>].</p>
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<p>Structural design of closed soft grippers for agricultural harvesting operations. (<b>a</b>) The experiment of closed soft gripper gripping shaped object. (<b>b</b>) The closed soft gripper with four air chambers control. (<b>c</b>) The closed soft gripper with improved obstruction variable stiffness. (<b>d</b>) The dielectric elastomer-actuated closed soft gripper. (<b>e</b>) The closed soft gripper gripping experiment for a plastic drum. (<b>f</b>) The closed soft gripper. (<b>g</b>) The closed soft gripper gripping experiment for a light. (<b>h</b>) The fluid-obstructed stiffness soft gripper. (<b>i</b>) The particle obstruction variable stiffness closed soft gripper. (<b>j</b>) The experiments on fruit grasping by a closed soft gripper. (<b>k</b>) The closed soft gripper for apple picking. Figure taken from [<a href="#B93-machines-13-00055" class="html-bibr">93</a>,<a href="#B94-machines-13-00055" class="html-bibr">94</a>,<a href="#B95-machines-13-00055" class="html-bibr">95</a>,<a href="#B96-machines-13-00055" class="html-bibr">96</a>,<a href="#B97-machines-13-00055" class="html-bibr">97</a>,<a href="#B98-machines-13-00055" class="html-bibr">98</a>,<a href="#B99-machines-13-00055" class="html-bibr">99</a>,<a href="#B100-machines-13-00055" class="html-bibr">100</a>,<a href="#B101-machines-13-00055" class="html-bibr">101</a>].</p>
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<p>Summary of variable stiffness methods for soft grippers.</p>
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<p>Application of thermal, magnetic, and electrically induced variable stiffness technology. (<b>a</b>) Bending stiffness of the soft gripper under cooling and heating conditions. (<b>b</b>) EPMs demonstration of the soft gripper load capacity under energized and unenergized conditions. (<b>c</b>) Stiffness of the soft gripper filled with ER fluid at different voltages. Figure taken from [<a href="#B106-machines-13-00055" class="html-bibr">106</a>,<a href="#B107-machines-13-00055" class="html-bibr">107</a>,<a href="#B108-machines-13-00055" class="html-bibr">108</a>].</p>
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<p>Application of antagonistic variable stiffness technology. (<b>a</b>) Triple air cavity antagonist actuation. (<b>b</b>) Tendon and air cavity antagonistic actuation. Figure taken from [<a href="#B109-machines-13-00055" class="html-bibr">109</a>,<a href="#B110-machines-13-00055" class="html-bibr">110</a>].</p>
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<p>Application of obstruction variable stiffness in soft grippers. (<b>a</b>) Structural diagram of the soft gripper with variable stiffness of fluid obstructed. (<b>b</b>) Real-time control method for variable stiffness of particle obstruction. Figure taken from [<a href="#B87-machines-13-00055" class="html-bibr">87</a>,<a href="#B111-machines-13-00055" class="html-bibr">111</a>].</p>
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<p>Application of combined material variable stiffness in the soft gripper. Figure taken from [<a href="#B75-machines-13-00055" class="html-bibr">75</a>].</p>
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<p>Summary of advantages and disadvantages of different soft gripper variable stiffness techniques.</p>
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18 pages, 7819 KiB  
Review
Low-Power Wake-Up Receivers for Resilient Cellular Internet of Things
by Siyu Wang, Trevor J. Odelberg, Peter W. Crary, Mason P. Obery and David D. Wentzloff
Information 2025, 16(1), 43; https://doi.org/10.3390/info16010043 - 13 Jan 2025
Viewed by 218
Abstract
Smart Cities leverage large networks of wirelessly connected nodes embedded with sensors and/or actuators. Cellular IoT, such as NB-IoT and 5G RedCap, is often preferred for these applications thanks to its long range, extensive coverage, and good quality of service. In these networks, [...] Read more.
Smart Cities leverage large networks of wirelessly connected nodes embedded with sensors and/or actuators. Cellular IoT, such as NB-IoT and 5G RedCap, is often preferred for these applications thanks to its long range, extensive coverage, and good quality of service. In these networks, wireless communication dominates power consumption, motivating research on energy-efficient yet resilient and robust wireless systems. Many IoT use cases require low latency but cannot afford high-power radios continuously operating to accomplish this. In these cases, wake-up receivers (WURs) are a promising solution: while the high-power main radio (MR) is turned off/idle, a lightweight WUR is continuously monitoring the RF channel; when it detects a wake-up sequence, the WUR will turn on the MR for subsequent communications. This article provides an overview of WUR hardware design considerations and challenges for 4G and 5G cellular IoT, summarizes the recent 3GPP activities to standardize NB-IoT and 5G wake-up signals, and presents a state-of-the-art WUR chip. Full article
(This article belongs to the Special Issue IoT-Based Systems for Resilient Smart Cities)
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Graphical abstract

Graphical abstract
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<p>Evolution of cellular device power-saving mechanisms (adapted from [<a href="#B6-information-16-00043" class="html-bibr">6</a>]).</p>
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<p>Side-by-side comparison of a traditional eDRX node vs. a node with a WUR. (<b>a</b>) Traditional IoT node structure and power consumption model in eDRX mode. (<b>b</b>) IoT node equipped with WUR and its power consumption model (assuming a duty-cycled WUR).</p>
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<p>Illustration of 4G and 5G device types (adapted from [<a href="#B14-information-16-00043" class="html-bibr">14</a>]).</p>
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<p>Power vs. sensitivity [<a href="#B15-information-16-00043" class="html-bibr">15</a>].</p>
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<p>Power vs. SIR (only 79 out of 228 ULP RXs reported SIR) [<a href="#B15-information-16-00043" class="html-bibr">15</a>].</p>
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<p>LTE/NB-IoT resource grid, frame structure, and resource block.</p>
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<p>NWUS physical structure.</p>
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<p>Frequency-domain allocation, assuming a 20 MHz channel BW and a 4.32 MHz LP-WUS BW.</p>
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<p>(<b>a</b>) Waveform generation at 5G gNB using the OOK-1 method; (<b>b</b>) the resulting WUS carries 1 information bit (wake up or not) per OFDM symbol.</p>
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<p>(<b>a</b>) Waveform generation at 5G gNB using the OOK-4 method; (<b>b</b>) the resulting time-domain WUS waveform and channel frequency allocation. With OOK-4, each OFDM symbol contains multiple (M) chips.</p>
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<p>Block diagram for baseband processing of LP-SS signal.</p>
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<p>Architecture of a conventional heterodyne receiver.</p>
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<p>Architecture of an ED-first ULP receiver.</p>
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<p>Architecture of a passive mixer-first ULP receiver.</p>
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<p>Architecture of an LNA-first ULP receiver.</p>
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<p>Block diagram of fabricated WUR with integrated digital backend.</p>
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<p>The optimized 12-point FFT. Through exploiting even–odd symmetry and inverting operations, the number of multipliers can be reduced.</p>
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<p>Power breakdown of the NB-IoT WUR.</p>
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<p>Test setup (<b>left</b>) and measured wake-up event (<b>right</b>).</p>
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<p>Power vs. sensitivity performance of the presented NB-IoT WUR (starred) compared to other receivers supporting coherent modulation schemes (blue dots).</p>
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20 pages, 3827 KiB  
Review
Two-Dimensional Ferroelectric Materials: From Prediction to Applications
by Shujuan Jiang, Yongwei Wang and Guangping Zheng
Nanomaterials 2025, 15(2), 109; https://doi.org/10.3390/nano15020109 - 12 Jan 2025
Viewed by 347
Abstract
Ferroelectric materials hold immense potential for diverse applications in sensors, actuators, memory storage, and microelectronics. The discovery of two-dimensional (2D) ferroelectrics, particularly ultrathin compounds with stable crystal structure and room-temperature ferroelectricity, has led to significant advancements in the field. However, challenges such as [...] Read more.
Ferroelectric materials hold immense potential for diverse applications in sensors, actuators, memory storage, and microelectronics. The discovery of two-dimensional (2D) ferroelectrics, particularly ultrathin compounds with stable crystal structure and room-temperature ferroelectricity, has led to significant advancements in the field. However, challenges such as depolarization effects, low Curie temperature, and high energy barriers for polarization reversal remain in the development of 2D ferroelectrics with high performance. In this review, recent progress in the discovery and design of 2D ferroelectric materials is discussed, focusing on their properties, underlying mechanisms, and applications. Based on the work discussed in this review, we look ahead to theoretical prediction for 2D ferroelectric materials and their potential applications, such as the application in nonlinear optics. The progress in theoretical and experimental research could lead to the discovery and design of next-generation nanoelectronic and optoelectronic devices, facilitating the applications of 2D ferroelectric materials in emerging advanced technologies. Full article
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<p>(<b>a</b>) Top view and (<b>b</b>) side view of the CuInP<sub>2</sub>S<sub>6</sub> monolayer [<a href="#B29-nanomaterials-15-00109" class="html-bibr">29</a>]. (<b>c</b>) The PFM phase images for the 4 nm-thick CIPS flakes with reversed DC bias [<a href="#B28-nanomaterials-15-00109" class="html-bibr">28</a>]. (<b>d</b>) The corresponding PFM amplitude (black) and phase (blue) hysteresis loops during the switching process for the 4 nm-thick CIPS flakes [<a href="#B28-nanomaterials-15-00109" class="html-bibr">28</a>]. (<b>e</b>) Energetics of the CuInP<sub>2</sub>Se<sub>6</sub> monolayer and bulk sample as determined by first-principles nudged elastic band (NEB) calculations, revealing the FE(AFE)–to–paraelectric phase transitions [<a href="#B29-nanomaterials-15-00109" class="html-bibr">29</a>]. (<b>f</b>) Energy variation with aspect to the applied electric field <span class="html-italic">D</span>/<span class="html-italic">ε</span><sub>0</sub> [<a href="#B29-nanomaterials-15-00109" class="html-bibr">29</a>]. (<b>g</b>) Temperature-dependent zero-field spontaneous polarization <span class="html-italic">P</span><sub><span class="html-italic">s</span></sub> in monolayer and bulk CuInP<sub>2</sub>Se<sub>6</sub> [<a href="#B29-nanomaterials-15-00109" class="html-bibr">29</a>]. Reprinted with permission from [<a href="#B29-nanomaterials-15-00109" class="html-bibr">29</a>], 2017, American Physical Society; and [<a href="#B28-nanomaterials-15-00109" class="html-bibr">28</a>], 2016, Springer Nature.</p>
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<p>(<b>a</b>) Schematic diagram of MoS<sub>2</sub>/CIPS 2D FE-FETs [<a href="#B36-nanomaterials-15-00109" class="html-bibr">36</a>]. (<b>b</b>) Polarization–voltage loop for FE capacitor at 290 K [<a href="#B36-nanomaterials-15-00109" class="html-bibr">36</a>]. (<b>c</b>) Schematic of Cr/CIPS/graphene FTJ on the SiO<sub>2</sub>/Si substrate [<a href="#B37-nanomaterials-15-00109" class="html-bibr">37</a>]. (<b>d</b>) Band diagrams for the on- and off-states of the vdW FTJ operation [<a href="#B37-nanomaterials-15-00109" class="html-bibr">37</a>]. The built-in polarization fields are indicated by cyan arrows. Reprinted with permission from [<a href="#B36-nanomaterials-15-00109" class="html-bibr">36</a>], 2018, American Chemical Society; and [<a href="#B37-nanomaterials-15-00109" class="html-bibr">37</a>], 2020, Springer Nature.</p>
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<p>(<b>a</b>) Trimerization of Mo atoms in the 1T crystal structure with a <math display="inline"><semantics> <mrow> <mo>√</mo> <mn>3</mn> <mo>×</mo> <mo>√</mo> <mn>3</mn> </mrow> </semantics></math> unit cell [<a href="#B41-nanomaterials-15-00109" class="html-bibr">41</a>]. (<b>b</b>) Polarization (P) and dielectric susceptibility (χ) as a function of temperature derived from Landau theory [<a href="#B41-nanomaterials-15-00109" class="html-bibr">41</a>]. (<b>c</b>–<b>e</b>) Conductance <span class="html-italic">G</span> of undoped trilayer, bilayer, and monolayer device as <span class="html-italic">E</span><sub>⊥</sub> is swept up and down (black arrows) [<a href="#B21-nanomaterials-15-00109" class="html-bibr">21</a>]; The polarization is represented by a green or red arrow in (<b>c</b>); The location of a centre of symmetry is represented by a red dot in (<b>e</b>). Reprinted with permission from [<a href="#B41-nanomaterials-15-00109" class="html-bibr">41</a>], 2014, American Chemical Society; and [<a href="#B21-nanomaterials-15-00109" class="html-bibr">21</a>], 2018, Springer Nature.</p>
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<p>(<b>a</b>) Multi-state (green and red arrows indicate the polarization of states) control of 2D multiferroic bilayer VS<sub>2</sub> [<a href="#B45-nanomaterials-15-00109" class="html-bibr">45</a>]. (<b>b</b>) FE domains formed by Moiré patterns upon a small angle twist of a VTe<sub>2</sub> bilayer [<a href="#B47-nanomaterials-15-00109" class="html-bibr">47</a>]. Reprinted with permission from [<a href="#B45-nanomaterials-15-00109" class="html-bibr">45</a>], 2020, American Chemical Society; and [<a href="#B47-nanomaterials-15-00109" class="html-bibr">47</a>], 2018, American Chemical Society.</p>
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<p>(<b>a</b>) The geometries of stable type−I (<b>a</b>), II (<b>b</b>), and III (<b>c</b>) FE MXenes [<a href="#B53-nanomaterials-15-00109" class="html-bibr">53</a>]. (<b>d</b>) FE hysteresis loops of the Ti<sub>3</sub>C<sub>2</sub>T<sub>x</sub> MXene film at 100 °C [<a href="#B54-nanomaterials-15-00109" class="html-bibr">54</a>]. (<b>e</b>) Nonvolatile bipolar switching in single cell for logarithmic I–V measurements [<a href="#B54-nanomaterials-15-00109" class="html-bibr">54</a>]. Reprinted with permission from [<a href="#B53-nanomaterials-15-00109" class="html-bibr">53</a>], 2020, Royal Society of Chemistry; and [<a href="#B54-nanomaterials-15-00109" class="html-bibr">54</a>], 2023, AIP Publishing.</p>
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<p>(<b>a</b>) Perspective view of GeSe monolayer [<a href="#B63-nanomaterials-15-00109" class="html-bibr">63</a>]. (<b>b</b>) Potential energy surface with fractional shift of Se atoms and the corresponding contour plots [<a href="#B63-nanomaterials-15-00109" class="html-bibr">63</a>]. (<b>c</b>) Double-well potential of GeSe monolayer and the atomic configurations with specific polarization [<a href="#B63-nanomaterials-15-00109" class="html-bibr">63</a>]. Reprinted with permission from [<a href="#B63-nanomaterials-15-00109" class="html-bibr">63</a>], 2017, IOP Publishing.</p>
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<p>(<b>a</b>) Description of sliding processes. FE polarization and total energy difference as functions of the sliding distance for bilayer SnSe shifted (<b>b</b>) from AC to AD and (<b>c</b>) from AC to AB stacking sequences. (<b>d</b>–<b>g</b>) Contour plots of spontaneous polarization as a function of mechanical sliding distance for SnS, SnSe, GeS, and GeSe, respectively [<a href="#B68-nanomaterials-15-00109" class="html-bibr">68</a>]. Reprinted with permission from [<a href="#B68-nanomaterials-15-00109" class="html-bibr">68</a>], 2022, Springer Nature.</p>
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<p>The energy barrier of polarization reversal in α-In<sub>2</sub>Se<sub>3</sub> through (<b>a</b>) one-step and (<b>b</b>) three-step concerted mechanisms [<a href="#B72-nanomaterials-15-00109" class="html-bibr">72</a>]; In and Se atoms are in blue and red, respectively. (<b>c</b>) In-plane (initial a<sub>1</sub>–d<sub>1</sub> and switched a<sub>2</sub>–d<sub>2</sub> states) and out-of-plane (switched e–h states) PFM phase images of 2H-stacked α-In<sub>2</sub>Se<sub>3</sub> with different layers [<a href="#B73-nanomaterials-15-00109" class="html-bibr">73</a>]. Reprinted with permission from [<a href="#B72-nanomaterials-15-00109" class="html-bibr">72</a>], 2017, Springer Nature; and [<a href="#B73-nanomaterials-15-00109" class="html-bibr">73</a>], 2021, Royal Society of Chemistry.</p>
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18 pages, 13315 KiB  
Article
Numerical Investigation of the Coupling Effects of Pulsed H2 Jets and Nanosecond-Pulsed Actuation in Supersonic Crossflow
by Keyu Li and Jiangfeng Wang
Aerospace 2025, 12(1), 44; https://doi.org/10.3390/aerospace12010044 - 11 Jan 2025
Viewed by 390
Abstract
Numerical investigations were conducted to analyze the coupling effects of pulsed H2 jets and nanosecond-pulsed actuation (NS-SDBD) in a supersonic crossflow. The FVM was employed to solve the multi-component 2D URANS equations with the SST k-omega turbulence model, while H2-air [...] Read more.
Numerical investigations were conducted to analyze the coupling effects of pulsed H2 jets and nanosecond-pulsed actuation (NS-SDBD) in a supersonic crossflow. The FVM was employed to solve the multi-component 2D URANS equations with the SST k-omega turbulence model, while H2-air combustion was described using a seven species–seven reactions chain reaction model, and the plasma thermal effect was represented by a phenomenological model. The backward-facing step flows with an inlet Mach number of 2.5 and a pulsed jet frequency of 10 kHz under different actuation conditions were simulated. The combustion enhancement mechanism under an actuation frequency of 20 kHz was analyzed. Research indicates that compression waves induced by NS-SDBD enhance H2-air mixing and facilitate temperature transport as the flow progresses. This progress is significantly associated with the flow structures generated by pulsed jets. Under this condition, the fuel utilization rate in the flow field increased by 61.2%, the total pressure recovery coefficient increased by 5.34%, and the outlet total temperature slightly increased even with a 50% reduction in fuel flow rate. Comparative analysis of different actuation cases demonstrates that evenly distributed actuation within the jet cycle yields better effects. The innovation of this study lies in proposing and exploring a potential method to address inadequate combustion under high-speed inflow conditions, which couples NS-SDBD with pulsed hydrogen jets. Full article
(This article belongs to the Special Issue Innovations in Hypersonic Propulsion Systems)
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<p>Schematic diagram of the pulsed H<sub>2</sub> jet and NS-SDBD combined flow control scheme.</p>
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<p>Geometric model and boundary conditions.</p>
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<p>Comparison of dimensionless pressure with Aso’s experiment [<a href="#B37-aerospace-12-00044" class="html-bibr">37</a>].</p>
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<p>Spatial and planar streamlines of the 3D flow: (<b>a</b>) overall diagram; (<b>b</b>) local magnified diagram.</p>
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<p>Computational domain of the NS-SDBD validation case.</p>
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<p>Comparison of density gradients: (<b>a</b>) schlieren images from ref. [<a href="#B39-aerospace-12-00044" class="html-bibr">39</a>]; (<b>b</b>) density gradient contours from this study.</p>
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<p>Comparison of dimensionless density distribution at Y = 1 mm, t = 0.3 ms with ref. [<a href="#B39-aerospace-12-00044" class="html-bibr">39</a>].</p>
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<p>Comparison of the three grids: (<b>a</b>) wall pressure; (<b>b</b>) velocity of Line 2.</p>
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<p>Grid errors between M2 and M3: (<b>a</b>) approximate relative error; (<b>b</b>) the numerical error band.</p>
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<p>M2 grid and local details.</p>
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<p>Mach number contours and streamline near the nozzle.</p>
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<p>Pulse jet and actuation waveform.</p>
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<p>H<sub>2</sub>O mass fraction distribution without actuation: A, B, and C represent hydrogen clusters; D represents the continuous hydrogen stream.</p>
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<p>Temporal variation of the average H<sub>2</sub>O mass fraction along the monitoring lines: (<b>a</b>) X = 0.086 m, L1; (<b>b</b>) X = 0.14 m, L2; (<b>c</b>) X = 0.194 m, L3. A–D represent the peak values of the corresponding flow structures.</p>
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<p>H<sub>2</sub>O mass fraction contours around the monitoring lines: (<b>a</b>) X = 0.086 m, t = 0.2<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>T</mi> </mrow> <mrow> <mi>j</mi> </mrow> </msub> </mrow> </semantics></math>; (<b>b</b>) X = 0.086 m, t = 0.65<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>T</mi> </mrow> <mrow> <mi>j</mi> </mrow> </msub> </mrow> </semantics></math>; (<b>c</b>) X = 0.14 m, t = 0.55<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>T</mi> </mrow> <mrow> <mi>j</mi> </mrow> </msub> </mrow> </semantics></math>, Peak A; (<b>d</b>) X = 0.14 m, t = 0.2<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>T</mi> </mrow> <mrow> <mi>j</mi> </mrow> </msub> </mrow> </semantics></math>, Peak D; (<b>e</b>) X = 0.194 m, t = 1.0<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>T</mi> </mrow> <mrow> <mi>j</mi> </mrow> </msub> </mrow> </semantics></math>, Peak A; (<b>f</b>) X = 0.194 m, t = 0.69<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>T</mi> </mrow> <mrow> <mi>j</mi> </mrow> </msub> </mrow> </semantics></math>, Peak D.</p>
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<p>Flow parameter distribution of the characteristic line: (<b>a</b>) pressure; (<b>b</b>) temperature.</p>
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<p>Flow parameter distribution without combustion: (<b>a</b>) temperature; (<b>b</b>) H<sub>2</sub> mass fraction.</p>
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<p>Variation of model outlet total temperature.</p>
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23 pages, 36687 KiB  
Article
UAV–UGV Formation for Delivery Missions: A Practical Case Study
by Leonardo A. Fagundes-Júnior, Celso O. Barcelos, Amanda S. Piaia and Alexandre S. Brandão
Drones 2025, 9(1), 48; https://doi.org/10.3390/drones9010048 - 11 Jan 2025
Viewed by 203
Abstract
Robotic transport missions serve a variety of valuable purposes within similar contexts. These include delivering packages in urban or remote areas, dispatching supplies to disaster or conflict zones, and facilitating delivery operations. In such a context, this work deals with the cooperation and [...] Read more.
Robotic transport missions serve a variety of valuable purposes within similar contexts. These include delivering packages in urban or remote areas, dispatching supplies to disaster or conflict zones, and facilitating delivery operations. In such a context, this work deals with the cooperation and control of multiple-robot systems involving heterogeneous robot formation with sensing and actuation capabilities to perform load transportation tasks. Two off-the-shelf unmanned ground vehicles (UGVs) working cooperatively with one unmanned aerial vehicle (UAV) are used to validate the proposal. The interactions between the UAV and the UGVs are not only information exchanges but also physical couplings required to cooperate in the load’s joint transportation. The existence of an obstacle between the two UGVs makes it impossible for them to meet each other. Thus, the lifting, transport, and delivery of the load from one UGV to the other are performed by a UAV with a suspended electromagnet actuator. Experiments are performed for a weight of 165 g (load + electronic board), which corresponds to up to 36% of the UAV’s mass. Full article
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<p>UGV load transportation limitations due to specific environment constraints. A possible solution for delivery packets in long-distance missions is the cooperation between UAV and UGVs in the mission planning step.</p>
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<p>Spatial unicycle-type robot representation and polar modeling variables (in blue). The target point is represented by <math display="inline"><semantics> <mrow> <msub> <mi mathvariant="bold">x</mi> <mi>d</mi> </msub> <mo>=</mo> <msup> <mrow> <mo>[</mo> <msub> <mi>x</mi> <mi>d</mi> </msub> <msub> <mi>y</mi> <mi>d</mi> </msub> <msub> <mi>ψ</mi> <mi>d</mi> </msub> <mo>]</mo> </mrow> <mo>⊺</mo> </msup> </mrow> </semantics></math>.</p>
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<p>The dynamic control system in charge of guiding the robot to the target point.</p>
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<p>Parrot Bebop 2 description and pose variables, according to Tait–Bryan angle notation.</p>
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<p>The dynamic control system in charge of guiding the robot to the target point.</p>
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<p>An example of a delivery agency and the route management proposed.</p>
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<p>Mission scenario description and the robots used in this work. Image (<b>1</b>) shows the real-world scenario where the experiments were conducted. Images (<b>2</b>) and (<b>3</b>) highlight the load and the actuator, respectively. The real-world devices are depicted in images (<b>4</b>–<b>6</b>): the Pioneer 3-DX and its trailer, as well as the Bebop 2 UAV with the markers used for motion capture. Image (<b>6</b>) provides a complete view of all robots used in this work, including the UGV, UAV, cargo, and the trailer coupled to the UGV. At the center, the virtual representation used in subsequent discussions is illustrated.</p>
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<p>The stages of the proposed UAV–UGV cooperation strategy for load transportation in hard-to-navigate terrestrial environments.</p>
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<p>An overview of the hardware setup used to run the experiment. The Optitrack cameras compose the motion capture system, responsible for tracking all the rigid bodies in the arena.</p>
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<p>Electromagnet PCBs: (<b>a</b>) Transmitter. (<b>b</b>) Receiver.</p>
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<p>The actuator control strategy: (<b>a</b>) Error measurement. (<b>b</b>) Situation in which the electromagnet will be activated to pick up the cargo.</p>
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<p>Task planning for each robot based on state machine representation.</p>
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<p>Tracking performance of the UAV: (<b>a</b>) <b>UAV</b> position; (<b>b</b>) <b>UGV A</b>; (<b>c</b>) load, (<b>d</b>) <b>UGV B</b>, and (<b>e</b>) trailer.</p>
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<p>Tracking performance of the UGVs in the experiments. The gray dashed regions represent the period in which the robots are executing a stage of the strategy. Tracked positions for both UGVs: (<b>a</b>) real-time autonomous take-off, tracking, and landing of UAV on a moving UGV platform and (<b>b</b>) <span class="html-italic">x</span>-<span class="html-italic">y</span> view of the UGVs’ performed routes and desired trajectory/positions.</p>
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12 pages, 3718 KiB  
Article
Analysis of Collision Types in Collaborative Robots Using Mechanism Actuated by Pneumatic Artificial Muscle
by Dávid Kóczi and József Sárosi
Actuators 2025, 14(1), 22; https://doi.org/10.3390/act14010022 - 10 Jan 2025
Viewed by 302
Abstract
In the safety technology of collaborative robots, standards differentiate between various collision types, the identification and differentiation of which are essential for ensuring safe operation. The objective of this paper is to develop and test a mechanism actuated by artificial muscle to examine [...] Read more.
In the safety technology of collaborative robots, standards differentiate between various collision types, the identification and differentiation of which are essential for ensuring safe operation. The objective of this paper is to develop and test a mechanism actuated by artificial muscle to examine the detection of these profiles in different collision scenarios. The ISO 15066 standard distinguishes between two types of collisions: quasi-static and transient. Using a simplified model, experiments were conducted to evaluate whether sensors could identify collision types accurately. The results demonstrate the feasibility of identifying collision types through sensor data. The findings have the potential to enhance the safety of collaborative robots. Full article
(This article belongs to the Special Issue Advanced Technologies in Soft Actuators)
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<p>Quasi-static and transient contact.</p>
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<p>Graphical representation of acceptable and unacceptable forces or pressures.</p>
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<p>Pneumatic artificial muscle (PAM).</p>
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<p>Pneumatic diagram: 1. air preparation unit; 2. artificial muscle: Festo MAS-10-40N-AA; 3. cylinder: Hafner PLF32; 4. proportional valve: AVENTIC Series ED02.</p>
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<p>Experimental setup for collision type analysis using PAM.</p>
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<p>Measurement system: (<b>a</b>) picture of assembled measurement system; (<b>b</b>) collision surface with sensor.</p>
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<p>Input/output diagram.</p>
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<p>LabVIEW user interface.</p>
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<p>Position measurement results. (<b>a</b>) PAM contraction/time diagram for transient collision; (<b>b</b>) PAM contraction/time diagram for static collision.</p>
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<p>Pressure measurement results. (<b>a</b>) PAM pressure change/time diagram for transient collision; (<b>b</b>) PAM pressure change/time diagram for static collision.</p>
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<p>Measurement results of a load cell. (<b>a</b>) PAM force–time diagram for transient collision; (<b>b</b>) PAM force–time diagram for static collision.</p>
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<p>Force-sensitive resistor measurement results. (<b>a</b>) PAM voltage–time diagram for transient collision; (<b>b</b>) PAM voltage–time diagram for static collision.</p>
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15 pages, 2985 KiB  
Article
‘Ship-in-a-Bottle’ Integration of pH-Sensitive 3D Proteinaceous Meshes into Microfluidic Channels
by Daniela Serien, Koji Sugioka and Aiko Narazaki
Nanomaterials 2025, 15(2), 104; https://doi.org/10.3390/nano15020104 - 10 Jan 2025
Viewed by 427
Abstract
Microfluidic sensors incorporated onto chips allow sensor miniaturization and high-throughput analyses for point-of-care or non-clinical analytical tools. Three-dimensional (3D) printing based on femtosecond laser direct writing (fs-LDW) is useful for creating 3D microstructures with high spatial resolution because the structures are printed in [...] Read more.
Microfluidic sensors incorporated onto chips allow sensor miniaturization and high-throughput analyses for point-of-care or non-clinical analytical tools. Three-dimensional (3D) printing based on femtosecond laser direct writing (fs-LDW) is useful for creating 3D microstructures with high spatial resolution because the structures are printed in 3D space along a designated laser light path. High-performance biochips can be fabricated using the ‘ship-in-a-bottle’ integration technique, in which functional microcomponents or biomimetic structures are embedded inside closed microchannels using fs-LDW. Solutions containing protein biomacromolecules as a precursor can be used to fabricate microstructures that retain their native protein functions. Here, we demonstrate the ship-in-a-bottle integration of pure 3D proteinaceous microstructures that exhibit pH sensitivity. We fabricated proteinaceous mesh structures with gap sizes of 10 and 5 μm. The sizes of these gaps changed when exposed to physiological buffers ranging from pH of 4 to 10. The size of the gaps in the mesh can be shrunk and expanded repeatedly by changing the pH of the surrounding buffer. Fs-LDW enables the construction of microscopic proteinaceous meshes that exhibit dynamic functions such as pH sensing and might find applications for filtering particles in microfluidic channels. Full article
(This article belongs to the Section Nanofabrication and Nanomanufacturing)
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<p>Schematic drawing showing integration of pure 3D proteinaceous mesh into glass-elastomer microchannels. (<b>a</b>) A thin cover glass is bonded to the elastomer microchannel to enclose the microchannel. The closed microchannel is filled with a high concentration of protein precursor solution. Fs-LDW is used to fabricate proteinaceous meshes in the channels which are anchored at the top and bottom of the channel. (<b>b</b>) In the pH range 4–10 under our fabrication conditions, the gap size of meshes correlates with the pH of the applied external pH buffer solution.</p>
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<p>Fabrication setup and microfluidic chip preparation. (<b>a</b>) The 1040-nm laser (L) output with a repetition rate of 100 kHz and a pulse width of about 350 fs is converted to 520 nm green laser light via lambda-half zero order waveplate (WP), beta barium borate crystal (BBO) and the remaining NIR is filtered by a 520 nm bandpass filter (F). PC-controlled power attenuation, which is achieved via another waveplate (WP) and a polarizing beam splitter (PBS) that leads excess energy into a beam dump (BD), mirrors (M), and neutral density (ND) filters set the pulse energy. A 2x beam expander (BE) overfills the back-end aperture of the N.A. = 0.45 objective lens (OL) with a working distance (WD) of 13.8 mm. Through a 50:50 beam splitter cube (BS), the average power is monitored in situ with a microscope slide power sensor (D). The inset shows the measured pulse energy converted from power measurements by taking into account a transmittance of 0.987 for both split paths. A dichroic mirror (DM) and camera (C) allow in situ observation. Mechanical shutter (S) and mechanical stage (ST) are PC-controlled. (<b>b</b>) (i) A microfluidic chip is split into elastomer and hard-plastic top cover. (ii) The elastomer is cut. (iii) After cleaning the surface with ethanol, an O<sub>2</sub> plasma is applied for 60 s to facilitate bonding and increase channel hydrophilicity. Then, the O<sub>2</sub> plasma-treated 120 μm-to 170 μm-thin glass is quickly and firmly attached to the channel to be bonded, as well as a 5 mm-long silicon tube aligned to the inlet. (iv) After a further 30 s of O<sub>2</sub> plasma, the channel is filled with protein precursor, as indicated with dashed outline. (v) Evaporation from the inlet and outlet causes flow inside the microchannel. Therefore, we store the channels for at least 1 day until the evaporation solidifies the precursor at inlet and outlet, causing the in-channel liquid precursor to become stationary.</p>
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<p>Design of 3D free-standing mesh and constrained on-glass control. (<b>a</b>) A 3D rendered image made from Blender (v 2.92.0, Blender Foundation, Amsterdam, The Netherlands) represents the dimensions of the mesh. The 3D render is to remind that fs-LDW forms volume elements and even though the top down view looks 2D, each line element is actually 3D of micron-to-submicron scale. Three microscopic images are shown. A 100 × 50 μm<sup>2</sup> area is fabricated with either 10 or 5 μm-wide gaps between the mesh lines. Immersion in pH 6 (left) and pH 9 (right) buffer shows that the meshes are free-standing. The mesh gap size changes from its original size, depending on the external pH. The original design is shown as a control attached to glass (middle). Attachment to the glass surface constrains the structure and prevents changes in the gap size. Scale bars represent 50 μm. (<b>b</b>) Gap sizes were evaluated as the percent change as a function of the pulse energy used for fabrication. At the given stage scanning speed, the fabrication window is approximately 1.25 to 3 nJ. On a secondary <span class="html-italic">x</span>-axis in (<b>b</b>), we converted the pulse energy to total accumulated fluence (TAF). (<b>c</b>) Recontextualized data of (<b>b</b>) are plotted as the dependence of gap size on the pH value for pulse energies between 1.5 and 3 nJ. The gap size monotonically increased with increasing pH for 1.5 nJ, but for 2, 2.5 nJ and 3 nJ are non-monotonic with fluctuations.</p>
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<p>(<b>a</b>) Fluorescence laser scanning visualization of 3D proteinaceous meshes in a channel upon 405 and 488 nm excitation. (Top) Schematic representations, (middle) orthogonal views, and (bottom) 3D reconstructions are shown for (<b>a</b>) a horizontal design anchored to the channel side walls and fabricated with pulse energy of 2 nJ, (<b>b</b>) a diagonal design fabricated with pulse energy of 1.5 nJ and (<b>c</b>) a vertical design fabricated with pulse energy of 2 nJ for horizontal and 1.4 nJ for vertical lines. The diagonal and vertical meshes are anchored on the channel ceiling and bottom. All designs have a gap size of 10 μm and were fabricated with 400 mg/mL BSA embedded in 100 μm-wide microchannels with a 100 × 50 μm<sup>2</sup> cross-section, using a laser energy of 1.4–2 nJ at a scanning speed of 5 μm/s. After removal of the precursor by rinsing with pH 6 buffer, a pH 6 buffer containing fluorescein sodium salt was capillary flowed into the channel to allow green fluorescence detection of the channel and blue fluorescence detection of the fabricated structures. The elastomer is not fluorescent and therefore shows as dark areas.</p>
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<p>Setup, gap size and pH-actuation of in-channel meshes. (<b>a</b>) Filling the inlet with fluorescein sodium salt and pH 6 buffer to trace liquid movement. The gravitation flow resulting from a height difference of 5 mm was determined to be about 30 μm/s. To observe the microstructures with 20× lens, 12 mm or more distance to the inlet is required, resulting in 10–20 min long experiments for buffer exchange. The timing of refilling the inlet is also delicate, waiting too long and accidentally including air inclusion risks terminating the flow. Rough handling of the inlet can cause leakage which also terminates the experiment. (<b>b</b>) Deformation of a mesh fabricated using a laser energy of 2 nJ and a scanning speed of 5 μm/s in pH 4 and pH 10 buffer. (<b>c</b>) Change in gap size by repeatedly changing the pH of buffer solution after 10 buffer exchanges. (<b>i</b>) The pH 10 buffer is introduced at the odd-numbered step and the pH 4 buffer is introduced at the even-numbered step. (<b>ii</b>) In pH 4 buffer, the gap size was smaller by −12 ± 2% compared to the original size. In pH 10 buffer, the gap size increased by +13 ± 2%.</p>
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27 pages, 16018 KiB  
Article
Investigation of Structural Nonlinearity Effects on the Aeroelastic and Wake Characteristics of a 15 MW Wind Turbine
by Zhenju Chuang, Lulin Xia, Yan Qu, Wenhua Li and Jiawen Li
J. Mar. Sci. Eng. 2025, 13(1), 116; https://doi.org/10.3390/jmse13010116 - 10 Jan 2025
Viewed by 323
Abstract
As wind turbines increase in size, blades become longer, thinner, and more flexible, making them more susceptible to large geometric nonlinear deformations, which pose challenges for aeroelastic simulations. This study presents a nonlinear aeroelastic model that accounts for large deformations of slender, flexible [...] Read more.
As wind turbines increase in size, blades become longer, thinner, and more flexible, making them more susceptible to large geometric nonlinear deformations, which pose challenges for aeroelastic simulations. This study presents a nonlinear aeroelastic model that accounts for large deformations of slender, flexible blades, coupled through the Actuator Line Method (ALM) and Geometrically Exact Beam Theory (GEBT). The accuracy of the model is validated by comparing it with established numerical methods, demonstrating its ability to capture the bending–torsional coupled nonlinear characteristics of highly flexible blades. A bidirectional fluid–structure coupling simulation of the IEA 15MW wind turbine under uniform flow conditions is conducted. The effect of blade nonlinear deformation on aeroelastic performance is compared with a linear model based on Euler–Bernoulli beam theory. The study finds that nonlinear deformations reduce predicted angle of attack, decrease aerodynamic load distribution, and lead to a noticeable decline in both wind turbine performance and blade deflection. The effects on thrust and edgewise deformation are particularly significant. Additionally, nonlinear deformations weaken the tip vortex strength, slow the momentum exchange in the wake region, reduce turbulence intensity, and delay wake recovery. This study highlights the importance of considering blade nonlinear deformations in large-scale wind turbines. Full article
(This article belongs to the Topic Wind, Wave and Tidal Energy Technologies in China)
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<p>Velocity vectors of an airfoil section.</p>
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<p>Beam in deformed states.</p>
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<p>Coupling scheme of the fluid and structural solvers.</p>
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<p>Grid discretization and boundary conditions of the computational domain.</p>
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<p>Rotor thrust and flapwise deformation with varying body force projection width (<math display="inline"><semantics> <mi>ϵ</mi> </semantics></math>): (<b>a</b>) rotor thrust. (<b>b</b>) flapwise deformation. <math display="inline"><semantics> <mrow> <mi>t</mi> <mo>/</mo> <msub> <mi>T</mi> <mi>R</mi> </msub> </mrow> </semantics></math> represents the ratio of the rotor response time to the rated period, where <math display="inline"><semantics> <mrow> <msub> <mi>T</mi> <mi>R</mi> </msub> <mo>=</mo> <mn>7.95</mn> <mspace width="0.166667em"/> <mi mathvariant="normal">s</mi> </mrow> </semantics></math>.</p>
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<p>Aeroelastic response under different mesh sizes: (<b>a</b>) rotor power and thrust; (<b>b</b>) flapwise and edgewise deformation.</p>
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<p>The periodic deflection of the tip at rated wind speed for 5MW: (<b>a</b>) flapwise deformation. (<b>b</b>) Edgewise deformation. CFD-CSD (Dose, 2018) [<a href="#B8-jmse-13-00116" class="html-bibr">8</a>]; ALM-GEBT (Leng, 2023) [<a href="#B9-jmse-13-00116" class="html-bibr">9</a>]; ACE+FEM (Yang, 2024) [<a href="#B49-jmse-13-00116" class="html-bibr">49</a>].</p>
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<p>Distribution of blade deflection along the blade at rated wind speed for 5MW: (<b>a</b>) Flapwise deformation. (<b>b</b>) Edgewise deformation. (<b>c</b>) Torsional deformation. <math display="inline"><semantics> <mrow> <mi>r</mi> <mo>/</mo> <mi>R</mi> </mrow> </semantics></math> represents the ratio of the blade position to the total blade length, where <math display="inline"><semantics> <mrow> <mi>R</mi> <mo>=</mo> <mn>117</mn> <mspace width="0.166667em"/> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>. CFD-CSD (Dose, 2018) [<a href="#B8-jmse-13-00116" class="html-bibr">8</a>]; ALM-GEBT (Leng, 2023) [<a href="#B9-jmse-13-00116" class="html-bibr">9</a>]; ACE+FEM (Yang, 2024) [<a href="#B49-jmse-13-00116" class="html-bibr">49</a>].</p>
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<p>Tip deflection of the 15MW wind turbine at rated wind speed: (<b>a</b>) Flapwise deformation. (<b>b</b>) Edgewise deformation. (<b>c</b>) Torsional deformation.</p>
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<p>Distribution of blade deflection along the blade at rated wind speed for 15MW: (<b>a</b>) Flapwise deformation. (<b>b</b>) Edgewise deformation. (<b>c</b>) Torsional deformation.</p>
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<p>Comparative analysis of aerodynamic loads for EALM and GALM at rated wind speed: (<b>a</b>) Aerodynamic power. (<b>b</b>) Aerodynamic thrust.</p>
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<p>Angle of attack (AOA) for EALM and GALM at rated wind speed: (<b>a</b>) Variation in the blade spanwise distribution. (<b>b</b>) Blade tip response.</p>
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<p>Relative speed (<math display="inline"><semantics> <msub> <mi>U</mi> <mi>mag</mi> </msub> </semantics></math>) for EALM and GALM at rated wind speed: (<b>a</b>) Variation in the blade spanwise distribution. (<b>b</b>) Blade tip response.</p>
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<p>Distribution of angle of attack (AOA) and relative speed (<math display="inline"><semantics> <msub> <mi>U</mi> <mi>mag</mi> </msub> </semantics></math>) along the blade for EALM and GALM at rated wind speed: (<b>a</b>) AOA. (<b>b</b>) <math display="inline"><semantics> <msub> <mi>U</mi> <mi>mag</mi> </msub> </semantics></math>.</p>
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<p>Distribution of aerodynamic loads along the blade for EALM and GALM at rated wind speed: (<b>a</b>) Normal force. (<b>b</b>) Tangential force.</p>
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<p>Flapwise deformation for EALM and GALM at rated wind speed: (<b>a</b>) Variation in the blade spanwise distribution. (<b>b</b>) Blade tip response.</p>
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<p>Edgewise deformation for EALM and GALM at rated wind speed: (<b>a</b>) Variation in the blade spanwise distribution. (<b>b</b>) Blade tip response.</p>
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<p>Torsional deformation for EALM and GALM at rated wind speed: (<b>a</b>) Variation in the blade spanwise distribution. (<b>b</b>) Blade tip response.</p>
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<p>Distribution of blade deformation along the blade at rated wind speed for EALM and GALM: (<b>a</b>) Flapwise deformation. (<b>b</b>) Edgewise deformation. (<b>c</b>) Torsional deformation.</p>
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<p>Vortex structure (Q = 0.001) at rated wind speed for EALM and GALM.</p>
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<p>Comparative analysis of vortex structure contours at hub-height horizontal plane (z = 0 m) for EALM and GALM.</p>
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<p>The wake-averaged velocity field in EALM and GALM: (<b>a</b>) In the vertical plane (y = 0 m). (<b>b</b>) In the horizontal plane (z = 0 m). <math display="inline"><semantics> <mrow> <mi>x</mi> <mo>/</mo> <mi>D</mi> </mrow> </semantics></math> represents the ratio of the flow field position to the wind turbine diameter, where <math display="inline"><semantics> <mrow> <mi>D</mi> <mo>=</mo> <mn>240</mn> <mspace width="0.166667em"/> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>.</p>
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<p>The wake-averaged velocity field in EALM and GALM: (<b>a</b>) The average velocity contour. (<b>b</b>) The streamwise velocity deficit profiles at hub height (z = 0 m). <math display="inline"><semantics> <mrow> <mrow> <mo mathvariant="normal">Δ</mo> <mi>U</mi> </mrow> <mo>/</mo> <msub> <mi>U</mi> <mi>hub</mi> </msub> </mrow> </semantics></math> is a dimensionless parameter that reflects the wake velocity loss, <math display="inline"><semantics> <mrow> <mo mathvariant="normal">Δ</mo> <mi>U</mi> <mo>=</mo> <msub> <mi>U</mi> <mi>hub</mi> </msub> <mo>−</mo> <msub> <mi>U</mi> <mi>mag</mi> </msub> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mi>U</mi> <mi>hub</mi> </msub> <mo>=</mo> <mn>10.59</mn> <mspace width="0.166667em"/> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>.</p>
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<p>Comparative analysis of the turbulence intensity field in EALM and GALM: (<b>a</b>) The turbulence intensity contour (z = 0 m). (<b>b</b>) The turbulence intensity at hub height (z = 0 m). <math display="inline"><semantics> <msub> <mi>T</mi> <mi>i</mi> </msub> </semantics></math> is the turbulence intensity.</p>
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24 pages, 13018 KiB  
Article
Amplifying the Sensitivity of Electrospun Polyvinylidene Fluoride Piezoelectric Sensors Through Electrical Polarization Process for Low-Frequency Applications
by Asra Tariq, Amir H. Behravesh, Muhammad Tariq and Ghaus Rizvi
Fibers 2025, 13(1), 5; https://doi.org/10.3390/fib13010005 - 9 Jan 2025
Viewed by 316
Abstract
Piezoelectric sensors convert mechanical stress into electrical charge via the piezoelectric effect, and when fabricated as fibers, they offer flexibility, lightweight properties, and adaptability to complex shapes for self-powered wearable sensors. Polyvinylidene fluoride (PVDF) nanofibers have garnered significant interest due to their potential [...] Read more.
Piezoelectric sensors convert mechanical stress into electrical charge via the piezoelectric effect, and when fabricated as fibers, they offer flexibility, lightweight properties, and adaptability to complex shapes for self-powered wearable sensors. Polyvinylidene fluoride (PVDF) nanofibers have garnered significant interest due to their potential applications in various fields, including sensors, actuators, and energy-harvesting devices. Achieving optimal piezoelectric properties in PVDF nanofibers requires the careful optimization of polarization. Applying a high electric field to PVDF chains can cause significant mechanical deformation due to electrostriction, leading to crack formation and fragmentation, particularly at the chain ends. Therefore, it is essential to explore methods for polarizing PVDF at the lowest possible voltage to prevent structural damage. In this study, a Design of Experiments (DoE) approach was employed to systematically optimize the polarization parameters using a definitive screening design. The main effects of the input parameters on piezoelectric properties were identified. Heat treatment and the electric field were significant factors affecting the sensor’s sensitivity and β-phase fraction. At the highest temperature of 120 °C and the maximum applied electric field of 3.5 kV/cm, the % β-phase (F(β)) exceeded 95%. However, when reducing the electric field to 1.5 kV/cm and 120 °C, the % F(β) ranged between 87.5% and 90%. The dielectric constant (ɛ′) of polarized PVDF was determined to be 30 at an electric field frequency of 1 Hz, compared to a value of 25 for non-polarized PVDF. The piezoelectric voltage coefficient (g33) for polarized PVDF was measured at 32 mV·m/N at 1 Hz, whereas non-polarized PVDF exhibited a value of 3.4 mV·m/N. The findings indicate that, in addition to a high density of β-phase dipoles, the polarization of these dipoles significantly enhances the sensitivity of the PVDF nanofiber mat. Full article
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<p>Step-by-step process for the electrospinning and electrical polarization of PVDF.</p>
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<p>Electrical polarization setup for PVDF electrospun mat.</p>
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<p>(<b>a</b>) Scanning electron microscopy (SEM) image of electrospun PVDF; (<b>b</b>) fiber diameter distribution.</p>
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<p>Processed micrographs of electrospun PVDF at three different thresholds (<b>a</b>) Threshold I, (<b>b</b>) Threshold II, (<b>c</b>) Threshold III.</p>
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<p>Processed micrographs of electrospun PVDF at three different thresholds (<b>a</b>) Threshold I, (<b>b</b>) Threshold II, (<b>c</b>) Threshold III.</p>
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<p>FTIR spectra of PVDF nanofibers, nonpolarized (P), and polarized mat (EP-3 and EP-5).</p>
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<p>Comparison of XRD pattern of nonpolarized (P) and polarized PVDF electrospun mats (EP-8, EP-4).</p>
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<p>The main effect plots obtained from the definitive screen design analysis for the β-phase.</p>
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<p>Mathematical model validation of the % β-phase content with experimental results.</p>
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<p>Contour plot of % of β-phase as a function of (<b>a</b>) heat treatment and electric field; (<b>b</b>) heat treatment and time; and (<b>c</b>) electric field and time.</p>
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<p>Nyquist plots for polarized and non-polarized electrospun PVDF.</p>
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<p>(<b>a</b>) Dielectric constant (<span class="html-italic">ɛ</span>′) and (<b>b</b>) dielectric loss (<span class="html-italic">ɛ</span>″) of polarized and non-polarized electrospun PVDF.</p>
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<p>Comparison of the measured dielectric constant (<span class="html-italic">ɛ</span>′) with the calculated <span class="html-italic">ɛ</span>′ at different digital porosities (DPs) % using Bruggeman Effective Medium Approximation.</p>
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<p>Sensor’s sensitivity measurement setup at precise force and frequency.</p>
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<p>The output response of sensors when applying different force levels at different frequencies: (<b>a</b>) high-sensitivity PVDF nanofiber mat (EP-5); (<b>b</b>) low-sensitivity PVDF nanofiber mat (EP-11); (<b>c</b>) measured response waveform of EP-5 at 1 Hz and 10 N; (<b>d</b>) measured response when applying a 10 N force at 1 Hz on silicon rubber.</p>
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<p>The voltage signal and force relation curve of the high-sensitivity sensor (EP-5) and low-sensitivity sensor EP-11.</p>
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<p>β-phase fraction (% F(β)) versus sensitivity of polarized and non-polarized PVDF.</p>
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<p>Main effect plots obtained from definitive screen design analysis for the sensitivity of PVDF electrospun sensors (<b>a</b>) at 2Hz, (<b>b</b>) at 1Hz, (<b>c</b>) at 0.5Hz.</p>
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<p>Main effect plots obtained from definitive screen design analysis for the sensitivity of PVDF electrospun sensors (<b>a</b>) at 2Hz, (<b>b</b>) at 1Hz, (<b>c</b>) at 0.5Hz.</p>
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36 pages, 9661 KiB  
Article
Piezoresistive Cantilever Microprobe with Integrated Actuator for Contact Resonance Imaging
by Tianran Ma, Michael Fahrbach and Erwin Peiner
Sensors 2025, 25(2), 332; https://doi.org/10.3390/s25020332 - 8 Jan 2025
Viewed by 442
Abstract
A novel piezoresistive cantilever microprobe (PCM) with an integrated electrothermal or piezoelectric actuator has been designed to replace current commercial PCMs, which require external actuators to perform contact-resonance imaging (CRI) of workpieces and avoid unwanted “forest of peaks” observed at large travel speed [...] Read more.
A novel piezoresistive cantilever microprobe (PCM) with an integrated electrothermal or piezoelectric actuator has been designed to replace current commercial PCMs, which require external actuators to perform contact-resonance imaging (CRI) of workpieces and avoid unwanted “forest of peaks” observed at large travel speed in the millimeter-per-second range. Initially, a PCM with integrated resistors for electrothermal actuation (ETA) was designed, built, and tested. Here, the ETA can be performed with a piezoresistive Wheatstone bridge, which converts mechanical strain into electrical signals by boron diffusion in order to simplify the production process. Moreover, a new substrate contact has been added in the new design for an AC voltage supply for the Wheatstone bridge to reduce parasitic signal influence via the EAM (Electromechanical Amplitude Modulation) in our homemade CRI system. Measurements on a bulk Al sample show the expected force dependence of the CR frequency. Meanwhile, fitting of the measured contact-resonance spectra was applied based on a Fano-type line shape to reveal the material-specific signature of a single harmonic resonator. However, noise is greatly increased with the bending mode and contact force increasing on viscoelastic samples. Then, to avoid unspecific peaks remaining in the spectra of soft samples, cantilevers with integrated piezoelectric actuators (PEAs) were designed. The numbers and positions of the actuators were optimized for specific CR vibration modes using analytical modeling of the cantilever bending based on the transfer-matrix method and Hertzian contact mechanics. To confirm the design of the PCM with a PEA, finite element analysis (FEA) of CR probing of a sample with a Young’s modulus of 10 GPa was performed. Close agreement was achieved by Fano-type line shape fitting of amplitude and phase of the first four vertical bending modes of the cantilever. As an important structure of the PCM with a PEA, the piezoresistive Wheatstone bridge had to have suitable doping parameters adapted to the boundary conditions of the manufacturing process of the newly designed PCM. Full article
(This article belongs to the Section Sensor Materials)
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<p>Contact-resonance imaging (CRI) system based on a piezoresistive cantilever microprobe (PCM) with an integrated actuator (electrothermal actuator, ETA or piezoelectric actuator, PEA). The homemade electronic system comprises an ADC (Analog-to-digital converter), two DDSs (Direct Digital Synthesizers), a VGA (Variable Gain Amplifier), a DAC (Digital-to-analog converter), an EAM (Electromechanical Amplitude Modulation), a PLL (Phase-Locked-Loop), an AGC (Automatic Gain Control), an FCL (Force Control Loop), an SPI (Serial Peripheral Interface), and a PC (Personal Computer).</p>
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<p>Schematic of electrothermal-actuated (<b>a</b>) and piezoelectric-actuated (<b>b</b>) piezoresistive microprobe (ETA-PCM and PEA-PCM).</p>
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<p>Interaction between the probe tip of a PCM and the sample surface of a viscoelastic material. Both lateral and vertical forces (relative to the surface orientation of the sample) are taken into account. Elastic behavior is modeled by vertical and lateral contact stiffness <math display="inline"><semantics> <mrow> <msup> <mrow> <mi>k</mi> </mrow> <mrow> <mo>*</mo> </mrow> </msup> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>k</mi> </mrow> <mrow> <mi>L</mi> <mi>a</mi> <mi>t</mi> </mrow> <mrow> <mo>*</mo> </mrow> </msubsup> </mrow> </semantics></math>, viscous behavior is modeled by vertical and lateral contact damping <math display="inline"><semantics> <mrow> <msup> <mrow> <mi>γ</mi> </mrow> <mrow> <mo>*</mo> </mrow> </msup> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mi>γ</mi> </mrow> <mrow> <mi>L</mi> <mi>a</mi> <mi>t</mi> </mrow> <mrow> <mo>*</mo> </mrow> </msubsup> </mrow> </semantics></math>.</p>
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<p>Measured spectral line shapes of amplitude (<b>upper</b>) and phase (<b>lower</b>) around resonance before (<b>a</b>) and after removing a Fano-resonance distortion (<b>b</b>).</p>
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<p>Eigenforms (<b>a</b>) of the third vertical bending mode and related strain distribution (<b>b</b>) along the surface of the cantilever (<a href="#sensors-25-00332-t001" class="html-table">Table 1</a>) are calculated using the described cantilever vibration model under varied contact stiffness. The angle of attack and the probing force are 0° and 10 µN, respectively. The optimal positions of the heaters are indicated by the purple and green bars, respectively. <span class="html-italic">u</span> is the position along the cantilever axis in the rotated coordinate system (see <a href="#sensors-25-00332-f0A3" class="html-fig">Figure A3</a>).</p>
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<p>Manufacturing process of a PCM with integrated thermoelectric actuators.</p>
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<p>Bottom-side view of a fabricated PCM with an integrated ETA (top side, not visible here) and a glued diamond tip at the bottom side.</p>
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<p>CR-measurements in the first (<b>a</b>) and second (<b>b</b>) modes using a PCM with integrated ETA and a diamond tip in contact with bulk Al (at a tilt angle of 0° and an actuation voltage of AC<sub>peak</sub>/DC = 2.5 V/2.5 V). The Wheatstone bridge is operated using an AC<sub>peak</sub> supply of 10 V at 2 MHz (<b>a</b>) or 3 MHz (<b>b</b>). The contact forces are 50 µN/365 µN (<b>a</b>) and &gt;1 mN (<b>b</b>). The light-colored circle points are measured via our homemade CRI setup. The superimposed lines are obtained by fitting using a Fano-resonance line shape (Equation (22)).</p>
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<p>CR frequency and <span class="html-italic">Q</span> factor of the first mode using a PCM with integrated ETA and diamond tip in contact with a PnBMA layer on glass [<a href="#B72-sensors-25-00332" class="html-bibr">72</a>,<a href="#B73-sensors-25-00332" class="html-bibr">73</a>].</p>
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<p>Amplitude and phase of the first CR mode with the PnBMA layer on glass using EAM of the Wheatstone bridge with an AC frequency of 2 MHz and a peak voltage of 10 V showing unidentified peaks around the fundamental CR mode.</p>
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<p>Strain along the surface of the cantilever in the eigenforms of the (<b>a</b>) first, (<b>b</b>) second, (<b>c</b>) third, and (<b>d</b>) fourth vertical bending mode, calculated for a diamond-tip sensor with contact stiffness between 0 and 100 kNm<sup>−1</sup> and contact damping between 0 and 1 mNsm<sup>−1</sup>. The blue bars indicate the optimum positions and polarities of the actuators.</p>
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<p>Finite element analysis (FEA) of the frequency response of a PCM with integrated piezo actuators positioned for preferential excitation of the first four vertical bending modes of the cantilever in contact with a sample of Young’s modulus of 10 GPa at angle of attack of 0°. The simulation results (light-colored circles) obtained by FEA of the first (<b>a</b>), second (<b>b</b>), third (<b>c</b>), and fourth (<b>d</b>) bending modes fitted using a Fano-resonance line shape are shown as colored lines (Equation (22)).</p>
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<p>The electrically active dopant concentration profile of (<b>a</b>) boron dopant (PBF2.2DS, Filmtronics, Butler, PA, USA) and (<b>b</b>) phosphorus (P509, Filmtronics, Butler, PA, USA) in <span class="html-italic">n</span>-type silicon (100) (resistivity: 1–10 Ohm-cm, Siegert Wafer, Germany) at different processing temperatures for 30 min, in dependence on depth from the top surface. The solid dots are the experiment data measured using electrochemical capacitance-voltage (ECV) profiling. The solid lines are fits based on a series of Gaussian normal distributions to the experiment data (Equation (23)).</p>
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<p>Dopant concentration profiles in silicon fabricated by boron diffusion at 1000 °C before and after two subsequent thermal oxidation steps for 105 min at 1100 °C. The filled circles are the experiment data from ECV. The solid lines are fits based on a series of Gaussian normal distributions to the experiment data by Equation (23). The fitting parameters are shown in <a href="#sensors-25-00332-t0A4" class="html-table">Table A4</a> in <a href="#app8-sensors-25-00332" class="html-app">Appendix H</a>.</p>
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<p>Fabrication process of a PCM with piezoelectric actuators.</p>
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<p>Deformation of an isotropic elastic body under applied normal force. (<b>a</b>) Body without external force, (<b>b</b>) Body with longitudinally applied normal force, (<b>c</b>) Body with transversely applied normal force.</p>
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<p>Circuit diagram of a Wheatstone bridge.</p>
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<p>A sensor at angle of attack <span class="html-italic">θ</span> between the cantilever and a sample surface is deflected at its probe tip with the force <span class="html-italic">F</span>. (<b>a</b>) This leads to a deflection of <span class="html-italic">δ</span> in the direction of the force and to a deflection of <span class="html-italic">δ</span><sub>Lat</sub> perpendicular to the force. The resting position of the beam is shown by a dashed contour, the deflected shape by a filled area [<a href="#B55-sensors-25-00332" class="html-bibr">55</a>]. (<b>b</b>) The applied force generates a transverse force <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>m</mi> </mrow> </msub> <mfenced separators="|"> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> <mo>+</mo> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mn>1</mn> </mrow> </msub> </mrow> </mfenced> <mo>=</mo> <mi>F</mi> <mi>c</mi> <mi>o</mi> <mi>s</mi> <mi>θ</mi> </mrow> </semantics></math> and a bending moment <math display="inline"><semantics> <mrow> <mi>M</mi> <mfenced separators="|"> <mrow> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> <mo>+</mo> <msub> <mrow> <mi>L</mi> </mrow> <mrow> <mn>1</mn> </mrow> </msub> </mrow> </mfenced> <mo>=</mo> <mi>F</mi> <mi>D</mi> <mi>s</mi> <mi>i</mi> <mi>n</mi> <mi>θ</mi> </mrow> </semantics></math> in the beam at the position of the probe tip.</p>
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<p>Shear force <span class="html-italic">Q<sub>m</sub></span>, the bending moment <span class="html-italic">M</span> and the mechanical stress <span class="html-italic">σ</span> in the bend beam.</p>
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<p>Position of the contact point of the deflected probe tip.</p>
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<p>Layout of PCM with integrated PEAs.</p>
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<p>Layout of PCM with integrated PEAs.</p>
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<p>Bock diagram of used modules of COMSOL Multiphysics 5.4 for FEA.</p>
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<p>The resistance measured by four-point probing (FPP) of (<b>a</b>) boron dopant (PBF2.2DS, Filmtronics, Butler, PA, USA) and (<b>b</b>) phosphorus (P509, Filmtronics, Butler, PA, USA) diffusion profiles in <span class="html-italic">n</span>-type silicon (100) at different processing temperatures for 30 min. The blue points, circles and triangles describe the resistance values measured at three different locations on the sample. The red symbols describe the residues of each measurement with respect to the average value at each temperature.</p>
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<p>Sheet conductance of boron (<b>a</b>) (PBF2.2DS, Filmtronics, Butler, PA, USA) and (<b>b</b>) phosphorus (P509, Filmtronics, Butler, PA, USA) dopants in <span class="html-italic">n</span>-type silicon (100) at different doping temperatures. The blue triangles depict data from the supplier. The blue circles and asterisks depict data calculated from ECV [<a href="#B73-sensors-25-00332" class="html-bibr">73</a>] and FPP, respectively (<a href="#sensors-25-00332-t0A5" class="html-table">Table A5</a> and <a href="#sensors-25-00332-t0A6" class="html-table">Table A6</a>). The lines are exponential fits of Equation (26), and the fitting parameters are shown in <a href="#sensors-25-00332-t004" class="html-table">Table 4</a>.</p>
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25 pages, 3804 KiB  
Article
Abnormal Operation Detection of Automated Orchard Irrigation System Actuators by Power Consumption Level
by Shahriar Ahmed, Md Nasim Reza, Md Rejaul Karim, Hongbin Jin, Heetae Kim and Sun-Ok Chung
Sensors 2025, 25(2), 331; https://doi.org/10.3390/s25020331 - 8 Jan 2025
Viewed by 415
Abstract
Information and communication technology (ICT) components, especially actuators in automated irrigation systems, are essential for managing precise irrigation and optimal soil moisture, enhancing orchard growth and yield. However, actuator malfunctions can lead to inefficient irrigation, resulting in water imbalances that impact crop health [...] Read more.
Information and communication technology (ICT) components, especially actuators in automated irrigation systems, are essential for managing precise irrigation and optimal soil moisture, enhancing orchard growth and yield. However, actuator malfunctions can lead to inefficient irrigation, resulting in water imbalances that impact crop health and reduce productivity. The objective of this study was to develop a signal processing technique to detect potential malfunctions based on the power consumption level and operating status of actuators for an automated orchard irrigation system. A demonstration orchard with four apple trees was set up in a 3 m × 3 m soil test bench inside a greenhouse, divided into two sections to enable independent irrigation schedules and management. The irrigation system consisted of a single pump and two solenoid valves controlled by a Python-programmed microcontroller. The microcontroller managed the pump cycling ‘On’ and ‘Off’ states every 60 s and solenoid valves while storing and transmitting sensor data to a smartphone application for remote monitoring. Commercial current sensors measured actuator power consumption, enabling the identification of normal and abnormal operations by applying threshold values to distinguish activation and deactivation states. Analysis of power consumption, control commands, and operating states effectively detected actuator operations, confirming reliability in identifying pump and solenoid valve failures. For the second solenoid valve in channel 2, with 333 actual instances of normal operation and 60 actual instances of abnormal operation, the model accurately detected 316 normal and 58 abnormal instances. The proposed method achieved a mean average precision of 99.9% for detecting abnormal control operation of the pump and solenoid valve of channel 1 and a precision of 99.7% for the solenoid valve of channel 2. The proposed approach effectively detects actuator malfunctions, demonstrating the potential to enhance irrigation management and crop productivity. Future research will integrate advanced machine learning with signal processing to improve fault detection accuracy and evaluate the scalability and adaptability of the system for larger orchards and diverse agricultural applications. Full article
(This article belongs to the Special Issue Sensors in Smart Irrigation Systems)
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Figure 1

Figure 1
<p>Experimental setup: (<b>a</b>) schematic diagram of the demonstration orchard with the irrigation system setup, (<b>b</b>) the test bench with soil, (<b>c</b>) drip irrigation system, and (<b>d</b>) watering area and emitter positions.</p>
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<p>Installation of sensors in the demonstration orchard: (<b>a</b>) wet soil addition for soil water potential measurement, (<b>b</b>) placement of soil water content and water potential sensors, and (<b>c</b>) placement of leaf temperature sensor.</p>
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<p>Sensor interfacing for measuring actuator power consumption using current sensors: (<b>a</b>) circuit diagram, and (<b>b</b>) sensors installation with the microcontroller.</p>
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<p>Irrigation control and data acquisition system: (<b>a</b>) schematic diagram of the sensor interfacing with the primary and secondary MCUs, and (<b>b</b>) data acquisition flow from the demonstration orchard.</p>
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<p>Schematic diagram of MQTT communication protocol between the irrigation systems and smartphone application.</p>
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<p>Overall, signal processing and anomaly detection workflow were used in this study.</p>
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<p>Real-time signal processing for estimating power consumption: (<b>a</b>) flowchart of the signal processing and power calculation, (<b>b</b>) low-pass filter application, and (<b>c</b>) signal amplification and offset value deduction.</p>
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<p>Detailed processing steps for detecting abnormal operation: (<b>a</b>) schematic diagram of abnormal operation detection, (<b>b</b>) visualization of threshold values on measured power, (<b>c</b>) classification of operating states after applying threshold values, (<b>d</b>) comparison of classified states with given control commands, and (<b>e</b>) performance evaluation by comparing detected operation with ground truth.</p>
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<p>Onsite monitoring of the irrigation system using secondary MCU: (<b>a</b>) monitoring in Raspberry Pi display and (<b>b</b>) monitoring in VNC viewer.</p>
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<p>Remote monitoring of the irrigation system on the Android application.</p>
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<p>Variation in the sensor data after irrigation control: (<b>a</b>) soil water potential, (<b>b</b>) soil water content, and (<b>c</b>) leaf temperature.</p>
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<p>Histogram analysis of power consumption behavior of the pump: (<b>a</b>) threshold value application using Min–Max and manual approaches, (<b>b</b>) performance of Min–Max threshold approach, and (<b>c</b>) performance of manual threshold approaches.</p>
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<p>Histogram analysis of power consumption behavior of the valve: (<b>a</b>) threshold value application using Min–Max and manual approaches, (<b>b</b>) performance of Min–Max threshold approach, and (<b>c</b>) performance of manual threshold approaches.3.3. Detecting Abnormal Operation of the Actuators.</p>
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<p>Precision–recall curve of the abnormal operation detection model.</p>
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<p>The low-pass filter was applied to the collected raw signal of the valve during lab conditions.</p>
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26 pages, 6106 KiB  
Article
Design of an Adaptive Fixed-Time Fast Terminal Sliding Mode Controller for Multi-Link Robots Actuated by Pneumatic Artificial Muscles
by Hesam Khajehsaeid, Ali Soltani and Vahid Azimirad
Biomimetics 2025, 10(1), 37; https://doi.org/10.3390/biomimetics10010037 - 8 Jan 2025
Viewed by 369
Abstract
Pneumatic artificial muscles (PAMs) are flexible actuators that can be contracted or expanded by applying air pressure. They are used in robotics, prosthetics, and other applications requiring flexible and compliant actuation. PAMs are basically designed to mimic the function of biological muscles, providing [...] Read more.
Pneumatic artificial muscles (PAMs) are flexible actuators that can be contracted or expanded by applying air pressure. They are used in robotics, prosthetics, and other applications requiring flexible and compliant actuation. PAMs are basically designed to mimic the function of biological muscles, providing a high force-to-weight ratio and smooth, lifelike movement. Inflation and deflation of these muscles can be controlled rapidly, allowing for fast actuation. In this work, a continuum mechanics-based model is developed to predict the output parameters of PAMs, like actuation force. Comparison of the model results with experimental data shows that the model efficiently predicts the mechanical behaviour of PAMs. Using the actuation force–air pressure–contraction relation provided by the proposed mechanical model, a dynamic model is derived for a multi-link PAM-actuated robot manipulator. An adaptive fixed-time fast terminal sliding mode control is proposed to track the desired joint position trajectories despite the model uncertainties and external disturbances with unknown magnitude bounds. Furthermore, the performance of the proposed controller is compared with an adaptive backstepping fast terminal sliding mode controller through numerical simulations. The simulations show faster convergence and more precise tracking for the proposed controller. Full article
(This article belongs to the Special Issue Bioinspired Structures for Soft Actuators: 2nd Edition)
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Figure 1
<p>(<b>Left</b>) The designed PAM and (<b>Right</b>) the rest and deformed states.</p>
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<p>Schematic representation of a PAM and a single thread.</p>
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<p>Free-body diagram of a pneumatic artificial muscle.</p>
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<p>Antagonistic joint actuation by a pair of PAMs.</p>
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<p>The Neo-Hookean model in comparison with the uniaxial tensile test data.</p>
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<p>Pressure–contraction curve, comparison of the test data with the model results.</p>
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<p>Actuation force–contraction curve at different air pressures.</p>
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<p>A two-link robot manipulator actuated by PAMs.</p>
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<p>Joint angles of the manipulator.</p>
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<p>Tracking errors of the joints.</p>
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<p>Time responses of the adaptive gains.</p>
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<p>Time responses of the adaptive gains.</p>
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<p>Time response of <math display="inline"><semantics> <mrow> <msub> <mi>w</mi> <mi>d</mi> </msub> </mrow> </semantics></math>.</p>
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<p>Pressure variations in the muscles.</p>
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<p>Actuation forces of the muscles.</p>
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<p>Actuation forces of the muscles.</p>
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<p>Pressure variation in the muscles of the first joint with <math display="inline"><semantics> <mrow> <msub> <mi>P</mi> <mn>0</mn> </msub> <mo>=</mo> <mn>200</mn> <mo> </mo> <mi>kPa</mi> </mrow> </semantics></math>.</p>
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<p>Actuation forces of the muscles with <math display="inline"><semantics> <mrow> <msub> <mi>P</mi> <mn>0</mn> </msub> <mo>=</mo> <mn>400</mn> <mo> </mo> <mi>kPa</mi> </mrow> </semantics></math>.</p>
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