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Keywords = wheel hub motor

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17 pages, 9712 KiB  
Article
Oil Cooling Method for Internal Heat Sources in the Outer Rotor Hub Motor of ElectricVehicle and Thermal Characteristics Research
by Fulai Guo and Chengning Zhang
Energies 2024, 17(24), 6312; https://doi.org/10.3390/en17246312 - 14 Dec 2024
Viewed by 530
Abstract
The heat dissipation of wheel hub motors is difficult due to the limited installation space and harsh working environment, which will lead to an increase in the operating temperature of the motor. Excessive motor temperature will limit the further increase in the power [...] Read more.
The heat dissipation of wheel hub motors is difficult due to the limited installation space and harsh working environment, which will lead to an increase in the operating temperature of the motor. Excessive motor temperature will limit the further increase in the power density and torque density of the motor. Taking the outer rotor hub motor as the research object, a heat dissipation structure is designed by passing oil through the stator core, slot wedge, and the motor end, mainly the cooling stator core, slot winding, and the end winding from inside of the motor. The internal heat is mainly carried away through lubricating oil by convective heat transfer and heat conduction. The heat distribution model of the motor based on the new cooling structure is established using the centralized parameter heat network method. The Motor-CAD software is used to build the motor 3d model and simulate the motor temperature field, and the temperature distribution in the motor under the rated working condition is analyzed. The temperature rising test of the motor prototype are performed on a bench built in the laboratory. The experimental results are consistent with the simulation results of the temperature field, which verify the rationality of the model. Full article
(This article belongs to the Section E: Electric Vehicles)
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Figure 1
<p>CAD drawing of the oil-cooled hub motor.</p>
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<p>Oil flow diagram of the oil-cooled hub motor.</p>
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<p>3D model drawing of hub oil-cooled motor.</p>
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<p>Motor heat generation and transfer path diagram.</p>
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<p>Overall thermal circuit diagram of the motor.</p>
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<p>Schematic diagram of geometric dimensions of motor teeth.</p>
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<p>Equivalent diagram of stator slot winding.</p>
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<p>Oil shield thermal resistance network.</p>
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<p>Cross-section temperature profile of the oil-cooled motor.</p>
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<p>Temperature distribution diagram of the axial section of the oil-cooled motor.</p>
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<p>Temperature distribution diagram of the water-cooled motor.</p>
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<p>Temperature distribution diagram of the axial section of the oil-cooled motor.</p>
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<p>Temperature distribution diagram of the axial section of the oil-cooled motor.</p>
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<p>Motor prototype.</p>
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<p>Test diagram of the oil-cooled motor bench.</p>
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<p>One-hour temperature increase curve of the oil-cooled motor.</p>
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<p>One-hour temperature increase curve of the oil-cooled motor and water-cooled motor.</p>
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47 pages, 21655 KiB  
Article
Analysis of the Selected Design Changes in a Wheel Hub Motor Electromagnetic Circuit on Motor Operating Parameters While Car Driving
by Piotr Dukalski and Roman Krok
Energies 2024, 17(23), 6091; https://doi.org/10.3390/en17236091 - 3 Dec 2024
Viewed by 553
Abstract
The drive system of an electric car must meet road requirements related to overcoming obstacles and driving dynamics depending on the class and purpose of the vehicle. The driving dynamics of modern cars as well as size and weight limitations mean that wheel [...] Read more.
The drive system of an electric car must meet road requirements related to overcoming obstacles and driving dynamics depending on the class and purpose of the vehicle. The driving dynamics of modern cars as well as size and weight limitations mean that wheel hub motors operate with relatively high current density and high power supply frequency, which may generate significant power losses in the windings and permanent magnets and increase their operating temperature. Designers of this type of motor often face the need to minimize the motor’s weight, as it constitutes the unsprung mass of the vehicle. Another limitation for motor designers is the motor dimensions, which are limited by the dimensions of the rim, the arrangement of suspension elements and the braking system. The article presents two directions in the design of wheel hub motors. The first one involves minimizing the length of the stator magnetic core, which allows for shortening of the axial dimension and mass of the motor but involves increasing the thermal load and the need for deeper de-excitation. The second one involves increasing the number of pairs of magnetic poles, which reduces the mass, increases the internal diameter of the motor and shortens the construction of the fronts, but is associated with an increase in the motor operating frequency and increased power losses. Additionally, increasing the number of pairs of magnetic poles is often associated with reducing the number of slots per pole and the phase for technological reasons, which in turn leads to a greater share of spatial harmonics of the magnetomotive force in the air gap and may lead to the generation of higher power losses and higher operating temperatures of permanent magnets. The analysis is based on a simulation of the motor operation, modeled on the basis of laboratory tests of the prototype, while the car is driving in various driving cycles. Full article
(This article belongs to the Special Issue Energy, Electrical and Power Engineering: 3rd Edition)
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Figure 1
<p>Models: The cross-section of the disassembled three-dimensional (3D) model of the SMzs200S32 motor, manufactured by Łukasiewicz Research Network—Upper Silesian Institute of Technology (Gliwice, Poland), and dedicated for assembly in the wheel hub of a car: 1—rotor, 2—rotor’s magnetic core, 3—magnet, 4—stator’s magnetic core, 5—stator winding coil ends, 6—resin, 7—permanent anchoring shield, 8—supporting structure, 9—casing with coolant ducts, 10—radiator of winding end, at drive end, 11—radiator of winding end, at non-drive side, 12—brake drum, 13—bearing assembly, 14—entry for supply wires, 15—cooling system ports, 16—rotor assembly openings, 17—stator assembly openings.</p>
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<p>Electromagnetic circuit model of the motor in the ANSYS Motor CAD program. (<b>a</b>) model cross-section, (<b>b</b>) longitudinal section, (<b>c</b>) FEM mesh, (<b>d</b>) calculated distribution of induction from magnets.</p>
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<p>Laboratory determined no-load losses of the SMzs200S32 motor during generator operation and during motor operation and drive power supply with <span class="html-italic">U</span><sub>DC</sub> = 350 V.</p>
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<p>Determined power losses in the magnetic core of motor, based on the measured no-load characteristics and the characteristic calculated in the ANSYS Motor CAD program.</p>
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<p>Mechanical losses of the SMzs200S32, measured in the laboratory and calculated in the simulation model.</p>
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<p>Thermal model of the motor in ANSYS Motor CAD.</p>
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<p>Cross-section of the SMzs200S32 prototype motor. Location of PT-100 temperature sensors in motor: 1—winding in slot, ND side, 2—winding in slot, D side, 3—zero point of the winding, 4—ND-side windings, 5—D-side windings, 6—D-side windings, 7—ND-side windings, 8—winding end D-side radiator, 9—winding end ND-side radiator, 10—D-side radiator element, 11—ND-side radiator element, 12—coolant inlet, 13—water outlet, 14—permanent magnets. ND—non-drive; D—drive.</p>
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<p>Prototype of SMzs200S32 motor: (<b>a</b>) in laboratory, (<b>b</b>) with wheel rim.</p>
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<p>Arrangement of temperature sensors: (<b>a</b>) on the magnet, (<b>b</b>) in the slot (top of the slot), (<b>c</b>) temperature sensor terminals from the winding fronts, (<b>d</b>) temperature sensor terminals from the stator core (top of the tooth) and (<b>e</b>) stator core temperature sensor (bottom of the tooth/stator yoke).</p>
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<p>Calculated steady temperatures for the motor operating point: <span class="html-italic">T</span><sub>m</sub> = 400 N·m, <span class="html-italic">n</span> = 950 rpm. (<span class="html-italic">V</span> = 105 km/h), <span class="html-italic">T</span><sub>ot.</sub> = 18 °C, coolant = 15.3 °C, <span class="html-italic">q</span> = 10 L/min.</p>
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<p>Comparison of calculated winding temperatures in the slot with measured temperatures at the test stand. <span class="html-italic">T</span><sub>m</sub> = 400 N·m, <span class="html-italic">n</span> = 950 rpm. (<span class="html-italic">V</span> = 105 km/h), <span class="html-italic">T</span><sub>ambient</sub> = 18 °C, <span class="html-italic">T</span><sub>Coolant</sub> = 15.3 °C, <span class="html-italic">q</span> = 10 L/min.</p>
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<p>Comparison of calculated winding end temperatures in the slot with measured temperatures at the test stand. <span class="html-italic">T</span><sub>m</sub> = 400 N·m, <span class="html-italic">n</span> = 950 rpm. (<span class="html-italic">V</span> = 105 km/h), <span class="html-italic">T</span><sub>ambient</sub> = 18 °C, <span class="html-italic">T</span><sub>Coolant</sub> = 15.3 °C, <span class="html-italic">q</span> = 10 L/min.</p>
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<p>Comparison of calculated stator tooth temperatures in the slot with measured temperatures at the test stand. <span class="html-italic">T</span><sub>m</sub> = 400 N·m, <span class="html-italic">n</span> = 950 rpm. (<span class="html-italic">V</span> = 105 km/h), <span class="html-italic">T</span><sub>ambient</sub> = 18 °C, <span class="html-italic">T</span><sub>Coolant</sub> = 15.3 °C, <span class="html-italic">q</span> = 10 L/min.</p>
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<p>Comparison of calculated magnet temperatures in the slot with measured temperatures at the test stand. <span class="html-italic">T</span><sub>m</sub> = 400 N m, <span class="html-italic">n</span> = 950 rpm. (<span class="html-italic">V</span> = 105 km/h), <span class="html-italic">T</span><sub>ambient</sub> = 18 °C, <span class="html-italic">T</span><sub>Coolant</sub> = 15.3 °C, <span class="html-italic">q</span> = 10 L/min.</p>
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<p>Comparison of calculated winding end radiator temperatures in the slot with measured temperatures at the test stand. <span class="html-italic">T</span><sub>m</sub> = 400 N m, <span class="html-italic">n</span> = 950 rpm. (<span class="html-italic">V</span> = 105 km/h), <span class="html-italic">T</span><sub>ambient</sub> = 18 °C, <span class="html-italic">T</span><sub>Coolant</sub> = 15.3 °C, <span class="html-italic">q</span> = 10 L/min.</p>
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<p>Calculated course of the required motor torque in a Nissan Leaf vehicle with dual-wheel drive, running in the driving cycle: (<b>a</b>) Artemis Urban, (<b>b</b>) Artemis Motorway 150, (<b>c</b>) US06 (motor share factor in braking torque 0.25).</p>
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<p>Calculated characteristics of maximum motor torques for different magnetic core lengths with plotted maximum torques occurring for the considered Nissan Leaf car model for the Artemis Urban, Artemis Motorway 150 and US06 driving cycles.</p>
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<p>Calculated temperature profile of individual motor components (for three core lengths) in the considered Nissan Leaf car with dual-motor drive, running in the Artemis Urban driving cycle repeated 5 times (braking torque participation factor 0.25): (<b>a</b>) maximum winding temperature, (<b>b</b>) magnet temperature, (<b>c</b>) stator magnetic core temperature.</p>
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<p>Calculated course of motor power losses (for three core lengths) in the considered Nissan Leaf car with dual-motor in-wheel drive, moving in the Artemis Urban driving cycle: (<b>a</b>) in the winding, (<b>b</b>) in the magnets, (<b>c</b>) in the stator magnetic core.</p>
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<p>Calculated course of temperatures of individual motor components in the considered Nissan Leaf car with dual-motor drive in the Artemis Motorway 150 driving cycle repeated 5 times (motor participation factor in braking moment 0.25). Courses for three lengths of magnetic cores: (<b>a</b>) maximum winding temperature, (<b>b</b>) magnet temperature, (<b>c</b>) stator magnetic core temperature.</p>
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<p>Calculated course of motor power losses in the considered Nissan Leaf car with dual-motor drive in the Artemis Motorway 150 driving cycle: (<b>a</b>) in the winding, (<b>b</b>) in the magnets, (<b>c</b>) in the stator magnetic core.</p>
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<p>Calculated temperature course of individual motor components in the considered Nissan Leaf car with a drive with two motors in the wheels, moving in the US06 driving cycle repeated 5 times (motor participation coefficient at the moment of braking 0.25). Waveforms for three lengths of magnetic cores: (<b>a</b>) maximum winding temperature, (<b>b</b>) magnet temperature, (<b>c</b>) stator magnetic core temperature.</p>
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<p>The course of individual losses of the electromagnetic circuit of the motor in the considered Nissan Leaf car during a drive with two motors in the wheels, moving in the US06 driving cycle repeated 5 times (motor participation coefficient at the moment of braking 0.25). Waveforms for three lengths of magnetic cores: (<b>a</b>) in the winding, (<b>b</b>) in the magnets, (<b>c</b>) in the stator magnetic core.</p>
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<p>Calculated characteristics of maximum torque as a function of rotational speed of the modeled motor and the motor with an increased number of pole pairs (2<span class="html-italic">p</span> = 56 and <span class="html-italic">q</span> = 0.375).</p>
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<p>Distribution of magnetic induction from permanent magnets of the considered motor model: <span class="html-italic">Q</span> = 48, 2<span class="html-italic">p</span> = 32, <span class="html-italic">q</span> = 0.5.</p>
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<p>Distribution of magnetic induction from permanent magnets of the considered motor model <span class="html-italic">Q</span> = 63, 2<span class="html-italic">p</span> = 56, <span class="html-italic">q</span> = 0.375.</p>
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<p>Motor model cross-sections: (<b>a</b>) cross section of the model 2<span class="html-italic">p</span> = 32, <span class="html-italic">q</span> = 0.5; (<b>b</b>) cross section of the model 2<span class="html-italic">p</span> = 56, <span class="html-italic">q</span> = 0.375. (<b>c</b>) longitudinal section of the model 2<span class="html-italic">p</span> = 32, <span class="html-italic">q</span> = 0.5. (<b>d</b>) longitudinal section of the model 2<span class="html-italic">p</span> = 56, <span class="html-italic">q</span> = 0.375.</p>
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<p>Calculated temperature curves of individual motor components in the considered Nissan Leaf car with dual-motor drive, running in the Artemis Urban driving cycle repeated 5 times (braking torque participation factor 0.25): (<b>a</b>) maximum winding, (<b>b</b>) magnet, (<b>c</b>) stator magnetic core.</p>
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<p>Calculated motor power loss curves for a Nissan Leaf with dual-wheel drive, running in the Artemis Urban driving cycle: (<b>a</b>) winding, (<b>b</b>) magnet, (<b>c</b>) stator magnetic core.</p>
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<p>Calculated temperature curves of individual motor components in the considered Nissan Leaf car with dual-motor drive, running in the Artemis Motorway 150 driving cycle repeated 5 times (braking torque participation factor 0.25): (<b>a</b>) maximum winding, (<b>b</b>) magnet, (<b>c</b>) stator magnetic core.</p>
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<p>Calculated motor power loss curves for the considered Nissan Leaf vehicle with dual-motor in-wheel drive, operating in the Artemis Motorway 150 driving cycle: losses in (<b>a</b>) winding, (<b>b</b>) magnets, (<b>c</b>) stator magnetic core.</p>
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<p>Calculated temperature curves of individual motor components in the considered Nissan Leaf car with dual-motor drive, running in the US06 driving cycle repeated 5 times (braking torque participation factor 0.25): (<b>a</b>) maximum winding, (<b>b</b>) magnet, (<b>c</b>) stator magnetic core.</p>
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<p>Calculated power loss curves of the motor in the considered Nissan Leaf car with a dual-motor drive, moving in the US06 driving cycle repeated 5 times (motor participation factor in the braking moment 0.25): (<b>a</b>) in the winding, (<b>b</b>) in the magnets, (<b>c</b>) in the stator magnetic core.</p>
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19 pages, 7127 KiB  
Article
Refinement of Control Strategies for Wheel-Fan Systems in High-Speed Air-Floating Vehicles Operating in Atmospheric Pressure Pipelines
by Kun Zhang, Bin Jiao, Yuliang Bian, Zeming Liu, Tiehua Ma and Changxin Chen
Aerospace 2024, 11(12), 974; https://doi.org/10.3390/aerospace11120974 - 26 Nov 2024
Viewed by 484
Abstract
This study explored the optimization of control systems for atmospheric pipeline air-floating vehicles traveling at ground level by introducing a novel composite wheel-fan system that integrates both wheels and fans. To evaluate the control impedance, the system simulates road conditions like inclines, uneven [...] Read more.
This study explored the optimization of control systems for atmospheric pipeline air-floating vehicles traveling at ground level by introducing a novel composite wheel-fan system that integrates both wheels and fans. To evaluate the control impedance, the system simulates road conditions like inclines, uneven surfaces, and obstacles by using fixed, random, and high torque settings. The hub motor of the wheel fan is managed through three distinct algorithms: PID, fuzzy PID, and the backpropagation neural network (BP). Each algorithm’s control strategy is outlined, and tracking experiments were conducted across straight, circular, and curved trajectories. Analysis of these experiments supports a hybrid control approach: initiating with fuzzy PID, employing the PID algorithm on straight paths, and utilizing the BP neural network for sinusoidal and circular paths. The adaptive capacity of the BP neural network suggests its potential to eventually supplant the PID algorithm in straight path scenarios over extended testing and operation, ensuring improved control performance. Full article
(This article belongs to the Section Aeronautics)
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<p>Schematic diagram of the position of the bottom wheel fan.</p>
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<p>Schematic diagram of the wheel-fan structure.</p>
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<p>Equivalent coordinate relationship between the center of the experimental mobile platform and the center of the wheel fan.</p>
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<p>Plot of wheel fan versus hub motor coordinates.</p>
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<p>Genetic algorithm, preferably PID, flowchart.</p>
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<p>Diagram of the n–t curve comparison of the original parameter and the first set of optimized parameters.</p>
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<p>Comparison T–t curve diagram of the original parameter and the first set optimization parameters.</p>
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<p>The curve relationship diagram of the original parameters Iabc-t.</p>
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<p>The curve relationship diagram of the first set of optimization parameters Iabc-t.</p>
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<p>The n–t curve comparison chart of the original parameter and the second set of optimized parameters.</p>
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<p>The T–t curve comparison chart of the original parameter and the second set of optimized parameters.</p>
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<p>The curve relationship diagram of the second set of optimized parameters Iabc-t.</p>
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<p>PID control algorithm schematic diagram.</p>
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<p>PID algorithm embedded software design flow.</p>
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<p>Vague adaptive PID box diagram.</p>
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<p>Blog controller frame diagram.</p>
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<p>Fuzzy PID operation flowchart of the hub motor wheel-to-wheel experimental mobile platform.</p>
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<p>Schematic of neural network.</p>
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<p>Flow of BP neural network algorithm in the embedded system.</p>
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<p>Test plot of impedance for two parameters.</p>
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<p>Comparison of the three algorithms tested in the driving condition of the straight line test.</p>
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<p>Comparison of the test results of the three algorithms in the driving condition of the circular test.</p>
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<p>Comparison of the test results of the three algorithms under the driving condition of the curve test.</p>
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<p>Comparison of the time spent by the three algorithms.</p>
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21 pages, 5339 KiB  
Article
Design and Stability Analysis of Six-Degree-of-Freedom Hydro-Pneumatic Spring Wheel-Leg
by Zhibo Wu, Bin Jiao, Chuanmeng Sun, Zezhou Xin, Yinzhi Jia and Heming Zhao
Appl. Sci. 2024, 14(21), 9815; https://doi.org/10.3390/app14219815 - 27 Oct 2024
Viewed by 730
Abstract
Traditional hydro-pneumatic spring suspensions are limited to a single vertical degree of freedom, which cannot accommodate the significant technological changes introduced by the new in-wheel motor drive mode. Integrating the motor into the vehicle’s hub creates a direct motor drive mode, replacing the [...] Read more.
Traditional hydro-pneumatic spring suspensions are limited to a single vertical degree of freedom, which cannot accommodate the significant technological changes introduced by the new in-wheel motor drive mode. Integrating the motor into the vehicle’s hub creates a direct motor drive mode, replacing the traditional engine–transmission–drive shaft configuration. Together with the dual in-wheel motor wheelset structure, this setup can achieve both drive and differential steering functions. In this study, we designed a six-arm suspension wheel-leg device based on hydro-pneumatic springs, and its structural composition and functional characteristics are presented herein. The external single-chamber hydro-pneumatic springs used in the six-arm structure suspension were analyzed and mathematically modeled, and the nonlinear characteristic curves of the springs were derived. To overcome the instability caused by inconsistent extension lengths of the hydro-pneumatic springs during horizontal steering, the spring correction force, horizontal rotational torque, consistency, and stiffness of the six-degree-of-freedom hydro-pneumatic spring wheel-leg device were analyzed. Finally, with the auxiliary action of tension springs, the rotational torque of the hydro-pneumatic springs and the tension resistance torque of the tension spring counterbalanced each other, keeping the resultant torque on the wheelset at approximately 0 N∙m. The results suggest that the proposed device has excellent self-stabilizing performance and meets the requirements for straight-line driving and differential steering applications. This device provides a new approach for the drive mode and suspension design of the dual in-wheel motor wheelset. Full article
(This article belongs to the Section Transportation and Future Mobility)
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<p>Dual in-wheel motor wheelset unit.</p>
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<p>Dual in-wheel motor wheel-leg system.</p>
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<p>Force analysis of the wheel-leg system under different load directions.</p>
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<p>Force analysis of the wheel-leg system under different load directions.</p>
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<p>Structure of the external single-chamber hydro-pneumatic spring.</p>
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<p>Simulation models of hydro-pneumatic springs.</p>
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<p>Simulation models of hydro-pneumatic springs.</p>
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<p>Characteristic curves of hydro-pneumatic springs.</p>
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<p>Output force curves of hydro-pneumatic springs.</p>
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<p>Schematic of horizontal rotation.</p>
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<p>Simplified model of horizontal rotation for the upper three hydro-pneumatic springs.</p>
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<p>Hydraulic rod force, displacement, and torque curves.</p>
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<p>Hydraulic rod force, displacement, and torque curves.</p>
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<p>Horizontal projection force analysis diagram of the springs.</p>
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<p>Variation curves of the hydro-pneumatic springs’ rotational torque, tension resistance torque, and resultant torque with respect to the rotation angle.</p>
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<p>Variation curves of torques with respect to the rotation angle under spring inconsistency.</p>
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18 pages, 7879 KiB  
Article
Research on an Adaptive Active Suspension Leveling Control Method for Special Vehicles
by Pan Zhang, Huijun Yue, Pengchao Zhang, Jie Gu and Hongjun Yu
Processes 2024, 12(7), 1483; https://doi.org/10.3390/pr12071483 - 15 Jul 2024
Viewed by 1233
Abstract
Adaptive active suspension systems, integral to specialized vehicles, hold significance for their stability and safety. This study introduces a novel adaptive active suspension system featuring four independently controlled wheels employing wheel-hub motors, hydraulic cylinders, pump motor power, controllers, and sensors. A rapid and, [...] Read more.
Adaptive active suspension systems, integral to specialized vehicles, hold significance for their stability and safety. This study introduces a novel adaptive active suspension system featuring four independently controlled wheels employing wheel-hub motors, hydraulic cylinders, pump motor power, controllers, and sensors. A rapid and, within a certain range, leveling and height adjustment control strategy is proposed for this system, utilizing the Kalman filter algorithm. Additionally, the paper examines the front-wheel Ackermann steering model and four-wheel reverse Ackermann transition model to enhance the suspension’s stability. Subsequently, experiments on leveling and height adjustment are conducted, demonstrating the system’s capability to swiftly and accurately rectify the vehicle’s deviation angle within the specified threshold. Following adjustments made by the leveling and height control algorithm, the vehicle body promptly returns to the preset level state and designated height. The leveling control system holds broad applicability in intelligent agriculture, logistics handling, off-road equipment, and other domains, presenting significant practical utility. Full article
(This article belongs to the Section Automation Control Systems)
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<p>Adaptive active suspension system structure.</p>
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<p>Three-dimensional diagram of adaptive active suspension.</p>
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<p>Shrinkage control of a single hydraulic cylinder.</p>
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<p>Several unbalanced-attitude adjustment processes.</p>
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<p>Schematic diagram of automatic leveling control.</p>
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<p>Schematic diagram of front high/rear low leveling control.</p>
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<p>Schematic diagram of front low/rear high leveling control.</p>
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<p>Schematic diagram of left high/right low leveling control.</p>
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<p>Schematic diagram of left low/right high leveling control.</p>
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<p>Schematic diagram of front right corner high leveling control.</p>
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<p>Schematic diagram of front left corner high leveling control.</p>
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<p>Schematic diagram of rear right corner high leveling control.</p>
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<p>Schematic diagram of rear-left corner height leveling control.</p>
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<p>Flowchart of the adaptive active suspension leveling.</p>
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<p>Hydraulic cylinder height adjustment.</p>
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<p>Adaptive active suspension height adjustment flowchart.</p>
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<p>Schematic diagram of active suspension front- and rear-wheel steering.</p>
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<p>Schematic diagram of active suspension with four wheels steering in the same direction and in the opposite direction.</p>
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<p>Ackermann steering model for the front wheels of the active suspension system.</p>
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<p>Ackermann steering model for four-wheel reverse cornering with active suspension.</p>
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<p>Angle data curve of automatic leveling in the high front−right corner state.</p>
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<p>Angle data curve of auto−leveling for the high back−left corner state.</p>
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<p>Angle data curve of auto−leveling for the high front−left corner state.</p>
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<p>Angle data curve for automatic body height leveling.</p>
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29 pages, 8141 KiB  
Article
Synthetic Optimization of Trafficability and Roll Stability for Off-Road Vehicles Based on Wheel-Hub Drive Motors and Semi-Active Suspension
by Xiang Fu, Jiaqi Wan, Daoyuan Liu, Song Huang, Sen Wu, Zexuan Liu, Jijie Wang, Qianfeng Ruan and Tianqi Yang
Mathematics 2024, 12(12), 1871; https://doi.org/10.3390/math12121871 - 15 Jun 2024
Cited by 1 | Viewed by 901
Abstract
Considering the requirements pertaining to the trafficability of off-road vehicles on rough roads, and since their roll stability deteriorates rapidly when turning violently or passing slant roads due to a high center of gravity (CG), an efficient anti-slip control (ASC) method with superior [...] Read more.
Considering the requirements pertaining to the trafficability of off-road vehicles on rough roads, and since their roll stability deteriorates rapidly when turning violently or passing slant roads due to a high center of gravity (CG), an efficient anti-slip control (ASC) method with superior instantaneity and robustness, in conjunction with a rollover prevention algorithm, was proposed in this study. A nonlinear 14 DOF vehicle model was initially constructed in order to explain the dynamic coupling mechanism among the lateral motion, yaw motion and roll motion of vehicles. To acquire physical state changes and friction forces of the tires in real time, corrected LuGre tire models were utilized with the aid of resolvers and inertial sensors, and an adaptive sliding mode controller (ASMC) was designed to suppress each wheel’s slip ratio. In addition, a model predictive controller (MPC) was established to forecast rollover risk and roll moment in reaction to the change in the lateral forces as well as the different ground heights of the opposite wheels. During experimentation, the mutations of tire adhesion capacity were quickly discerned and the wheel-hub drive motors (WHDM) and ASC maintained the drive efficiency under different adhesion conditions. Finally, a hardware-in-the-loop (HIL) platform made up of the vehicle dynamic model in the dSPACE software, semi-active suspension (SAS), a vehicle control unit (VCU) and driver simulator was constructed, where the prediction and moving optimization of MPC was found to enhance roll stability effectively by reducing the length of roll arm when necessary. Full article
(This article belongs to the Special Issue Modeling, Optimization and Control of Industrial Processes)
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Figure 1
<p>Nonlinear 14 DOF vehicle dynamic model. (<b>a</b>) Dynamic model of the vehicle in the XY plane. (<b>b</b>) Dynamic model of the vehicle in the YZ plane. (<b>c</b>) Dynamic model of the vehicle X-Z plane.</p>
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<p>Logic diagram of the vehicle stability control module.</p>
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<p>Sensor systems of real-vehicle experiments.</p>
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<p>Results of the real-vehicle test of the climbing experiment with a standard gradient of 40%. (<b>a</b>) Pitch and roll angles of the carriage. (<b>b</b>) Output torques of the four wheels. (<b>c</b>) Rotation speeds of the four wheels. (<b>d</b>) Slip rates of the four wheels.</p>
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<p>Test results of the climbing experiment with a standard gradient of 60%. (<b>a</b>) Pitch and roll angles of the carriage. (<b>b</b>) Output torques of the four wheels. (<b>c</b>) Rotation speeds of the four wheels. (d) Slip rates of the four wheels.</p>
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<p>Results of cross-axis experiment with the maximum vertical height <math display="inline"><semantics> <mrow> <msub> <mi>h</mi> <mrow> <mi>m</mi> <mi>a</mi> <mi>x</mi> <mn>1</mn> </mrow> </msub> </mrow> </semantics></math>. (<b>a</b>) Pitch and Roll angles of the carriage. (<b>b</b>) Output torques of the four wheels. (<b>c</b>) Rotation speeds of the four wheels.</p>
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<p>Results of cross-axis experiment with the maximum vertical height <math display="inline"><semantics> <mrow> <msub> <mi>h</mi> <mrow> <mi>m</mi> <mi>a</mi> <mi>x</mi> <mn>2</mn> </mrow> </msub> </mrow> </semantics></math>. (<b>a</b>) Pitch and Roll angles of the carriage. (<b>b</b>) Output torques of the four wheels. (<b>c</b>) Rotation speeds of the four wheels. (d) DPUR of the four wheels.</p>
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<p>Results of the acceleration experiment on a low-adhesion road (<math display="inline"><semantics> <mrow> <mi>μ</mi> <mo>≈</mo> <msub> <mi>μ</mi> <mrow> <mi>L</mi> <mi>o</mi> <mi>w</mi> </mrow> </msub> </mrow> </semantics></math>). (<b>a</b>) The measured vehicle velocity under different controllers. (<b>b</b>) SWA under different controllers. (<b>c</b>) Slip rates of the four wheels under the controller ASC AND ODC. (<b>d</b>) Slip rates of the four wheels under the controller ODC. (<b>e</b>) Output torques of the four wheels response to the accelerating demand under the controller ASC AND ODC. (<b>f</b>) Output torques of the response of the four wheels’ response to the accelerating demand under the ODC controller.</p>
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<p>Results of the acceleration experiment on a split road (<math display="inline"><semantics> <mrow> <msub> <mi>μ</mi> <mrow> <mi>L</mi> <mi>e</mi> <mi>f</mi> <mi>t</mi> </mrow> </msub> <mo>≈</mo> <msub> <mi>μ</mi> <mrow> <mi>L</mi> <mi>o</mi> <mi>w</mi> </mrow> </msub> <mo>,</mo> <msub> <mi>μ</mi> <mrow> <mi>R</mi> <mi>i</mi> <mi>g</mi> <mi>h</mi> <mi>t</mi> </mrow> </msub> <mo>≈</mo> <msub> <mi>μ</mi> <mrow> <mi>h</mi> <mi>i</mi> <mi>g</mi> <mi>h</mi> </mrow> </msub> </mrow> </semantics></math>). (<b>a</b>) The vehicle velocity under different controllers. (<b>b</b>) SWA under different controllers. (<b>c</b>) Slip rates of the four wheels under the controller ASC AND ODC. (<b>d</b>) Slip rates of the four wheels under the controller ASC. (<b>e</b>) Output torques of the four wheels response to the accelerating demand under the controller ASC AND ODC. (<b>f</b>) Output torques of the response of the four wheels’ response to the accelerating demand under the ASC controller.</p>
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<p>Results of the acceleration experiment on a road with great <math display="inline"><semantics> <mover accent="true"> <mi>μ</mi> <mo stretchy="false">˙</mo> </mover> </semantics></math> (<math display="inline"><semantics> <mrow> <msub> <mi>μ</mi> <mrow> <mi>h</mi> <mi>i</mi> <mi>g</mi> <mi>h</mi> </mrow> </msub> <mo>→</mo> <msub> <mi>μ</mi> <mrow> <mi>L</mi> <mi>o</mi> <mi>w</mi> </mrow> </msub> </mrow> </semantics></math>). (<b>a</b>) The measured vehicle velocity and SWA under the controller ASC AND ODC. (<b>b</b>) Slip rates of the four wheels under the controller ASC AND ODC. (<b>c</b>) Output torques of the four wheels response to the accelerating demand under the controller ASC AND ODC.</p>
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<p>The simulation environment setting. (<b>a</b>) The desired SWA. (<b>b</b>) The HIL test environment.</p>
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<p>Performance validation of the controller MPC through the side slope passing simulation test. (<b>a</b>) The curve of roll arm’s length with the control of MPC or not. (<b>b</b>) The curve of LTR with the control of MPC or not. (<b>c</b>) The curve of the left wheels’ lateral force with the control of MPC or not.</p>
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<p>Performance validation of the controller MPC through the sine wave steering simulation test (<math display="inline"><semantics> <mrow> <mi>μ</mi> <mo>=</mo> <mn>0.85</mn> </mrow> </semantics></math>). (<b>a</b>) The curve of roll arm’s length with the control of MPC or not. (<b>b</b>) The curve of LTR with the control of MPC or not. (<b>c</b>) The curve of the sideslip angle with the control of MPC or not.</p>
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<p>Performance validation of the controller MPC through the sine wave steering simulation test (<math display="inline"><semantics> <mrow> <mi>μ</mi> <mo>=</mo> <mn>0.25</mn> </mrow> </semantics></math>). (<b>a</b>) The curve of roll arm’s length with the control of MPC or not. (<b>b</b>) The curve of LTR with the control of MPC or not. (<b>c</b>) The curve of the sideslip angle with the control of MPC or not.</p>
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30 pages, 16470 KiB  
Article
Research on Torque Characteristics of Vehicle Motor under Multisource Excitation
by Mingliang Yang, Yangyang Bao, Haibo Huang, Yalei Liu, Honglin Zhu and Weiping Ding
Electronics 2024, 13(11), 2019; https://doi.org/10.3390/electronics13112019 - 22 May 2024
Viewed by 1086
Abstract
A hub motor is integrated into an electric wheel. The external excitation is complex and the heat dissipation conditions are poor. The working temperature of the hub motor easily becomes too high, resulting in large fluctuations in the output torque, which affect its [...] Read more.
A hub motor is integrated into an electric wheel. The external excitation is complex and the heat dissipation conditions are poor. The working temperature of the hub motor easily becomes too high, resulting in large fluctuations in the output torque, which affect its service life. Taking a four-wheel hub-driven electric vehicle as the research object and aiming to resolve the issue of inaccurate prediction of the output torque of the hub motor in the real operating environment of the vehicle, a method for analyzing the temperature rise and torque characteristics of the hub motor considering multisource excitation and magnetic–thermal bidirectional coupling is proposed. First, the multisource excitation transmission path of the hub motor and the coupling principle of the road-electric wheel-vehicle body suspension system are analyzed from three aspects: the electromagnetic effect of the hub motor itself, the tire-ground effect, and the interaction between suspension (body) and electric wheel. We concluded that the load torque and air gap change in the motor are the key factors of its torque characteristics. On this basis, a dynamic model of the road-electric wheel-suspension-vehicle body system, an electromagnetic field model of the hub motor, and a temperature field model are established, and the influence of load torque and air gap change on the loss of in-wheel motor under multisource excitation is analyzed. Furthermore, based on the magnetic–thermal bidirectional coupling method, the motor loss under the combined action of load torque and air gap change is introduced into the temperature field model, and combined with the electromagnetic field model of the hub motor, the temperature distribution law and torque characteristics of the hub motor are accurately predicted. Finally, the accuracy and effectiveness of the calculation results of the temperature and torque characteristics of the hub motor are verified via an electric wheel bench test. Full article
(This article belongs to the Topic Power System Dynamics and Stability)
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<p>Multisource excitation transmission path of a hub-drive vehicle.</p>
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<p>Coupling principle of the road-electric wheel-suspension system.</p>
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<p>Force analysis of the electric wheel during rolling.</p>
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<p>Change rule of dynamic eccentricity <math display="inline"><semantics> <mrow> <msub> <mi>e</mi> <mi>d</mi> </msub> </mrow> </semantics></math>.</p>
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<p>Relationships between various models.</p>
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<p>(<b>a</b>) 1/4 suspension model principle. (<b>b</b>) 1/4 suspension dynamics model.</p>
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<p>Finite element model of the hub motor electromagnetic field.</p>
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<p>Relationship between the speed and output torque of the hub motor.</p>
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<p>Finite element model of the hub motor temperature field.</p>
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<p>Magnetic–thermal two-way coupling process.</p>
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<p>(<b>a</b>) Relationship between the output torque of the hub motor and the wheel speed under different working conditions. (<b>b</b>) Tire dynamic load under different working conditions.</p>
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<p>(<b>a</b>) Core loss of the hub motor; (<b>b</b>) eddy current loss of the hub motor; (<b>c</b>) winding loss of the hub motor; (<b>d</b>) output torque of the hub motors.</p>
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<p>(<b>a</b>) Core loss of the hub motor; (<b>b</b>) eddy current loss of the hub motor; (<b>c</b>) winding loss of the hub motor; (<b>d</b>) output torque of the hub motors.</p>
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<p>(<b>a</b>) Change in the radial magnetic density at 600 rpm; (<b>b</b>) Change in the unbalanced magnetic pull <math display="inline"><semantics> <mrow> <msub> <mi>F</mi> <mi>y</mi> </msub> </mrow> </semantics></math> at 600 rpm.</p>
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<p>Equivalent stiffness <math display="inline"><semantics> <mrow> <msub> <mi>K</mi> <mrow> <mi>U</mi> <mi>M</mi> <msub> <mi>P</mi> <mi>y</mi> </msub> </mrow> </msub> </mrow> </semantics></math> curves of the motor at different speeds.</p>
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<p>(<b>a</b>) Force between the stator and rotor; (<b>b</b>) relative offset of the stator and rotor.</p>
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<p>(<b>a</b>) Output torque of the hub motor caused by changes in the air gap at 600 rpm; (<b>b</b>) core loss of the hub motor caused by air gap changes at 600 rpm; (<b>c</b>) eddy current loss of the hub motor caused by air gap changes at 600 rpm; (<b>d</b>) winding loss of the hub motor caused by air gap changes at 600 rpm.</p>
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<p>(<b>a</b>) Output torque of the hub motor caused by changes in the air gap at 600 rpm; (<b>b</b>) core loss of the hub motor caused by air gap changes at 600 rpm; (<b>c</b>) eddy current loss of the hub motor caused by air gap changes at 600 rpm; (<b>d</b>) winding loss of the hub motor caused by air gap changes at 600 rpm.</p>
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<p>Overall temperature cloud diagrams of the hub motor at 200 rpm, 400 rpm, and 600 rpm.</p>
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<p>(<b>a</b>) Temperature variation curves of the hub motor stator. (<b>b</b>) Temperature variation curves of the hub motor rotor. (<b>c</b>) Temperature variation curves of the hub motor winding. (<b>d</b>) Temperature variation curves of the hub motor permanent magnet.</p>
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<p>Changes in the output torque of the hub motor at 600 rpm.</p>
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<p>Temperature rise test system of the 1/4 suspension hub motor driven by the hub.</p>
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<p>Rotor and winding test temperature and calculated temperature curves at 600 rpm.</p>
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<p>Motor test torque with time at 600 rpm.</p>
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<p>(<b>a</b>) Change in the radial magnetic density at 200 rpm. (<b>b</b>) Change in unbalanced magnetic pull <math display="inline"><semantics> <mrow> <msub> <mi>F</mi> <mi>y</mi> </msub> </mrow> </semantics></math> at 200 rpm.</p>
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<p>(<b>a</b>) Change in the radial magnetic density at 200 rpm. (<b>b</b>) Change in unbalanced magnetic pull <math display="inline"><semantics> <mrow> <msub> <mi>F</mi> <mi>y</mi> </msub> </mrow> </semantics></math> at 400 rpm.</p>
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<p>(<b>a</b>) Output torque of the hub motor caused by changes in the air gap at 200 rpm. (<b>b</b>) Core loss of the hub motor caused by air gap changes at 200 rpm. (<b>c</b>) Eddy current loss of the hub motor caused by air gap changes at 200 rpm. (<b>d</b>) Winding loss of the hub motor caused by air gap changes at 200 rpm.</p>
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<p>(<b>a</b>) Output torque of the hub motor caused by changes in the air gap at 200 rpm. (<b>b</b>) Core loss of the hub motor caused by air gap changes at 200 rpm. (<b>c</b>) Eddy current loss of the hub motor caused by air gap changes at 200 rpm. (<b>d</b>) Winding loss of the hub motor caused by air gap changes at 200 rpm.</p>
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<p>(<b>a</b>) Output torque of the hub motor caused by changes in the air gap at 400 rpm. (<b>b</b>) Core loss of the hub motor caused by air gap changes at 400 rpm. (<b>c</b>) Eddy current loss of the hub motor caused by air gap changes at 400 rpm. (<b>d</b>) Winding loss of the hub motor caused by air gap changes at 400 rpm.</p>
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<p>(<b>a</b>) Output torque change in the hub motor at 200 rpm. (<b>b</b>) Output torque change in the hub motor at 400 rpm.</p>
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<p>(<b>a</b>) Rotor and winding test temperature and calculated temperature curves at 200 rpm. (<b>b</b>) Rotor and winding test temperature and calculated temperature curves at 400 rpm.</p>
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<p>Motor test torque curve with time at 200 rpm.</p>
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<p>Motor test torque curve with time at 400 rpm.</p>
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23 pages, 4148 KiB  
Article
Optimization of the Semi-Active-Suspension Control of BP Neural Network PID Based on the Sparrow Search Algorithm
by Mei Li, Jie Xu, Zelong Wang and Shuaihang Liu
Sensors 2024, 24(6), 1757; https://doi.org/10.3390/s24061757 - 8 Mar 2024
Cited by 7 | Viewed by 1533
Abstract
Electric vehicles with hub motors have integrated the motor into the wheel, which increase the unsprung mass of the vehicle, and intensifies the vibration of the underspring components. The motor excitation during driving also intensifies the wheel vibration. The coupling effect between the [...] Read more.
Electric vehicles with hub motors have integrated the motor into the wheel, which increase the unsprung mass of the vehicle, and intensifies the vibration of the underspring components. The motor excitation during driving also intensifies the wheel vibration. The coupling effect between the two makes the performance of electric vehicles deteriorate. The article employed a disc-type permanent-magnet motor as the hub motor, taking into consideration the increase in sprung mass caused by the hub motor and the adverse effects of vertical vibration from motor excitation. Based on random road-surface excitation, and considering the secondary excitation caused by wheel motor drive and vehicle-road coupling, a coupled-dynamics model of a semi-active-suspension vehicle-road system for vertical vehicle motion is investigated under multiple excitations. Using body acceleration, suspension deflection, and dynamic tire load as evaluation indicators, a BP neural network PID controller based on the sparrow search algorithm optimization is proposed for the semi-active-suspension system. Compared with PID control and particle swarm optimization (PSO-BPNN-PID), the research findings indicate that the optimized semi-active suspension significantly improves the ride comfort of hub-motor electric vehicles, and meets the requirements for control performance under different vehicle driving conditions. Full article
(This article belongs to the Section Vehicular Sensing)
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<p>Dynamic model of electric vehicle wheel-hub motor system coupled with road.</p>
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<p>Random excitation of C-level road surface.</p>
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<p>The displacement of the road surface due to the secondary excitation.</p>
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<p>Disk-motor vertical excitation.</p>
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<p>Structure of back-propagation neural network.</p>
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<p>Structure of SSA-BPNN-PID controller.</p>
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<p>SSA-BP-PID flowchart.</p>
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<p>30 km/h-vehicle driving conditions. (<b>a</b>) Body acceleration, (<b>b</b>) suspension deflection, (<b>c</b>) dynamic tire load.</p>
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<p>60 km/h-vehicle driving conditions. (<b>a</b>) Body acceleration, (<b>b</b>) suspension deflection, (<b>c</b>) dynamic tire load.</p>
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<p>60 km/h-vehicle driving conditions. (<b>a</b>) Body acceleration, (<b>b</b>) suspension deflection, (<b>c</b>) dynamic tire load.</p>
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<p>90 km/h-vehicle driving conditions. (<b>a</b>) Body acceleration, (<b>b</b>) suspension deflection, (<b>c</b>) dynamic tire load.</p>
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<p>30 km/h-vehicle driving conditions. (<b>a</b>) Body acceleration, (<b>b</b>) suspension deflection, (<b>c</b>) dynamic tire load.</p>
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<p>30 km/h-vehicle driving conditions. (<b>a</b>) Body acceleration, (<b>b</b>) suspension deflection, (<b>c</b>) dynamic tire load.</p>
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<p>60-km/h vehicle driving conditions. (<b>a</b>) Body acceleration, (<b>b</b>) suspension deflection, (<b>c</b>) dynamic tire load.</p>
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<p>90 km/h-vehicle driving conditions. (<b>a</b>) Body acceleration, (<b>b</b>) suspension deflection, (<b>c</b>) dynamic tire load.</p>
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16 pages, 5700 KiB  
Article
Vibration Control of Car Body and Wheel Motions for In-Wheel Motor Vehicles Using Road Type Classification
by Young-Jun Kim, Youngil Sohn, Sehyun Chang, Seung-Bok Choi and Jong-Seok Oh
Actuators 2024, 13(2), 80; https://doi.org/10.3390/act13020080 - 18 Feb 2024
Cited by 2 | Viewed by 2061
Abstract
In-wheel motor vehicles are gaining attention as a new type of electric vehicle due to their efficient power units located inside each wheel hub. However, they are more susceptible to wheel resonance due to the increase in unsprung mass caused by the weight [...] Read more.
In-wheel motor vehicles are gaining attention as a new type of electric vehicle due to their efficient power units located inside each wheel hub. However, they are more susceptible to wheel resonance due to the increase in unsprung mass caused by the weight of the motor. This can result in both decreased ride comfort and driving stability. To resolve this issue, in this study, we aim to apply an optimal switching controller with a semi-active actuator—a magnetorheological (MR) damper. For the implementation of the optimal switching controller, road type classification is also carried out. An acceleration sensor is used for the road type classification, and the control logics include a ride comfort controller (the linear quadratic regulator (LQR_Paved Road)) and a wheel motion controller (LQR_Off Road) for improved driving stability. For paved roads, the LQR_Paved Road control input is applied to the MR damper. However, if a road type prone to wheel resonance is detected, the control logic switches to the LQR_Off Road. During the transition, a weighted average of both the LQR_Paved Road and LQR_Off Road control input is applied to the actuator. Computer simulations are performed to evaluate the vibration control performance, including the ride comfort and driving stability on various road profiles. Full article
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<p>Dynamic characteristics of the vehicle suspension system.</p>
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<p>A 2-DOF quarter-car suspension model of the in-wheel motor vehicle.</p>
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<p>Typical control flowchart.</p>
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<p>Control flowchart proposed in this work.</p>
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<p>Road type classification based on LSTM and Kalman filter.</p>
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<p>Internal structure of LSTM model.</p>
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<p>LSTM layers.</p>
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<p>Confusion matrix for random road + 9 Hz wavy road.</p>
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<p>Road profile used for simulation with MATLAB/Simulink.</p>
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<p>Control results in frequency domain.</p>
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<p>Control results in time domain.</p>
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<p>Control input results of each controller.</p>
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21 pages, 30482 KiB  
Article
Design and Testing of a New Type of Planetary Traction Drive Bearing-Type Reducer
by Hongyu Shu, Yijie Yu, Ran Shu, Wenjie Wang and Changjiang Pan
Machines 2024, 12(2), 107; https://doi.org/10.3390/machines12020107 - 4 Feb 2024
Viewed by 2088
Abstract
This paper presents the design and development of a new type of planetary traction drive bearing-type reducer. In this design, the transmission outer ring is replaced with an elastic ring. The design constructs a circular arc at the axial end of the rolling [...] Read more.
This paper presents the design and development of a new type of planetary traction drive bearing-type reducer. In this design, the transmission outer ring is replaced with an elastic ring. The design constructs a circular arc at the axial end of the rolling body’s contour line. This ensures that the contact point of this arc with the reducer’s outer ring and the inner ring’s axial end face is maintained on the radial traction contact line. As a result, it can replace the thrust bearing and provide an axial support function. It has the advantages of simple structure, easy processing, smooth transmission, and low noise. This paper first introduces the design and development process of this bearing-type reducer and presents systematic research on its transmission principle and dynamics. Subsequently, in response to the edge effect phenomenon of the outer ring contact line, the contour line of the outer ring is refined by adopting the shaping method used for bearing rollers, establishing a full circular arc profile shaping method, which significantly improves its edge effect. Finally, in our investigations, combined with experimental tests, a prototype of the bearing-type reducer was fabricated, and the speed ratio, torque, and transmission efficiency of the reducer were studied. The results demonstrate that the bearing-type reducer can achieve high transmission accuracy and efficiency. The transmission performance varies significantly under different lubrication conditions, with the peak efficiency reaching as high as 99.97% when using Santotrac 50 traction oil. The results verify the feasibility of the proposed design method and have the potential to be applied in wheel hub motors and robot joints. Full article
(This article belongs to the Section Electrical Machines and Drives)
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<p>Bearing-type reducer assembly diagram.</p>
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<p>Sketch of single bearing-type reducer structure.</p>
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<p>The actual structure of the bearing-type reducer.</p>
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<p>Reducer cutaway view and partial enlargement.</p>
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<p>Design parameters of reducer outer ring–rolling element on the flange.</p>
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<p>The relationship between the film thickness ratio and the maximum contact stress along the contact line relative to the length of the contact line: (<b>a</b>) inner contact line; (<b>b</b>) outer contact line.</p>
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<p>Contact stress cloud of bearing-type reducer: (<b>a</b>) contact stress cloud of outer ring–rolling body; (<b>b</b>) contact stress cloud of inner ring–rolling body.</p>
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<p>Contact stresses at the contact line of a bearing-type reducer: (<b>a</b>) contact stress at the outer ring–roller contact line; (<b>b</b>) contact stress at the inner ring–roller contact line.</p>
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<p>Convexity trimming methods for bearing rollers: (<b>a</b>) full-circle vein trimming; (<b>b</b>) modification of intersecting arc prime line; (<b>c</b>) tangent arc plain line modification; (<b>d</b>) logarithmic prime line trimming.</p>
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<p>Variation curves of contact stresses of the bearing-type reducer with different camber modifications of the unchamfered outer ring: (<b>a</b>) inner ring–roller contact stress curve; (<b>b</b>) outer ring–roller contact stress curve.</p>
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<p>Variation curves of contact stresses of the bearing-type reducer when the outer ring with an end chamfer of 1 mm is modified with different convexities: (<b>a</b>) inner ring–roller contact stress profile; (<b>b</b>) outer ring–rolling element contact stress curve.</p>
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<p>Comparison of contact stresses at outer ring–roller contact line: (<b>a</b>) untrimmed unchamfered outer ring; (<b>b</b>) convexity 10 <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">μ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math> unchamfered outer ring; (<b>c</b>) untrimmed chamfered outer ring; (<b>d</b>) convexity 10 <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">μ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math> chamfered outer ring.</p>
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<p>Bearing-type reducer: physical pictures.</p>
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<p>Bearing-type reducer: test bench.</p>
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<p>Real−time variation curves of input torque and output torque at 1000 rpm with no load.</p>
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<p>Variation in transmission efficiency with output torque at 1500 rpm with different traction oils.</p>
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<p>Plot of ratio versus load at different speeds.</p>
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<p>The relationship between transmission efficiency and output torque at different speeds.</p>
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<p>The 2500 rpm slip rate and transmission efficiency with increasing output torque.</p>
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27 pages, 9211 KiB  
Article
Back Propagation Neural Network-Based Fault Diagnosis and Fault Tolerant Control of Distributed Drive Electric Vehicles Based on Sliding Mode Control-Based Direct Yaw Moment Control
by Tianang Sun, Pak-Kin Wong and Xiaozheng Wang
Vehicles 2024, 6(1), 93-119; https://doi.org/10.3390/vehicles6010004 - 29 Dec 2023
Cited by 2 | Viewed by 1548
Abstract
Distributed-drive vehicles utilize independent drive motors on the four-wheel hubs. The working conditions of the wheel-hub motors are so harsh that the motors are prone to failing under different driving conditions. This study addresses the impact of drive motor faults on vehicle performance, [...] Read more.
Distributed-drive vehicles utilize independent drive motors on the four-wheel hubs. The working conditions of the wheel-hub motors are so harsh that the motors are prone to failing under different driving conditions. This study addresses the impact of drive motor faults on vehicle performance, particularly on slippery roads where sudden faults can lead to accidents. A fault-tolerant control system integrating motor fault diagnosis and a direct yaw moment control (DYC) based fault-tolerant controller are proposed to ensure the stability of the vehicle during various motor faults. Due to the difficulty of identifying the parameters of the popular permanent magnet synchronous wheel hub motors (PMSMs), the system employs a model-free backpropagation neural network (BPNN)-based fault detector. Turn-to-turn short circuits, open-phase faults, and diamagnetic faults are considered in this research. The fault detector is trained offline and utilizes rotor speed and phase currents for online fault detection. The system assigns the torque outputs from both healthy and faulted motors based on fault categories using sliding mode control (SMC)-based DYC. Simulations with four-wheel electric vehicle models demonstrate the accuracy of the fault detector and the effectiveness of the fault-tolerant controller. The proposed system is prospective and has potential for the development of distributed electric vehicles. Full article
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<p>2-DOF vehicle dynamics model.</p>
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<p>7-DOF vehicle model (<b>a</b>) 7-DOF vehicle model (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>i</mi> <mi>j</mi> </mrow> </semantics></math> wheel model (<math display="inline"><semantics> <mrow> <mi>i</mi> <mo>=</mo> <mi>R</mi> <mo>\</mo> <mi>F</mi> </mrow> </semantics></math> (right\left),<math display="inline"><semantics> <mrow> <mo> </mo> <mi>j</mi> <mo>=</mo> <mi>F</mi> <mo>\</mo> <mi>R</mi> </mrow> </semantics></math> (front\rear)).</p>
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<p>Forces on one tire.</p>
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<p>Schematic diagram of the control system.</p>
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<p>Flow chat of a BPNN-based motor fault detector.</p>
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<p>Schematic diagram of a neural network.</p>
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<p>DYC schematic diagram (<b>a</b>) Force analysis of DYC; (<b>b</b>) DYC flowchart.</p>
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<p>Schematic diagram of a normal three-phase motor.</p>
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<p>Control diagram of PMSMs.</p>
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<p>Equivalent circuit model of a short-circuit fault between turns.</p>
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<p>Equivalent circuit model for an open circuit fault.</p>
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<p>Friction coefficient of the road for simulation tests.</p>
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<p>J functions for normal motors. (<b>a</b>) time domain response; (<b>b</b>) power spectral density response.</p>
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<p>J functions for normal, open circuit, and short circuit faults. (<b>a</b>) time domain response; (<b>b</b>) power spectral density response.</p>
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<p>Neural network iteration error.</p>
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<p>The confusion matrix of results for BPNN. (<b>a</b>) Confusion matrix of results; (<b>b</b>) Confusion matrix of results in percentage.</p>
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<p>Simulation results for straight-line driving with a faulted LR motor. (<b>a</b>) Phase currents of the motor with SC faults; (<b>b</b>) Phase currents of the motor with OC faults; (<b>c</b>) Longitudinal speed; (<b>d</b>) Lateral speed; (<b>e</b>) Yaw rate; (<b>f</b>) Trajectory.</p>
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<p>Simulation results for straight-line driving with a faulted LR motor. (<b>a</b>) Phase currents of the motor with SC faults; (<b>b</b>) Phase currents of the motor with OC faults; (<b>c</b>) Longitudinal speed; (<b>d</b>) Lateral speed; (<b>e</b>) Yaw rate; (<b>f</b>) Trajectory.</p>
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<p>Simulation results for SLC with a faulted LR motor. (<b>a</b>) Steering angles of the front wheel; (<b>b</b>) Phase currents of the motor with SC fault; (<b>c</b>) Phase currents of the motor with OC fault; (<b>d</b>) Longitudinal speed; (<b>e</b>) Lateral speed; (<b>f</b>) Yaw rate; (<b>g</b>) Trajectory.</p>
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<p>Simulation results for SLC with a faulted LR motor. (<b>a</b>) Steering angles of the front wheel; (<b>b</b>) Phase currents of the motor with SC fault; (<b>c</b>) Phase currents of the motor with OC fault; (<b>d</b>) Longitudinal speed; (<b>e</b>) Lateral speed; (<b>f</b>) Yaw rate; (<b>g</b>) Trajectory.</p>
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25 pages, 7840 KiB  
Article
In-Wheel Motor Control System for Four-Wheel Drive Electric Vehicle Based on CR-GWO-PID Control
by Xiaoguang Xu, Miao Wang, Ping Xiao, Jiale Ding and Xiaoyu Zhang
Sensors 2023, 23(19), 8311; https://doi.org/10.3390/s23198311 - 8 Oct 2023
Cited by 4 | Viewed by 3327
Abstract
In order to improve the driving performance of four-wheel drive electric vehicles and realize precise control of their speed, a Chaotic Random Grey Wolf Optimization-based PID in-wheel motor control algorithm is proposed in this paper. Based on an analysis of the structural principles [...] Read more.
In order to improve the driving performance of four-wheel drive electric vehicles and realize precise control of their speed, a Chaotic Random Grey Wolf Optimization-based PID in-wheel motor control algorithm is proposed in this paper. Based on an analysis of the structural principles of electric vehicles, mathematical and simulation models for the whole vehicle are established. In order to improve the control performance of the hub motor, the traditional Grey Wolf Optimization algorithm is improved. In particular, an enhanced population initialization strategy integrating sine and cosine random distribution factors into a Kent chaotic map is proposed, the weight factor of the algorithm is improved using a sine-based non-linear decreasing strategy, and the population position is improved using the random proportional movement strategy. These strategies effectively enhance the global optimization ability, convergence speed, and optimization accuracy of the traditional Grey Wolf Optimization algorithm. On this basis, the CR-GWO-PID control algorithm is established. Then, the software and hardware of an in-wheel motor controller are designed and an in-wheel motor bench test system is built. The simulation and bench test results demonstrate the significantly improved response speed and control accuracy of the proposed in-wheel motor control system. Full article
(This article belongs to the Topic Vehicle Dynamics and Control)
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<p>Structural diagram of a four-wheel drive in-wheel motor electric vehicle.</p>
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<p>In-wheel motor map.</p>
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<p>Vehicle model simulation diagram. (Green triangles indicate the changes in the number of in-wheel motors).</p>
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<p>The results of vehicle driving simulation: (<b>a</b>) EV battery change and (<b>b</b>) EV mileage.</p>
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<p>Comparison of key indicators of simulated driving under vehicle simulation road conditions: (<b>a</b>) Comparing the required EV driving speed with the actual EV driving speed; (<b>b</b>) Comparing the required motor torque of the EV with the actual motor torque of the EV.</p>
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<p>Algorithm population initialization comparison diagram: (<b>a</b>) and (<b>b</b>).</p>
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<p>Algorithm distance weight comparison diagram.</p>
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<p>Algorithm flowchart.</p>
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<p>Test function comparison results: (<b>a</b>) Test function <span class="html-italic">f</span><sub>1</sub>; (<b>b</b>) test function <span class="html-italic">f</span><sub>2</sub>; (<b>c</b>) test function <span class="html-italic">f</span><sub>3</sub>; (<b>d</b>) test function <span class="html-italic">f</span><sub>4</sub>; (<b>e</b>) test function <span class="html-italic">f</span><sub>5</sub>; and (<b>f</b>) test function <span class="html-italic">f</span><sub>6</sub>.</p>
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<p>CR-GWO-PID motor speed simulation flow diagram.</p>
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<p>Motor speed simulation curves under the four control strategies: (<b>a</b>) Target speed 600 rpm; (<b>b</b>) target speed 500 rpm; and (<b>c</b>) target speed 400 rpm. (The red arrow indicates magnification of the specified location.).</p>
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<p>Flowchart of the in-wheel motor test. (The solid line represents the process and the dashed line represents the constituent structure.).</p>
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<p>Images of the test bench, showing its layout.</p>
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<p>In Test Group 1, the Simulation curve diagram of motor speed under the four control strategies: (<b>a</b>) Target speed 400 rpm; (<b>b</b>) target speed 500 rpm; and (<b>c</b>) target speed 600 rpm.</p>
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<p>In Test Group 2, the Simulation curve diagram of motor speed under the four control strategies: (<b>a</b>) Target speed 400 rpm; (<b>b</b>) target speed 500 rpm; and (<b>c</b>) target speed 600 rpm.</p>
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<p>In Test Group 3, the Simulation curve diagram of motor speed under the four control strategies: (<b>a</b>) Target speed 400 rpm; (<b>b</b>) target speed 500 rpm; and (<b>c</b>) target speed 600 rpm.</p>
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12 pages, 3548 KiB  
Article
Development and Testing of a Friction-Driven Forestry Electric Monorail Car
by Haoting Xu, Daochun Xu, Cheng Zheng, Xiaopeng Bai and Wenbin Li
Forests 2023, 14(2), 263; https://doi.org/10.3390/f14020263 - 30 Jan 2023
Cited by 1 | Viewed by 1851
Abstract
A friction-driven forestry electric monorail car based on a wheel hub motor is designed with the aim of solving the problems of the low transportation capacity, low running speed, large turning radius, and poor stability of low-slope mountain forestry monorails. The relationships between [...] Read more.
A friction-driven forestry electric monorail car based on a wheel hub motor is designed with the aim of solving the problems of the low transportation capacity, low running speed, large turning radius, and poor stability of low-slope mountain forestry monorails. The relationships between the minimum turning radius and the steering spring elasticity coefficient, between the body tilt and the anti-tip spring elasticity coefficient, and between the minimum turning radius of the monorail car and the distance between the two chassis and the two steering wheels was provided by the theoretical calculation and analysis of the key parameters of a dual-chassis structure, steering device, and anti-tip device. The dimensional parameters of the key components were determined. The three-dimensional design of the overall car was carried out, and the feasibility of the design was verified in kinematic simulation experiments. A performance test of the monorail car was conducted with the minimum turning radius, maximum load capacity, maximum full load speed, climbing degree, and center of gravity offset as indicators. The test results show that the monorail car has a minimum turning radius of 3.3 m, a maximum load capacity of 300 kg, a maximum speed of 20 km·h−1 fully loaded, a maximum gradient of 21°, and a unilateral vibration amplitude of 8 mm or less. The double-chassis structure and anti-tip device met the design requirements. The good transportation performance of the designed monorail car effectively solves the problems of a large turning radius and unstable driving of current forestry monorails. Additionally, the designed monorail car is environmentally friendly and efficient, meeting the requirements of monorail transporters for low-slope mountain forests and laying the foundation for the intelligent harvesting and transportation of mountain forest fruits. Full article
(This article belongs to the Section Forest Operations and Engineering)
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<p>Three-dimensional modeling of the monorail car: 1. track and connecting parts; 2. drive unit; 3. body; 4. chassis; 5. counterweight box; 6. anti-tip device; 7. gap-adjusting frame; 8. spring; 9. I-beam; 10. guide wheel; 11. load-bearing wheel; 12. wheel motor; 13. articulated disc; 14. chassis; 15. body. (<b>a</b>) Design of the complete car structure; (<b>b</b>) Design of the chassis structure.</p>
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<p>Turning diagrams. (<b>a</b>) Whole-car double-chassis turning; (<b>b</b>) Single-chassis steering.</p>
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<p>Force analysis of the driving wheel.</p>
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<p>Force analysis. (<b>a</b>) Whole-car force analysis (<b>b</b>) Force analysis of the anti-tip device.</p>
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<p>Monorail car simulation experiment. (<b>a</b>) horizontal straight track (<b>b</b>) climbing straight track (<b>c</b>) horizontal curved track.</p>
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<p>Simulation experiment of a gravity offset.</p>
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<p>Car site test. (<b>a</b>) Performance test charts (<b>b</b>) Vibration test chart.</p>
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<p>Frequency amplitude comparison of the track and chassis.</p>
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16 pages, 2969 KiB  
Article
Transformable Wheelchair–Exoskeleton Hybrid Robot for Assisting Human Locomotion
by Ronnapee Chaichaowarat, Sarunpat Prakthong and Siri Thitipankul
Robotics 2023, 12(1), 16; https://doi.org/10.3390/robotics12010016 - 18 Jan 2023
Cited by 18 | Viewed by 7394
Abstract
This paper presents a novel wheelchair–exoskeleton hybrid robot that can transform between sitting and walking modes. The lower-limb exoskeleton uses planetary-geared motors to support the hip and knee joints. Meanwhile, the ankle joints are passive. The left and right wheel modules can be [...] Read more.
This paper presents a novel wheelchair–exoskeleton hybrid robot that can transform between sitting and walking modes. The lower-limb exoskeleton uses planetary-geared motors to support the hip and knee joints. Meanwhile, the ankle joints are passive. The left and right wheel modules can be retracted to the lower legs of the exoskeleton to prepare for walking or stepping over obstacles. The chair legs are designed to form a stable sitting posture to avoid falling while traveling on smooth surfaces with low energy consumption. Skateboard hub motors are used as the front driving wheels along with the rear caster wheels. The turning radius trajectory as the result of differential driving was observed in several scenarios. For assisting sit-to-stand motion, the desired joint velocities are commanded by the user while the damping of the motors is set. For stand-to-sit motion, the equilibrium of each joint is set to correspond to the standing posture, while stiffness is adjusted on the basis of assistive levels. The joint torques supported by the exoskeleton were recorded during motion, and leg muscle activities were studied via surface electromyography for further improvement. Full article
(This article belongs to the Special Issue Human Factors in Human–Robot Interaction)
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<p>Conceptual design of the wheelchair–exoskeleton hybrid robot during the sit-to-stand transition on the sagittal plane. In the sitting configuration, the ground reaction force position is assumed to be at the front wheel. The trunk, head, and arms are simply considered a rigid upper-body link. The hip, knee, and ankle joint angles are shown. The weight of each segment is assumed to be at its center of gravity. The locations of the link lengths and center of gravity in the standing configuration are shown.</p>
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<p>Simulated sit-to-stand motion: (<b>a</b>) Simplified kinematics of sit-to-stand motion in our study. The ankle, knee, and hip joints shown by the red markers connect the shank, thigh, and body links. The links’ CGs are shown by the green makers. The origin of the plot is the intersection between the horizontal line crossing the ankle joint and the vertical line crossing the front wheel center; (<b>b</b>) Simulated knee and hip angles are plotted in blue and orange, respectively. The total duration of the sit-to-stand motion is approximately 2 min for this quasi-static simulation. The estimated knee and hip extension moments are plotted in blue and orange, respectively, and the total clockwise moment computed via Equation (6) is plotted in yellow.</p>
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<p>Alpha prototype of the wheelchair–exoskeleton hybrid robot in the standing upright posture (for walking across obstacles) and the wheelchair mode (for safe and low-energy traveling on smooth surfaces).</p>
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<p>(<b>a</b>) Wheel module’s retraction mechanism using the Actuonix linear actuator; (<b>b</b>) Foldable chair leg driven through the elastomer cord.</p>
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<p>Diagram of hardware integration. The first microcontroller with an analog joystick is used to control the robot running in wheelchair mode. The skateboard hub motors operated at 24 V are driven by the electronic speed control circuits receiving commands via pulse-width modulation (PWM) signals. The second microcontroller is used to control the exoskeleton’s hip and knee motors supporting sit-to-stand and stand-to-sit motions. The motors operated at 24 V receive the commands and return their status via CANBUS. The two linear actuators for retracting the left and right wheel modules are operated at 12 V and controlled via PWM signals.</p>
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<p>(<b>a</b>) Experimental setup and procedure; (<b>b</b>) Surface electromyography (EMG) electrodes (DELSYS’s Trigno™) were attached to both legs of the participant over the vastus lateralis (VL) in front of the thigh, the bicep femoris (BF) behind the thigh, the tibialis anterior (TA) in front of the shank, and the gastrocnemius (GC) behind the shank [<a href="#B32-robotics-12-00016" class="html-bibr">32</a>]; (<b>c</b>) The participant wearing the exoskeleton prototype performed sit-to-stand and stand-to-sit motions while recording the EMG of the muscles, along with the exoskeleton knee and hip motors’ position, velocity, and torque to evaluate assistive performance.</p>
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<p>Angle and moment of the exoskeleton’s right knee and hip motors.</p>
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<p>RMS electromyography (EMG) of the <b>right</b> (blue) and <b>left</b> (green) muscles recorded during the basic sit-to-stand test (without wearing the exoskeleton).</p>
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<p>RMS electromyography (EMG) of the <b>right</b> (blue) and <b>left</b> (green) muscles recorded during the passive sit-to-stand test (without actuation).</p>
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<p>RMS electromyography (EMG) of the <b>right</b> (blue) and the <b>left</b> (green) muscles recorded during the robot sit-to-stand test (with knee extension support).</p>
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<p>Markers are attached to the floor in a 5 × 3 array: (<b>a</b>) Original recording with distortion from wide lines; (<b>b</b>) Recording processed via OpenCV to yield the 4 × 2 m reference grid.</p>
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<p>Tracking of the coordinates of both caster wheels during turning.</p>
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<p>Examples of the wheelchair turning trajectories with/without the occupant during pivot <b>left</b> turns, one-wheel <b>left</b> turns, and two-wheel <b>right</b> turns. Blue markers indicate the front driving hub motors. Black, cyan, and pink markers and curves represent the wheelchair–human’s CG, <b>left</b>, and <b>right</b> caster wheels, respectively.</p>
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<p>Estimated CG velocity and acceleration with/without the occupant during pivot turns, one-wheel turns, and two-wheel turns.</p>
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<p>Best fit circles, based on the Taubin algebraic method, showing the turning radius of wheelchair with/without the occupant during pivot turns, one-wheel turns, and two-wheel turns.</p>
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28 pages, 17229 KiB  
Article
Comparative Studies on Batteries for the Electrochemical Energy Storage in the Delivery Vehicle
by Piotr Szewczyk and Andrzej Łebkowski
Energies 2022, 15(24), 9613; https://doi.org/10.3390/en15249613 - 18 Dec 2022
Cited by 3 | Viewed by 1758
Abstract
The publication presents a proposal of methodology for the evaluation of electric vehicle energy storage, based on examples of three types of batteries. Energy stores are evaluated in different categories such as cost, reliability, total range, energy density, battery life, weight, dependency on [...] Read more.
The publication presents a proposal of methodology for the evaluation of electric vehicle energy storage, based on examples of three types of batteries. Energy stores are evaluated in different categories such as cost, reliability, total range, energy density, battery life, weight, dependency on ambient temperature, and requirements of battery conditioning system. The performance of the battery systems were analyzed on exemplary 4 × 4 vehicle with 4 independent drives systems composed of inverters and synchronous in-wheel motors. The studies showed that the best results were obtained for energy storage built on LFP prismatic batteries, and the lowest ranking was given to energy storage built on cylindrical NMC batteries. The studies present the method of aggregation of optimization criteria as a valuable methodology for assessing design requirements and the risk of traction batteries in electric vehicles. Full article
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<p>Loss of capacity of Winston WB–LYP160Aha cells as a function of the number of cycles for different operating ranges.</p>
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<p>Loss of capacity of NMC Samsung INR18650–30Q cells as a function of the number of cycles for various operating ranges.</p>
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<p>Dependence of internal resistance versus temperature for LFP—WB-LYP160, NMC—30Q, NMC—E76 (at load of 1C).</p>
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<p>Configuration of the electric drive system with four electric motors installed in the wheels of the vehicle and inverter on board the vehicle. PE—Power Electronics (Inverter), WHM—Wheel Hub Motor.</p>
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<p>Reliability block diagram of vehicle energy storage (all types).</p>
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<p>Reliability of different energy storage systems: Type 1: LFP—prismatic, Type 2: 30Q—cylindrical, Type 3: E76—pouch.</p>
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<p>WLTP test cycle, in accordance with Commission Regulation (EU) 2017/1151 [<a href="#B33-energies-15-09613" class="html-bibr">33</a>], where: (<b>a</b>) phase Low<sub>3</sub>(A1/7); (<b>b</b>) Medium<sub>3-1</sub>(A1/8) phase; (<b>c</b>) phase High<sub>3-1</sub>(A1/10); and (<b>d</b>) Extra High<sub>3</sub> phase (A1/12).</p>
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<p>WLTP test cycle, in accordance with Commission Regulation (EU) 2017/1151 [<a href="#B33-energies-15-09613" class="html-bibr">33</a>], where: (<b>a</b>) phase Low<sub>3</sub>(A1/7); (<b>b</b>) Medium<sub>3-1</sub>(A1/8) phase; (<b>c</b>) phase High<sub>3-1</sub>(A1/10); and (<b>d</b>) Extra High<sub>3</sub> phase (A1/12).</p>
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<p>WLTP and WLTP-90 tests profiles.</p>
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<p>City Flat Road test profile (speed, absolute altitude, and grade).</p>
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<p>View of the simulation model of a vehicle with an electric 4 × 4 drive system, divided into blocks: 1—vehicle motion resistance; 2—synchronous motors; 3—voltage inverters; 4—energy storage; 5—travel route adjuster; 6—vehicle cabin heating/cooling system; 7—electric load on the vehicle’s on-board system receivers 12VDC.</p>
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<p>WLTP results of simulation tests for the 4 × 4 drive system with Type 1 energy storage.</p>
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<p>WLTP results of simulation tests for the 4 × 4 drive system with Type 1 energy storage.</p>
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<p>WLTP-90 results of simulation tests for the 4 × 4 drive system with Type 1 energy storage.</p>
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<p>City Flat Road results of simulation tests for the 4 × 4 drive system with Type 1 energy storage.</p>
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<p>WLTP results of simulation tests for the 4 × 4 drive system with Type 2 energy storage.</p>
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<p>WLTP-90 results of simulation tests for the 4 × 4 drive system with Type 2 energy storage.</p>
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<p>City Flat Road results of simulation tests for the 4 × 4 drive system with Type 2 energy storage.</p>
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<p>WLTP results of simulation tests for the 4 × 4 drive system with Type 3 energy storage.</p>
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<p>WLTP-90 results of simulation tests for the 4 × 4 drive system with Type 3 energy storage.</p>
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<p>WLTP-90 results of simulation tests for the 4 × 4 drive system with Type 3 energy storage.</p>
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<p>City Flat Road results of simulation tests for the 4 × 4 drive system with Type 3 energy storage.</p>
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<p>City Flat Road results of simulation tests for the 4 × 4 drive system with Type 3 energy storage.</p>
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<p>Ranking of energy storage types.</p>
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