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Search Results (929)

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Keywords = shape memory alloy

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13 pages, 5359 KiB  
Article
Displaying Tactile Sensation by SMA-Driven Vibration and Controlled Temperature for Cutaneous Sensation Assessment
by Tomohiro Nozawa, Renke Liu and Hideyuki Sawada
Actuators 2024, 13(11), 463; https://doi.org/10.3390/act13110463 (registering DOI) - 18 Nov 2024
Abstract
In this paper, we propose a novel tactile display that can present vibration patterns and thermal stimuli simultaneously. The vibration actuator employs a shape memory alloy (SMA) wire to generate micro-vibration with a frequency control of up to 300 Hz. The micro-vibration is [...] Read more.
In this paper, we propose a novel tactile display that can present vibration patterns and thermal stimuli simultaneously. The vibration actuator employs a shape memory alloy (SMA) wire to generate micro-vibration with a frequency control of up to 300 Hz. The micro-vibration is conducted to a tactile pin for amplifying the vibration, to be sufficiently recognized by a user. A thermal stimulation unit, on the other hand, consists of four Peltier elements with heatsinks for heat radiation. Four vibration actuators and a thermal unit are arranged in a flat plane with a size of 20 mm × 20 mm, on which a user places the tip of an index finger to feel the presented vibratory stimuli under different temperature conditions. We conducted an experiment by employing nine subjects to evaluate the performance of the proposed tactile display and also to investigate the effects of temperature on recognizing tactile sensation. The results demonstrated that the proposed device was feasible for the quantitative diagnosis of tactile sensation. In addition, we verified that the sensitivity of tactile sensation decreased with colder stimuli. Full article
(This article belongs to the Special Issue Innovative Actuators Based on Shape Memory Alloys)
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Figure 1
<p>Illustration of shape memory effect.</p>
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<p>SMA actuator for vibration presentation: (<b>a</b>) Entire structure presenting stimuli to a fingertip; (<b>b</b>) Schematic illustration of the behavior.</p>
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<p>Pulse wave current.</p>
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<p>Structure of the tactile display: (<b>a</b>) Circuit board with four holes and the positions of SMA actuators; (<b>b</b>) Schematic illustration of the arrangement of actuators; (<b>c</b>) Top view of the tactile display with four SMA actuators covered by copper plate; (<b>d</b>) A finger placed on the display.</p>
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<p>Overview of the total system.</p>
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<p>Two different user interfaces. (<b>a</b>) A dialog box with custom parameter settings and a virtual keyboard. (<b>b</b>) A dialog box with pre-defined parameter values.</p>
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<p>Relationship between the frequency and time resolution.</p>
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<p>Boxplots of the scores under different conditions.</p>
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<p>Change in recognition response by trial times.</p>
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<p>Confusion matrices between the correct answers and the subject’s answers.</p>
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15 pages, 6365 KiB  
Article
Finite Element Combined Design and Material Optimization Addressing the Wear in Removable Implant Prosthodontics
by Pejman Shayanfard, Xingchen Tan, Matthias Karl and Frank Wendler
J. Funct. Biomater. 2024, 15(11), 344; https://doi.org/10.3390/jfb15110344 - 14 Nov 2024
Viewed by 337
Abstract
Wear at the male–female interface of retentive elements in implant-supported removable prostheses is the most frequent complication in such applications. The lack of an ideal/optimal insertion path, as well as the fabrication inaccuracies, are the primary contributors to this issue. A male attachment [...] Read more.
Wear at the male–female interface of retentive elements in implant-supported removable prostheses is the most frequent complication in such applications. The lack of an ideal/optimal insertion path, as well as the fabrication inaccuracies, are the primary contributors to this issue. A male attachment with a common ball anchor enhanced by lateral flexibility was investigated as a solution, compared to the widely used rigid ball anchor design. A parametric finite element analysis was performed to compare the wear-inducing maximum strain at the female polymer counterpart by various attachment designs made from titanium and Nitinol. The evolution of mechanical strains causing wear in the female part, as well as the contribution of stresses and martensitic transformation in the implant’s flexible shaft, were evaluated under several insertion misfit scenarios. Results indicate that introducing a long flexible shaft in the titanium implant reduced maximum strains in the female attachment part by up to 61% as compared to the solid ball anchor. Further improvement was observed by using the shape memory alloy Nitinol as shaft material, leading to a minor reduction in stress and strain at the contact surface but allowing for a shorter abutment. Finally, the optimized Nitinol implant design with a short, necked flexible shaft promoting martensitic transformation at low plateau stress resulted in an approximate 90% reduction in maximum strains at the inner surface of the female part during manual insertion, which indicates a significantly reduced wear phenomenon at the contact. Full article
(This article belongs to the Special Issue Biomaterials and Biomechanics Modelling in Dental Implantology)
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Figure 1
<p>Panoramic radiograph of a geriatric patient presenting multiple single-piece implants in the maxilla with balls for prosthesis retention (implant placement alio loco several years ago). Please note that a common path of insertion has not been established for the maxillary implants. The mandibular dentition is failing, but the patient still wanted to postpone treatment.</p>
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<p>Maxillary removable prosthesis not covering the palate as per the patient’s request. New O-rings have been placed inside corresponding metal housings to fit onto the implants. Two O-rings were intentionally removed as the patient was unable to remove the restoration when all six balls were engaged.</p>
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<p>Eight months after prosthesis delivery, the patient complained about loss of retention of her restoration, presenting with the O-rings shown in the bottom line (top line: new O-rings for comparison). Unilateral deterioration of the O-rings following compression of the material during repeated insertion and removal of the prosthesis is obvious.</p>
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<p>(<b>a</b>) Reference: solid Ti implant; (<b>b</b>) Ti and Nitinol implants, where a flexible long shaft is embedded; (<b>c</b>) short Nitinol implant, where the embedded long shaft is 3 mm shorter; (<b>d</b>) short-necked Nitinol implant; (<b>e</b>) representation of a design fault zone denoted as LPZ within the manuscript; and (<b>f</b>) representation of the optimized design in LPZ for the short-necked Nitinol implant.</p>
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<p>Three-dimensional model of a simplistic one-piece attachment with a ball anchor on top for retaining a removable prosthesis; (<b>a</b>) a 3D model of the female part fitting the ball anchor in different views; and (<b>b</b>) representation of the entire assembled FEM model including the surrounding Ti abutment: 1—female part; 2—male attachment part; and 3—Ti implant.</p>
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<p>Misfit types considered in this study: (<b>a</b>) perfect fit; (<b>b</b>) horizontal misfit between male and female attachment parts of 0.2 mm; (<b>c</b>) angulation misfit with the female part rotated (<math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> </mrow> </semantics></math> 3 degrees); and (<b>d</b>) horizontal and angulation misfit.</p>
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<p>FEM results for the reference solid Ti implant design. Stresses are depicted as equivalent to von Mises stress, while strains represent maximum principal strain; (<b>a1</b>–<b>a4</b>) perfect fit (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>a), where the longitudinal axis of the female component aligns with that of the inserted implant; (<b>b1</b>–<b>b4</b>) horizontal misfit: the abutment shifts horizontally for 0.2 mm (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>b); and (<b>c1</b>–<b>c4</b>) angulation misfit: the abutment rotates for 3 degrees (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c).</p>
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<p>FEM results for the angulation misfit (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c) of the long Ti implant (see <a href="#jfb-15-00344-f004" class="html-fig">Figure 4</a>b). Stresses are depicted as equivalent to von Mises stress, while strains represent the maximum principal strain. (<b>c1</b>–<b>c4</b>) angulation misfit: the abutment rotates for 3 degrees (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c), (<b>c5</b>) Detail of the flexible ball head (stress).</p>
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<p>FEM results for the long Nitinol implant, featuring an embedded flexible Nitinol long shaft (see <a href="#jfb-15-00344-f004" class="html-fig">Figure 4</a>b) for the angulation misfit (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c). Stresses are depicted as equivalent to von Mises stress, while strains represent the maximum principal strain. In (c5), the martensite volume fraction is mapped. (<b>c1</b>–<b>c4</b>) angulation misfit: the abutment rotates for 3 degrees (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c), (<b>c5</b>) detail of the flexible ball head (martensite volume fraction MVF).</p>
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<p>FEM results for the short Nitinol implant, featuring an embedded flexible Nitinol short shaft (see <a href="#jfb-15-00344-f004" class="html-fig">Figure 4</a>c) for the angulation misfit (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c). Stresses are depicted as equivalent to von Mises stress, while strains represent the maximum principal strain. (<b>c1</b>–<b>c4</b>) angulation misfit: the abutment rotates for 3 degrees (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c), (<b>c5</b>) Martensite volume fraction MVF.</p>
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<p>FEM results for the short-necked Nitinol implant, featuring a short-necked embedded Nitinol shaft (see <a href="#jfb-15-00344-f004" class="html-fig">Figure 4</a>d) in angulation misfit (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c). Stresses are depicted as equivalent to von Mises stress, while strains represent the maximum principal strain. (<b>c1</b>–<b>c4</b>) angulation misfit: the abutment rotates for 3 degrees (see <a href="#jfb-15-00344-f006" class="html-fig">Figure 6</a>c), (<b>c5</b>) Martensite volume fraction MVF.</p>
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<p>The effect of the ultimate design and material optimization on the reaction stresses on the surrounding Ti abutment. (<b>a1</b>,<b>b1</b>) The solid Ti implant and the flexible-necked Nitinol implant, respectively. In both trials, the implant is rotated (<math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>3</mn> </mrow> </semantics></math> degrees) and shifted horizontally by 0.1 mm in relation to the female part. (<b>a2</b>,<b>b2</b>) The resultant reaction stresses on the surrounding Ti abutment for the reference solid Ti design and the final optimized Nitinol implant design, respectively.</p>
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16 pages, 4756 KiB  
Article
Influence of Thermomechanical Treatments and Chemical Composition on the Phase Transformation of Cu-Al-Mn Shape Memory Alloy Thin Sheets
by Dusan Milosavljevic, Nora Lecis and Simone Cinquemani
Appl. Sci. 2024, 14(22), 10406; https://doi.org/10.3390/app142210406 - 12 Nov 2024
Viewed by 383
Abstract
This paper investigates the interrelated effects of thermomechanical treatments and chemical composition on the phase transformation capabilities of thin sheets made from Cu-Al-Mn shape memory alloys. The transformation capacity and transition temperatures were determined using DSC and DMA testing, while composition measurements were [...] Read more.
This paper investigates the interrelated effects of thermomechanical treatments and chemical composition on the phase transformation capabilities of thin sheets made from Cu-Al-Mn shape memory alloys. The transformation capacity and transition temperatures were determined using DSC and DMA testing, while composition measurements were performed using SEM/EDX analysis. The results demonstrate that applying hot-rolling treatments to alloys of reduced thickness leads to manganese oxidation and modifications in chemical composition, adversely impacting the phase transformation performance. This effect can be mitigated by the use of cold rolling. Additionally, the presence of phosphorus impurities can create inclusions that bind manganese, preventing it from remaining in the solid solution and further affecting phase transformation capabilities. Full article
(This article belongs to the Section Materials Science and Engineering)
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<p>Isothermal and iso-Mn section of the ternary Cu-Al-Mn phase diagram at 10% at. of Mn, as seen in [<a href="#B10-applsci-14-10406" class="html-bibr">10</a>], showing the selection of thermal treatment temperatures based on the phase regions at 16% at. of Al.</p>
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<p>Abnormal grain growth (AGG) [<a href="#B25-applsci-14-10406" class="html-bibr">25</a>], and betatization (BET) thermal treatments used for increasing relative grain size and obtaining martensite to induce the SME in the SMA sheets, respectively.</p>
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<p>Section of the Brinson one-dimensional SMA constitutive model showing the pseudoelastic (PE) tensile loading cycle used during the SMA “training process” highlighted by the red arrows for the tensile loading and unloading at a fixed temperature above the A<sub>f</sub> temperature of phase transformation.</p>
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<p>Optical microscopy images showing the martensitic phase obtained by betatization and quenching treatment: (<b>a</b>) 100× magnification sample, (<b>b</b>) 50× magnification sample.</p>
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<p>Differential scanning calorimetry (DSC) test performed on the Cu-Al-Mn alloy (sample 16 in <a href="#applsci-14-10406-t002" class="html-table">Table 2</a>).</p>
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<p>Ratio of the average measured concentrations of Mn and Al within each sample, sorted according to increasing ratio values.</p>
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<p>DSC analysis performed on a sample (sample 10 in <a href="#applsci-14-10406-f006" class="html-fig">Figure 6</a>) of Cu-Al-Mn showing inconsistent phase transformation performance.</p>
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<p>Cu-Al-Mn sheet samples used in the study, presented according to their average manganese content and their corresponding thermomechanical history, with each sample’s phase transformation ability highlighted.</p>
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<p>SEM and EDX analysis performed on sample 4 in the form of maps: (<b>a</b>) electron image of the sample, (<b>b</b>) EDX map showing Al distribution in the sample, (<b>c</b>) EDX map showing P distribution in the sample, (<b>d</b>) EDX map showing Mn distribution in the sample.</p>
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<p>Average composition of the inclusions observed in the Cu-Al-Mn SMA sheet samples (numbered according to the corresponding sample in <a href="#applsci-14-10406-t003" class="html-table">Table 3</a>).</p>
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21 pages, 4140 KiB  
Article
Investigation of the Seismic Performance of a Multi-Story, Multi-Bay Special Truss Moment Steel Frame with X-Diagonal Shape Memory Alloy Bars
by Dimitrios S. Sophianopoulos and Maria I. Ntina
Appl. Sci. 2024, 14(22), 10283; https://doi.org/10.3390/app142210283 - 8 Nov 2024
Viewed by 440
Abstract
In this work, the seismic response of a multi-story, multi-bay special truss moment frame (STMF) with Ni-Ti shape memory alloys (SMAs) incorporated in the form of X-diagonal braces in the special segment is investigated. The diameter of the SMAs per diagonal in each [...] Read more.
In this work, the seismic response of a multi-story, multi-bay special truss moment frame (STMF) with Ni-Ti shape memory alloys (SMAs) incorporated in the form of X-diagonal braces in the special segment is investigated. The diameter of the SMAs per diagonal in each floor was initially determined, considering the expected ultimate strength of the special segment, developed when the frame reaches its target drift and the desirable collapse mechanism, i.e., the formation of plastic hinges, according to the performance-based plastic design procedure. To further investigate the response of the structure with the SMAs incorporated, half the calculated SMA diameters were introduced. Continuing, three more cases were investigated: the mean value of the SMA diameter was introduced at each floor (case DC1), half the SMA diameter of case DC1 (case DC2), and twice the SMA diameter of case DC1 (case CD3). Dynamic time history analyses under seven benchmark earthquakes were conducted using commercial nonlinear Finite Element software (SeismoStruct 2024). Results were presented in the form of top-displacement time histories, the SMAs force–displacement curves, and maximum inter-story drifts, calculating also maximum SMA displacements. The analysis outcomes highlight the potential of the SMAs to be considered as a novel material in the seismic retrofit of steel structures. Both design approaches presented exhibit a certain amount of effectiveness, depending on the distribution, with the placement of the SMA bars and the seismic excitation considered. Further research is suggested to fully understand the capabilities of the use of SMAs as dissipation devices in steel structures. Full article
(This article belongs to the Special Issue Seismic and Energy Retrofitting of Existing Buildings)
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<p>The undeformed shape of the structure (conventional STMF).</p>
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<p>LPE: (<b>a</b>) comparison of the response of the conventional and the proposed STMF (with the full SMA diameter per diagonal); (<b>b</b>) 9th floor damper force–displacement curve (with the full SMA diameter per diagonal).</p>
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<p>LPE: (<b>a</b>) comparison of the response of the conventional and the proposed STMF (with half the SMAs diameter per diagonal); (<b>b</b>) 9th floor damper force–displacement curve STMF (with half the SMAs diameter per diagonal).</p>
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<p>Comparison of maximum inter-story drifts for the design cases considered: (<b>a</b>) LPE; (<b>b</b>) NE.</p>
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<p>Comparison of maximum inter-story drifts for the design cases considered: (<b>a</b>) K1E; (<b>b</b>) IVE.</p>
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<p>Comparison of maximum inter-story drifts for the design cases dealt with (<b>a</b>) K2E; (<b>b</b>) CE.</p>
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<p>Comparison of maximum inter-story drifts for the design cases considered: LE.</p>
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<p>Comparison of maximum inter-story drifts for (<b>a</b>) LPE; (<b>b</b>) NE.</p>
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<p>Comparison of maximum inter-story drifts for: (<b>a</b>) K1E; (<b>b</b>) IVE.</p>
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<p>Comparison of maximum inter-story drifts for: (<b>a</b>) K2E; (<b>b</b>) CE.</p>
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<p>Comparison of maximum inter-story drifts for: LE.</p>
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25 pages, 6663 KiB  
Article
Optimization of Dynamic Characteristics of Rubber-Based SMA Composite Dampers Using Multi-Body Dynamics and Response Surface Methodology
by Yizhe Huang, Qiyuan Fan, Huizhen Zhang, Lefei Shao and Yuanyuan Shi
Appl. Sci. 2024, 14(21), 10063; https://doi.org/10.3390/app142110063 - 4 Nov 2024
Viewed by 983
Abstract
The suspension system of a commercial vehicle cab plays a crucial role in enhancing ride comfort by mitigating vibrations. However, conventional rubber suspension systems have relatively fixed stiffness and damping properties, rendering them inflexible to load variations and resulting in suboptimal ride comfort [...] Read more.
The suspension system of a commercial vehicle cab plays a crucial role in enhancing ride comfort by mitigating vibrations. However, conventional rubber suspension systems have relatively fixed stiffness and damping properties, rendering them inflexible to load variations and resulting in suboptimal ride comfort under extreme road conditions. Shape memory alloys (SMAs) represent an innovative class of intelligent materials characterized by superelasticity, shape memory effects, and high damping properties. Recent advancements in materials science and engineering technology have focused on rubber-based SMA composite dampers due to their adjustable stiffness and damping through temperature or strain rate. This paper investigates how various structural parameters affect the stiffness and damping characteristics of sleeve-type rubber-based SMA composite vibration dampers. We developed a six-degree-of-freedom vibration differential equation and an Adams multi-body dynamics model for the rubber-based SMA suspension system in commercial vehicle cabins. We validated the model’s reliability through theoretical analysis and simulation comparisons. To achieve a 45% increase in stiffness and a 64.5% increase in damping, we optimized the suspension system’s z-axis stiffness and damping parameters under different operating conditions. This optimization aimed to minimize the z-axis vibration acceleration at the driver’s seat. We employed response surface methodology to design the composite shock absorber structure and then conducted a comparative analysis of the vibration reduction performance of the optimized front and rear suspension systems. This study provides significant theoretical foundations and practical guidelines for enhancing the performance of commercial vehicle cab suspension systems. Full article
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<p>Cross-section view of rubber-based SMA composite vibration damper [<a href="#B12-applsci-14-10063" class="html-bibr">12</a>].</p>
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<p>Stress-displacement curves corresponding to SMA metal modules with different thickness and diameters: (<b>a</b>) different thicknesses; (<b>b</b>) different diameters.</p>
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<p>The variation curves of stiffness and damping with the thickness and diameter of SMA metal modules: (<b>a</b>) SMA metal module thickness; (<b>b</b>) SMA metal module diameter.</p>
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<p>Force-displacement curves during loading and unloading process corresponding to different thicknesses of outer rubber damping layers.</p>
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<p>Curve of stiffness and damping characteristics of rubber-based SMA composite shock absorber with the thickness of outer rubber damping components.</p>
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<p>Force-displacement curves during loading and unloading process corresponding to different widths of shock absorbers.</p>
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<p>Curve of stiffness and damping characteristics of rubber-based SMA composite shock absorber with respect to the width of the shock absorber.</p>
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<p>Vibration model of the cab vibration subsystem.</p>
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<p>Adams multi-body dynamics model of cab suspension system.</p>
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<p>Comparison between the Adams z-direction displacement of the seat and numerical calculation results: (<b>a</b>) time-domain response; (<b>b</b>) frequency-domain response.</p>
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<p>Time-domain response of seat z-direction displacement under different loading rates.</p>
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<p>Time-domain response of seat z-direction acceleration under different loading rates.</p>
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<p>Adams iterative optimization process for the root mean square value of seat z-direction acceleration.</p>
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<p>Iterative optimization process of seat z-direction acceleration.</p>
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<p>Iterative optimization process of seat z-direction displacement.</p>
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<p>Response surface graph of z-direction stiffness and diameter and loading rate of SMA metal module.</p>
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<p>Response surface graph of z-direction damping and diameter and loading rate of SMA metal module.</p>
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<p>Comparison of cross-sectional views of rubber-based SMA composite dampers before and after optimization: (<b>a</b>) before optimization; (<b>b</b>) after optimization.</p>
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<p>Comparison of optimized stiffness and damping with target stiffness and damping under different loading rates: (<b>a</b>) stiffness; (<b>b</b>) damping.</p>
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<p>Comparison of <span class="html-italic">z</span>-axis acceleration response of seats with a loading rate of 120 mm/s before and after optimization.</p>
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<p>Comparison of <span class="html-italic">z</span>-axis acceleration response of seats with a loading rate of 600 mm/s before and after optimization.</p>
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13 pages, 5075 KiB  
Article
Friction and Wear Resistance of Nanostructured TiNi Shape Memory Alloy
by Alexandr Dmitrievskiy, Victor Komarov, Roman Karelin, Vladimir Andreev and Vladimir Stolyarov
Metals 2024, 14(11), 1248; https://doi.org/10.3390/met14111248 - 3 Nov 2024
Viewed by 399
Abstract
TiNi shape memory alloys with a superelastic effect are widely used in tribological interfaces requiring high wear resistance. One of the common approaches to reducing the wear of various metals is the application of severe plastic deformation (SPD), resulting in structural refinement and [...] Read more.
TiNi shape memory alloys with a superelastic effect are widely used in tribological interfaces requiring high wear resistance. One of the common approaches to reducing the wear of various metals is the application of severe plastic deformation (SPD), resulting in structural refinement and corresponding hardening. This paper investigates the tribological behaviour of a nanostructured Ti49.3Ni50.7 shape memory alloy produced using SPD. The friction and wear characteristics of the alloy at room temperature are compared in the coarse-grained, nanostructured, and nanostructured aged states. Through hardness measurement and transmission electron microscopy, it is shown that the transformation of a coarse-grained state into a nanostructured state increases wear resistance and hardness, reduces the coefficient of friction, and changes the friction mechanism. Formed nanoparticles during ageing in a nanostructured state further increase wear resistance. Full article
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<p>Microstructure of TiNi SMA in different structural states: (<b>a</b>)—CG, (<b>b</b>)—NS and (<b>c</b>)—NS + ageing.</p>
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<p>DSC curves of TiNi SMA in different structural states: (<b>a</b>)—CG, (<b>b</b>)—NS and (<b>c</b>)—NS + ageing.</p>
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<p>Hardness of TiNi SMA in different structural states: 1—CG, 2—NS and 3—NS + ageing.</p>
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<p>Dependence of the friction coefficient of TiNi SMA on the number of cycles in the studied structural states: 1—CG, 2—NS and 3—NS + ageing. The insets show microphotographs of counterbody wear marks.</p>
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<p>Profilograms of track cross-sections (<b>a</b>–<b>c</b>) and the ratio of wear rates (<b>d</b>) of TiNi SMA in studied structural states. 1—CG, 2—NS, and 3—NS + ageing. Profilograms 2 and 3 are shifted along the ordinate by 2.5 μm and 5.75 μm, respectively, to avoid line intersections.</p>
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<p>SEM images of wear track areas in TiNi SMA in studied structural states 1 (<b>a</b>,<b>b</b>), 2 (<b>c</b>,<b>d</b>), and 3 (<b>e</b>,<b>f</b>).</p>
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<p>Distribution of signal intensities (energy dispersive spectrometry) from (1) Ti, (2) Ni, (3) O, and (4) Al along a line normally cutting the wear track of a TiNi alloy in an NS state (<b>a</b>) and an NS aged state (<b>b</b>).</p>
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13 pages, 7299 KiB  
Article
Thermal Cycling Behavior of Aged FeNiCoAlTiNb Cold-Rolled Shape Memory Alloys
by Li-Wei Tseng and Wei-Cheng Chen
Micromachines 2024, 15(11), 1338; https://doi.org/10.3390/mi15111338 - 31 Oct 2024
Viewed by 463
Abstract
Fe–Ni–Co–Al-based systems have attracted a lot of interest due to their large recoverable strain. In this study, the microstructure and thermal cycling behaviors of Fe41Ni28Co17Al11.5Ti1.25Nb1.25 (at.%) 98.5% cold-rolled alloys after annealing treatment [...] Read more.
Fe–Ni–Co–Al-based systems have attracted a lot of interest due to their large recoverable strain. In this study, the microstructure and thermal cycling behaviors of Fe41Ni28Co17Al11.5Ti1.25Nb1.25 (at.%) 98.5% cold-rolled alloys after annealing treatment at 1277 °C for 1 h, followed by aging for 48 h at 600 °C, were investigated. From the electron backscatter diffraction results, we see that the texture intensity increased from 9.4 to 16.5 mud and the average grain size increased from 300 to 400 μm as the annealing time increased from 0.5 h to 1 h. The hardness results for different aging heat treatment conditions show the maximum value was reached for samples aged at 600 °C for 48 h (peak aging condition). The orientation distribution functions (ODFs) displayed by Goss, brass, and copper were the main textural features in the FeNiCoAlTiNb cold-rolled alloy. After annealing, strong Goss and brass textures were formed. The transmission electron microscopy (TEM) results show that the precipitate size was ~10 nm. The X-ray diffraction (XRD) results show a strong peak in the (111) and (200) planes of the austenite (⁠⁠γ, FCC) structure for the annealed sample. After aging, a new peak in the (111) plane of the precipitate (⁠⁠γ′, L12) structure emerged, and the peak intensity of austenite (⁠⁠γ, FCC) decreased. The magnetization–temperature curves of the aged sample show that both the magnetization and transformation temperature increased with the increasing magnetic fields. The shape memory properties show a fully recoverable strain of up to 2% at 400 MPa stress produced in the three-point bending test. However, the experimental recoverable strain values were lower than the theoretical values, possibly due to the fact that the volume fraction of the low-angle grain boundary (LABs) was small compared to the reported values (60%), and it was insufficient to suppress the beta phases. The beta phases made the grain boundaries brittle and deteriorated the ductility. On the fracture surface of samples after the three-point bending test, the fracture spread along the grain boundary, and the cross-section microstructural results show that the faces of the grain boundary were smooth, indicating that the grain boundary was brittle with an intergranular fracture. Full article
(This article belongs to the Special Issue Shape Memory Alloys: Manufacturing and Micromachined Applications)
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<p>EBSD pattern of the FeNiCoAlTiNb cold-rolled alloys annealed at 1277 °C for (<b>a</b>) 0.5 h and (<b>b</b>) 1 h. (<b>c</b>) BSE image and (<b>d</b>) grain boundary misorientation of the 98.5%CR + 1277 °C, 1 h sample. RD (rolling direction), TD (transverse direction), and ND (normal direction).</p>
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<p>EBSD pattern of the FeNiCoAlTiNb cold-rolled alloys annealed at 1277 °C for (<b>a</b>) 0.5 h and (<b>b</b>) 1 h. (<b>c</b>) BSE image and (<b>d</b>) grain boundary misorientation of the 98.5%CR + 1277 °C, 1 h sample. RD (rolling direction), TD (transverse direction), and ND (normal direction).</p>
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<p>ODFs of the FeNiCoAlTiNb cold-rolled alloys: (<b>a</b>) 98.5%CR and (<b>b</b>) 98.5%CR + 1277 °C, 1 h.</p>
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<p>Hardness of a FeNiCoAlTiNb 98.5%CR with a different aging treatment duration.</p>
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<p>XRD pattern for FeNiCoAlTiNb cold-rolled alloys under different thermomechanical processing times.</p>
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<p>TEM images of the aged FeNiCoAlTiNb sample: (<b>a</b>) BF TEM image and (<b>b</b>) SAED pattern. The white circle shows the size of the precipitate.</p>
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<p>Magnetization vs. temperature at various levels of magnetic field for the aged FeNiCoAlTiNb sample: (<b>a</b>) 0.05 T, (<b>b</b>) 1, 3, 5, and 7 T. (<b>c</b>) Magnetic field vs. magnetization response and (<b>d</b>) magnetic field vs. temperature response.</p>
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<p>Shape memory characteristics of three-point bending test for the aged FeNiCoAlTiNb sample: (<b>a</b>) illustration of how to obtain recoverable strain, irrecoverable strain, and transformation temperatures from thermal cyclic tests, (<b>b</b>) strain vs. temperatures under different applied stress values, (<b>c</b>) recoverable and irrecoverable strains at various stress, and (<b>d</b>) stress vs. transformation temperatures responses.</p>
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<p>An optical microscope image of an aged sample: (<b>a</b>) before and (<b>b</b>) after the three-point bending test. (<b>c</b>,<b>d</b>) show high-magnification BSE images of the cross-sections of three-point bending fracture surfaces.</p>
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15 pages, 9503 KiB  
Article
A Multi-Posture Grasping Manipulator Actuated by Shape Memory Alloy with Different Functional Modules
by Xiaozheng Li and Chongjing Cao
Micromachines 2024, 15(11), 1328; https://doi.org/10.3390/mi15111328 - 30 Oct 2024
Viewed by 503
Abstract
Currently, multi-posture robots have complex grasping robotic manipulators with low power density, making it difficult to miniaturize and integrate. In this paper, a multi-posture grasping manipulator actuated by shape memory alloy with different functional modules is presented. It is composed of deflection, translation, [...] Read more.
Currently, multi-posture robots have complex grasping robotic manipulators with low power density, making it difficult to miniaturize and integrate. In this paper, a multi-posture grasping manipulator actuated by shape memory alloy with different functional modules is presented. It is composed of deflection, translation, rotation and grasping modules. Based on a D-H parameter method, the end motion trajectory model is established and the end motion space is drawn. Finally, the grasping experiment of a light circular object is carried out to verify the validity of the multi-posture grasping function of the multi-module combination manipulator, which provides a choice for future intelligent robot manipulators. Full article
(This article belongs to the Special Issue Soft Actuators: Design, Fabrication and Applications, 2nd Edition)
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<p>Typical multi-posture grasping manipulator schematic diagram.</p>
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<p>Functional implementation principles and control diagrams in different modules [<a href="#B27-micromachines-15-01328" class="html-bibr">27</a>,<a href="#B28-micromachines-15-01328" class="html-bibr">28</a>,<a href="#B29-micromachines-15-01328" class="html-bibr">29</a>]: (<b>a</b>) deflection function module; (<b>b</b>) translation function module and (<b>c</b>) rotation function module; (<b>d</b>) winding module; (<b>e</b>) grasping function module; (<b>f</b>) schematic diagram of overall structural control and (<b>g</b>) schematic diagram of SMA actuation control for each module.</p>
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<p>Schematic diagram of two adjacent links of the multi-posture manipulator [<a href="#B30-micromachines-15-01328" class="html-bibr">30</a>,<a href="#B31-micromachines-15-01328" class="html-bibr">31</a>]. Adapted with permission from Refs. [<a href="#B30-micromachines-15-01328" class="html-bibr">30</a>,<a href="#B31-micromachines-15-01328" class="html-bibr">31</a>].</p>
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<p>Simplified kinematic model of a multi-posture grasping manipulator: (<b>a</b>) geometric model; (<b>b</b>) abstract linkage joint model; and (<b>c</b>) kinematics model.</p>
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<p>The analysis process of end motion trajectory space of the multi-posture grasping manipulator.</p>
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<p>Multi-posture grasping manipulator end motion trajectory space.</p>
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<p>Test pieces for multi-posture grasping manipulator and each functional module: (<b>a</b>) the multi-posture grasping manipulator; (<b>b</b>) the base with rotational function module; (<b>c</b>) the translational function module; (<b>d</b>) the deflection function module; and (<b>e</b>) the connection plate with grasping function module.</p>
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<p>Simulation and experimental comparison of multi-posture grasping manipulator deflection function module during actuation: (<b>a</b>) upward deflection; (<b>b</b>) initial state; and (<b>c</b>) downward deflection.</p>
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<p>Simulation and experimental comparison of the multi-posture grasping manipulator rotating (translational and rotational) function module during actuation: (<b>a</b>) counterclockwise rotation; (<b>b</b>) initial state; and (<b>c</b>) clockwise rotation.</p>
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<p>Simulation and experimental comparison of the multi-posture grasping manipulator deflection function module during actuation: (<b>a</b>) translation down + upward deflection; (<b>b</b>) initial state; and (<b>c</b>) translation down + downward deflection.</p>
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<p>Simulation and experimental comparison of multi-posture grasping manipulator: (<b>a</b>) deflection; (<b>b</b>) rotation; and (<b>c</b>) translation down with deflection.</p>
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<p>The multi-posture grasping manipulator grasping a ball under the actuation of different functional modules: (<b>a</b>) upward deflection; (<b>b</b>) initial state; (<b>c</b>) downward deflection; (<b>d</b>) counterclockwise rotation; (<b>e</b>) initial state; (<b>f</b>) clockwise rotation; (<b>g</b>) translation down + upward deflection; (<b>h</b>) initial state; and (<b>i</b>) translation down + downward deflection.</p>
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20 pages, 5089 KiB  
Article
A Two-Finger Gripper Actuated by Shape Memory Alloy for Applications in Automation Technology with Minimized Installation Space
by Tobias Schmelter, Lukas Bade and Bernd Kuhlenkötter
Actuators 2024, 13(10), 425; https://doi.org/10.3390/act13100425 - 21 Oct 2024
Viewed by 782
Abstract
The increasing demand for innovative grippers and actuators for the automation sector encourages the development of new and innovative functional principles. Intelligent materials are particularly suitable for this purpose based on their high energy density. In this study, a two-finger gripper driven by [...] Read more.
The increasing demand for innovative grippers and actuators for the automation sector encourages the development of new and innovative functional principles. Intelligent materials are particularly suitable for this purpose based on their high energy density. In this study, a two-finger gripper driven by shape memory alloys (SMA) for use in automation technology is presented. Previous grippers driven by SMA can only be found in the field of micro gripping due to the limited stroke generated by SMA. Based on a methodical product development, a new type of gripper was developed and is presented in this study, which can achieve an opening width comparable to conventional grippers based on transmission mechanisms. Two different variants of the gripper are shown and compared aiming to minimize the installation space and weight of the gripper. In addition to the design presentation, a prototype is built, and the functionality is demonstrated through various test series. Full article
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<p>Representation of the thermal SME with the associated transformation temperatures and the lattice structure of NiTi.</p>
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<p>Schematic representation of an exemplary gripper system and its components (own presentation) [<a href="#B24-actuators-13-00425" class="html-bibr">24</a>].</p>
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<p>Kinematic system of the new gripper design.</p>
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<p>Sketch for calculation of the holding arms.</p>
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<p>Sketch for calculation of the lever arms.</p>
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<p>CAD illustration of the gripper with list of parts.</p>
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<p>Evaluation of the opening width in CAD (<b>a</b>) fully opened (<b>b</b>) closed.</p>
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<p>Force curve of wire and counter spring.</p>
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<p>Force curve via gearwheel and pinion to the gripper fingers.</p>
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<p>Size comparison of the two gripper variants (<b>a</b>) with installation space not reduced and (<b>b</b>) with installation space reduced.</p>
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<p>Optimized version of the gripper in CAD with weight reduction, deflection, and fan.</p>
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<p>Pictures of the prototype with different opening widths, which were set mechanically and not by an SMA wire. (<b>a</b>) Fully closed; (<b>b</b>) 30 mm opened; (<b>c</b>) maximum opening width of 50 mm. A video of the actuator in operation can be found in the <a href="#app1-actuators-13-00425" class="html-app">Supplementary Material</a>.</p>
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<p>Opening width of the gripper over the first 30 cycles.</p>
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<p>Opening width of the gripper at different cooling speeds with and without a fan.</p>
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<p>Minimum and maximum opening width of the gripper in a long-term test over the lifetime of the wire.</p>
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<p>Resulting opening width with compensation line over the lifetime of the wire.</p>
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13 pages, 3078 KiB  
Article
Machine-Learning-Driven Design of High-Elastocaloric NiTi-Based Shape Memory Alloys
by Yingyu Gao, Yunfeng Hu, Xinpeng Zhao, Yang Liu, Haiyou Huang and Yanjing Su
Metals 2024, 14(10), 1193; https://doi.org/10.3390/met14101193 - 20 Oct 2024
Viewed by 710
Abstract
In recent years, the detrimental impact of traditional gas–liquid refrigerants on the environment has prompted a shift towards sustainable solid-state refrigeration technology. The elastocaloric effect, particularly in NiTi-based shape memory alloys (SMAs), presents a promising alternative due to its high coefficient of performance. [...] Read more.
In recent years, the detrimental impact of traditional gas–liquid refrigerants on the environment has prompted a shift towards sustainable solid-state refrigeration technology. The elastocaloric effect, particularly in NiTi-based shape memory alloys (SMAs), presents a promising alternative due to its high coefficient of performance. However, conventional methods for alloy development are inefficient, often failing to meet the stringent requirements for practical applications. This study employed machine learning (ML) to accelerate the design of NiTi-based SMAs with an enhanced elastocaloric effect. Through active learning across four iterations, we identified nine novel NiTi-based SMAs exhibiting phase-transformation-induced entropy changes (ΔS) greater than 90 J/kg·K−1, surpassing most existing alloys. Our ML model demonstrates robust interpretability, revealing key relationships between material features and performance. This work not only establishes a more efficient pathway for alloy discovery but also aims to contribute significantly to the advancement of sustainable refrigeration technologies. Full article
(This article belongs to the Special Issue Machine Learning Models in Metals)
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<p>A schematic of the machine-learning-based iterative design loop for accelerated design of high-elastocaloric NiTi-based SMAs.</p>
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<p>Characterization and model selection for the physical and chemical characteristic model (M1). (<b>a</b>) Pearson correlation matrix for the initial 60 descriptors. (<b>b</b>) Model selection based on leave-out cross-validation. (<b>c</b>) Cross-validation error from SVR.rbf model containing a subset of the retained descriptors. (<b>d</b>) The prediction performance of M1. (<b>e</b>) Results of 4 iterations of active learning based on M1.</p>
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<p>Characterization and model selection for the physical and chemical characteristic model (M1). (<b>a</b>) Pearson correlation matrix for the initial 60 descriptors. (<b>b</b>) Model selection based on leave-out cross-validation. (<b>c</b>) Cross-validation error from SVR.rbf model containing a subset of the retained descriptors. (<b>d</b>) The prediction performance of M1. (<b>e</b>) Results of 4 iterations of active learning based on M1.</p>
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<p>Characteristics and model selection for physical and chemical characteristics combined with heat treatment process characteristic model (M2). (<b>a</b>) Pearson correlation matrix for the initial 29 descriptors. (<b>b</b>) Model selection based on leave-out cross-validation. (<b>c</b>) The prediction performance of M2.</p>
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<p>Characteristics and model selection for physical and chemical characteristics combined with heat treatment process characteristic model (M2). (<b>a</b>) Pearson correlation matrix for the initial 29 descriptors. (<b>b</b>) Model selection based on leave-out cross-validation. (<b>c</b>) The prediction performance of M2.</p>
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<p>Results of K-Means clustering model M3. (<b>a</b>) The best models for each clustering subset and their <span class="html-italic">R</span><sup>2</sup> and RMSE values. (<b>b</b>) The prediction performance of M3.</p>
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<p>Fitting results of M1 (<b>a</b>), M2 (<b>b</b>), and M3 (<b>c</b>) on new validation data.</p>
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12 pages, 3719 KiB  
Article
Influence of β-Stabilizing Nb on Phase Stability and Phase Transformation in Ti-Zr Shape Memory Alloys: From the Viewpoint of the First-Principles Calculation
by Xinxin Feng, Xuepei Chen, Xiaoyang Yi, Weijian Li, Chenguang Liu, Xianglong Meng, Zhiyong Gao, Xinjian Cao and Haizhen Wang
Metals 2024, 14(10), 1192; https://doi.org/10.3390/met14101192 - 20 Oct 2024
Viewed by 576
Abstract
In the present study, the effect of the Nb element on the lattice parameters, phase stability and martensitic transformation behaviors of Ti-Zr-based shape memory alloys was extensively investigated using the first-principles calculation. The lattice parameters of both the β parent phase and α′ [...] Read more.
In the present study, the effect of the Nb element on the lattice parameters, phase stability and martensitic transformation behaviors of Ti-Zr-based shape memory alloys was extensively investigated using the first-principles calculation. The lattice parameters of both the β parent phase and α′ martensite phase gradually decreased with Nb content increasing. For the α″ martensite phase, the lattice constant (a) gradually increased with the increase in Nb content, whereas the lattice constants (b and c) continuously decreased due to the addition of Nb. Based on the formation energy and density of state, β→α′ martensitic transformation occurred, as the Nb content was not more than 12.5 at.%. However, the Ti-Zr-Nb shape memory alloys with a Nb content higher than 12.5 at.% possessed the β→α″ martensitic transformation. However, both the largest transformation strain and sensitivity of critical stress to temperature (dσ/dT) can be optimized by controlling 12.5 at.% Nb in the Ti-Zr-Nb shape memory alloy, which was favorable to obtaining the largest elastocaloric effect. Full article
(This article belongs to the Special Issue Manufacture, Properties and Applications of Light Alloys)
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<p>The cell model of (<b>a</b>–<b>e</b>) β phase; (<b>f</b>–<b>j</b>) α′ phase; and (<b>k</b>–<b>o</b>) α″ phase in Ti-Zr-Nb shape memory alloys with the various Nb contents (dark represents Ti atom, green represents Zr atom and pink represents Nb atom). (<b>a</b>) β-Ti-25Zr; (<b>b</b>) β-Ti-18.75Zr-6.25Nb; (<b>c</b>) β-Ti-12.5Zr-12.5Nb; (<b>d</b>) β-Ti-6.25Zr-18.75Nb; (<b>e</b>) β-Ti-25Nb; (<b>f</b>) α’-Ti-25Zr; (<b>g</b>) α’-Ti-18.75Zr-6.25Nb; (<b>h</b>) α’-Ti-12.5Zr-12.5Nb; (<b>i</b>) α’-Ti-6.25Zr-18.75Nb; (<b>j</b>) α’-β-Ti-25Nb; (<b>k</b>) α’’-Ti-25Zr; (<b>l</b>) α’’-Ti-18.75Zr-6.25Nb; (<b>m</b>) α’’-Ti-12.5Zr-12.5Nb; (<b>n</b>) α’’-Ti-6.25Zr-18.75Nb; and (<b>o</b>) α’’-Ti-25Nb.</p>
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<p>The formation energy of β parent phase, α′ martensite phase and α″ martensite phase of Ti-Zr-Nb shape memory alloys with different Nb contents.</p>
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<p>The total and partial DOSs of β phase for Ti-Zr-Nb shape memory alloys with various Nb contents.</p>
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<p>The total and partial DOSs of α′ phase for Ti-Zr-Nb shape memory alloys with various Nb contents.</p>
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<p>The total and partial DOSs of α″ phase for Ti-Zr-Nb shape memory alloys with various Nb contents.</p>
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<p>The effect of Nb content on the total DOS at EF of the β parent phase, α′ martensite phase and α″ martensite phase in Ti-Zr-Nb shape memory alloys.</p>
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<p>The effect of Nb content on the lattice parameters of β parent phase, α′ martensite phase and α″ martensite phase in Ti-Zr-Nb shape memory alloys.</p>
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<p>Effect of Nb content on (<b>a</b>) the principal lattice strain and (<b>b</b>) transformation strain of Ti-Zr-Nb shape memory alloys.</p>
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<p>The free energy difference between β phase and α″ martensite phase under the different applied stress conditions in (<b>a</b>) Ti-18.75Zr-6.25Nb alloy and (<b>b</b>) Ti-12.5Zr-12.5Nb alloy.</p>
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15 pages, 3757 KiB  
Article
The Effect of Fe Content on the Shape Memory Effect of Ni-Mn-Ga-Fe Shape Memory Alloy Microwires after Ordering Heat Treatment
by Yanfen Liu, Zixuan Ma, Shuang Li, Puhan Yan, Qingnan Hou and Jianfei Sun
Metals 2024, 14(10), 1167; https://doi.org/10.3390/met14101167 - 12 Oct 2024
Viewed by 619
Abstract
The shape memory capabilities of Heusler alloy microwires with two different contents of Fe element instead of Ga element following step-by-step ordering heat treatment were explored based on the stoichiometric ratio of Ni2MnGa. The melt-drawing technique was used to create the [...] Read more.
The shape memory capabilities of Heusler alloy microwires with two different contents of Fe element instead of Ga element following step-by-step ordering heat treatment were explored based on the stoichiometric ratio of Ni2MnGa. The melt-drawing technique was used to create the polycrystalline microwires, and the two microwires had Fe atomic contents of 4.7 at.% and 5.5 at.%, respectively. The field emission scanning electron microscope was used to analyze the microwire’s surface condition as well as the microscopic tensile fracture morphology. Using an X-ray diffractometer, the microwires’ crystal structure was identified for phase analysis. Differential scanning calorimetry was used to examine the microwires’ behavior during martensitic transformation. Using a dynamic mechanical stretcher, the elongation and recovery rate of microwires’ one- and two-way shape memory behavior were examined. The findings demonstrated that the microwire phase structure, martensitic transformation behavior, and shape memory capabilities all displayed good properties after the heat treatment was ordered. Full article
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<p>(<b>a</b>) The diagram of melt drawing equipment schematic; (<b>b</b>) the diagram of step-by-step ladder ordered heat-treated schematic.</p>
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<p>SEM diagram of ordered heat-treated microwire: Microwire morphology at low magnification (<b>a</b>); Ni<sub>49.3</sub>Mn<sub>24.9</sub>Ga<sub>21.1</sub>Fe<sub>4.7</sub> microwire cross-section fracture diagram (<b>b</b>); Ni<sub>49.9</sub>Mn<sub>24.7</sub>Ga<sub>19.9</sub>Fe<sub>5.5</sub> microwire cross-section fracture diagram (<b>c</b>); free solidification circle surface microstructure (<b>d</b>); microwire flat surface grain (<b>e</b>); Ni<sub>49.3</sub>Mn<sub>24.9</sub>Ga<sub>21.1</sub>Fe<sub>4.7</sub> microwire modulation structure (<b>f</b>); Ni<sub>49.9</sub>Mn<sub>24.7</sub>Ga<sub>19.9</sub>Fe<sub>5.5</sub> microwire modulation structure (<b>g</b>).</p>
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<p>XRD diffraction patterns of microwires after ordering heat treatment: (<b>a</b>) Ni<sub>49.3</sub>Mn<sub>24.9</sub>Ga<sub>21.1</sub>Fe<sub>4.7</sub> microwire; (<b>b</b>) Ni<sub>49.9</sub>Mn<sub>24.7</sub>Ga<sub>19.9</sub>Fe<sub>5.5</sub> microwire.</p>
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<p>DSC diagram of two kinds of microwire ordering heat treatment: (<b>a</b>) Ni<sub>49.3</sub>Mn<sub>24.9</sub>Ga<sub>21.1</sub>Fe<sub>4.7</sub> microwire; (<b>b</b>) Ni<sub>49.9</sub>Mn<sub>24.7</sub>Ga<sub>19.9</sub>Fe<sub>5.5</sub> microwire.</p>
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<p>One-way curve stretching and shape recovery of ordered heat-treated microwires: (<b>a</b>) Ni<sub>49.3</sub>Mn<sub>24.9</sub>Ga<sub>21.1</sub>Fe<sub>4.7</sub> microwire; (<b>b</b>) Ni<sub>49.9</sub>Mn<sub>24.7</sub>Ga<sub>19.9</sub>Fe<sub>5.5</sub> microwire.</p>
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<p>Two-way stretching and shape recovery of ordered heat-treated microwires: Ni<sub>49.3</sub>Mn<sub>24.9</sub>Ga<sub>21.1</sub>Fe<sub>4.7</sub> microwire (<b>a</b>); Ni<sub>49.9</sub>Mn<sub>24.7</sub>Ga<sub>19.9</sub>Fe<sub>5.5</sub> microwire (<b>b</b>).</p>
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<p>Stress–temperature diagram of ordered heat-treated microwire: Ni<sub>49.3</sub>Mn<sub>24.9</sub>Ga<sub>21.1</sub>Fe<sub>4.7</sub> microwire (<b>a</b>): Ni<sub>49.9</sub>Mn<sub>24.7</sub>Ga<sub>19.9</sub>Fe<sub>5.5</sub> microwire (<b>b</b>).</p>
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16 pages, 5805 KiB  
Article
Numerical and Experimental Study of a Wearable Exo-Glove for Telerehabilitation Application Using Shape Memory Alloy Actuators
by Mohammad Sadeghi, Alireza Abbasimoshaei, Jose Pedro Kitajima Borges and Thorsten Alexander Kern
Actuators 2024, 13(10), 409; https://doi.org/10.3390/act13100409 - 11 Oct 2024
Viewed by 920
Abstract
Hand paralysis, caused by conditions such as spinal cord injuries, strokes, and arthritis, significantly hinders daily activities. Wearable exo-gloves and telerehabilitation offer effective hand training solutions to aid the recovery process. This study presents the development of lightweight wearable exo-gloves designed for finger [...] Read more.
Hand paralysis, caused by conditions such as spinal cord injuries, strokes, and arthritis, significantly hinders daily activities. Wearable exo-gloves and telerehabilitation offer effective hand training solutions to aid the recovery process. This study presents the development of lightweight wearable exo-gloves designed for finger telerehabilitation. The prototype uses NiTi shape memory alloy (SMA) actuators to control five fingers. Specialized end effectors target the metacarpophalangeal (MCP), proximal interphalangeal (PIP), and distal interphalangeal (DIP) joints, mimicking human finger tendon actions. A variable structure controller, managed through a web-based Human–Machine Interface (HMI), allows remote adjustments. Thermal behavior, dynamics, and overall performance were modeled in MATLAB Simulink, with experimental validation confirming the model’s efficacy. The phase transformation characteristics of NiTi shape memory wire were studied using the Souza–Auricchio model within COMSOL Multiphysics 6.2 software. Comparing the simulation to trial data showed an average error of 2.76°. The range of motion for the MCP, PIP, and DIP joints was 21°, 65°, and 60.3°, respectively. Additionally, a minimum torque of 0.2 Nm at each finger joint was observed, which is sufficient to overcome resistance and meet the torque requirements. Results demonstrate that integrating SMA actuators with telerehabilitation addresses the need for compact and efficient wearable devices, potentially improving patient outcomes through remote therapy. Full article
(This article belongs to the Special Issue Shape Memory Alloy (SMA) Actuators and Their Applications)
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<p>Illustration of the human finger movement mechanism and various joint structures.</p>
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<p>(<b>a</b>) Fabricated exoskeleton glove, (<b>b</b>) Control and power system, (<b>c</b>–<b>e</b>) Various end effectors designed for the treatment of the MCP, PIP, and DIP joints, respectively.</p>
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<p>Linkage mechanism: (<b>a</b>) Side view, (<b>b</b>) Four-bar model, (<b>c</b>) Hollow disks friction model.</p>
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<p>Schematic representation of the Simulink system model.</p>
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<p>Measurement apparatus for evaluating dynamic finger movements.</p>
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<p>(<b>a</b>) Schematic depiction of the Grip Sensor and test objects, (<b>b</b>) Calibration results.</p>
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<p>Comparison of simulation and experimental test for a profile input.</p>
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<p>Stress–temperature phase diagrams for NiTi shape memory alloy wire: (<b>a</b>) Under different constant DC voltage stimulation, (<b>b</b>) Under PWM stimulation signals. The color legend indicates the martensite volume fraction.</p>
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<p>Experimental results of finger movement measurements at different input speeds, with transparent margins indicating the measurement error bands.</p>
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<p>Experimental results of the joint displacements for all fingers: (<b>a</b>) Metacarpophalangeal (MCP) joint, (<b>b</b>) Proximal Interphalangeal (PIP) joint, and (<b>c</b>) Distal Interphalangeal/Interphalangeal (DIP/IP) joint.</p>
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<p>Experimental results of the torque measurement for all fingers: (<b>a</b>) Metacarpophalangeal (MCP) joint; (<b>b</b>) Proximal Interphalangeal (PIP) joint, and (<b>c</b>) Distal Interphalangeal/Interphalangeal (DIP/IP) joint.</p>
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13 pages, 4856 KiB  
Article
Preparation and Characterization of Ni-Mn-Ga-Cu Shape Memory Alloy with Micron-Scale Pores
by Kunyu Wang, Zhiqiang Wang, Yunlong Li, Jie Zhu and Zhiyi Ding
Metals 2024, 14(10), 1155; https://doi.org/10.3390/met14101155 - 10 Oct 2024
Viewed by 653
Abstract
Porous Ni-Mn-Ga shape memory alloys (SMAs) were prepared by powder metallurgy using NaCl as a pore-forming agent with an average pore size of 20–30 μm. The microstructure, phase transformation, superelasticity, and elastocaloric properties of the porous alloys were investigated. The prepared porous alloy [...] Read more.
Porous Ni-Mn-Ga shape memory alloys (SMAs) were prepared by powder metallurgy using NaCl as a pore-forming agent with an average pore size of 20–30 μm. The microstructure, phase transformation, superelasticity, and elastocaloric properties of the porous alloys were investigated. The prepared porous alloy had a uniform pore distribution and interconnected microchannels were formed. Cu doping can effectively improve the toughness of a porous alloy, thus improving the superelasticity. It was found that porous Ni-Mn-Ga-Cu SMAs have a flat stress plateau, which exhibits a maximum elongation of 5% with partially recoverable strain and a critical stress for martensite transformation as low as about 160 MPa. In addition, an adiabatic temperature change of 0.6 K was obtained for the prepared porous alloy at a strain of 1.2% at about 150 MPa. This work confirms that the introduction of porous structures into polycrystalline Ni-Mn-Ga SMAs is an effective way to reduce costs and improve performance, and provides opportunities for engineering applications. Full article
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<p>SEM image of (<b>a</b>) Ni-Mn-Ga-Cu alloy powder, (<b>b</b>) NaCl powder, and (<b>c</b>) Ni-Mn-Ga-Cu porous alloy; morphology of porous alloy pores obtained by industrial CT. (<b>d</b>) Connected pores, (<b>e</b>) isolated pores, and (<b>f</b>) radial (<b>left</b>) and axial (<b>right</b>) cross-sectional CT scans.</p>
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<p>XRD curves of Cu0–3 (<b>a</b>) bulk; (<b>b</b>) as-milled powder; and (<b>c</b>) porous alloy. DSC curves of Cu0–3 (<b>d</b>) bulk; (<b>e</b>) as-milled powder; and (<b>f</b>) porous alloy.</p>
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<p>Stress–strain curve under cyclic increasing compression: (<b>a</b>) Cu0, (<b>b</b>) Cu2, and (<b>c</b>) Cu3 porous alloys; (<b>d</b>) Cu2 bulk alloy; (<b>e</b>) schematic of strain component decomposition; and (<b>f</b>) the ratio of strain components in Cu2 and Cu3 porous alloys.</p>
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<p>(<b>a</b>) Fracture morphology of Cu2 specimen; (<b>b</b>) intergranular fracture morphology (the blue box in (<b>a</b>)); (<b>c</b>) transgranular fracture morphology (the red box in (<b>a</b>)); (<b>d</b>) sintering neck containing martensitic lath; (<b>e</b>) EDS line scanning route on sintering neck; (<b>f</b>) intergranular fracture morphology of Cu0 specimen.</p>
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<p>TEM morphology of Cu2 porous alloy. (<b>a</b>) Interface between martensite and austenite; (<b>b</b>) 7M martensitic structure.</p>
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<p>(<b>a</b>) TEM micrograph of precipitates; (<b>b</b>) bright-field diagram of large precipitate; (<b>c</b>) HRTEM morphology at the boundaries of precipitates; (<b>d</b>,<b>e</b>) the corresponding selected electron diffraction patterns of martensite and precipitate.</p>
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<p>Comparison of critical stress and strain of martensite transformation in SMAs in other studies. The data were extracted from [<a href="#B1-metals-14-01155" class="html-bibr">1</a>,<a href="#B5-metals-14-01155" class="html-bibr">5</a>,<a href="#B17-metals-14-01155" class="html-bibr">17</a>,<a href="#B25-metals-14-01155" class="html-bibr">25</a>,<a href="#B34-metals-14-01155" class="html-bibr">34</a>,<a href="#B42-metals-14-01155" class="html-bibr">42</a>,<a href="#B43-metals-14-01155" class="html-bibr">43</a>,<a href="#B44-metals-14-01155" class="html-bibr">44</a>,<a href="#B45-metals-14-01155" class="html-bibr">45</a>,<a href="#B46-metals-14-01155" class="html-bibr">46</a>,<a href="#B47-metals-14-01155" class="html-bibr">47</a>,<a href="#B48-metals-14-01155" class="html-bibr">48</a>,<a href="#B49-metals-14-01155" class="html-bibr">49</a>,<a href="#B50-metals-14-01155" class="html-bibr">50</a>,<a href="#B51-metals-14-01155" class="html-bibr">51</a>,<a href="#B52-metals-14-01155" class="html-bibr">52</a>,<a href="#B53-metals-14-01155" class="html-bibr">53</a>,<a href="#B54-metals-14-01155" class="html-bibr">54</a>,<a href="#B55-metals-14-01155" class="html-bibr">55</a>].</p>
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<p>Time dependence of ΔT<sub>ad</sub> during loading and unloading of (<b>a</b>) Cu2 porous alloy and (<b>b</b>) Cu2 bulk alloy (the inner graphs show the corresponding stress–strain curve); (<b>c</b>) ΔT<sub>ad</sub> of Cu2 porous and bulk alloy during a cycle.</p>
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14 pages, 33689 KiB  
Article
Optimisation of Active Magnetic Elements in Beam-like Structures—Numerical Modelling Studies
by Katarzyna Majewska
Materials 2024, 17(19), 4929; https://doi.org/10.3390/ma17194929 - 9 Oct 2024
Viewed by 698
Abstract
This paper explores integrating advanced materials, including magnetic shape memory alloys, magnetorheological fluids, and classical shape memory alloys, within structural elements to achieve exceptional physical properties. When these materials are integrated within structures—whether as wires, actuators, or dampers—they provide the structures with unique [...] Read more.
This paper explores integrating advanced materials, including magnetic shape memory alloys, magnetorheological fluids, and classical shape memory alloys, within structural elements to achieve exceptional physical properties. When these materials are integrated within structures—whether as wires, actuators, or dampers—they provide the structures with unique static, dynamic, and damping characteristics not commonly found in nature. This study aimed to evaluate the efficacy of these active materials in enhancing the performance of beam-like structures. This investigation was conducted through a comprehensive numerical analysis, focusing on a composite beam. The study examined the impact of different active elements, their position within the structure, and their influence on key dynamic properties. Additionally, a simplified damage scenario was considered, wherein the adverse effects of structural damage were mitigated through the strategic application of these materials. Numerical simulations were carried out using the finite element method, with custom computational codes developed in MATLAB. The findings of these simulations are presented and discussed in this paper. Full article
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<p>Main groups of smart materials based on [<a href="#B1-materials-17-04929" class="html-bibr">1</a>,<a href="#B2-materials-17-04929" class="html-bibr">2</a>].</p>
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<p>Comparison of the number of papers (in %), related to the researcher’s interest, published in the last decades.</p>
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<p>(<b>a</b>) Object of investigation with geometry, (<b>b</b>) structure and working principle of actuators.</p>
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<p>Transverse displacement as a function of time: (<b>a</b>) SM alloy wires’ volume fraction (min = 0%, max = 100%), (<b>b</b>) reinforcement glass fibres’ volume fraction (min = 0%, max = 100%), and (<b>c</b>) angle of reinforcement fibre (min = 0°, max = 90°) based on [<a href="#B5-materials-17-04929" class="html-bibr">5</a>].</p>
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<p>Transverse displacement as a function of time: (<b>a</b>) MSM actuator’s excitation amplitude (min = 0 N, max = 1 N), (<b>b</b>) MSM actuator’s excitation frequency (min = 0 Hz, max = 10 Hz), and (<b>c</b>) MSM actuator’s phase angle (min = 0°, max = 360°) based on [<a href="#B5-materials-17-04929" class="html-bibr">5</a>].</p>
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<p>Transverse displacement as a function of time: (<b>a</b>) MR damper activation level (min = 0%, max = 100%), (<b>b</b>) angle of reinforcement glass fibre (min = 0°, max = 90°), and (<b>c</b>) reinforcement fibre volume fraction (min = 0%, max = 100%); based on [<a href="#B5-materials-17-04929" class="html-bibr">5</a>].</p>
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<p>Relative vibration energy as a function of MSM actuator position and excitation amplitude.</p>
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<p>Relative vibration energy as a function of the MR damper position and its activation level.</p>
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<p>Relative vibration energy as a function of the MSM actuator and damage position.</p>
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<p>Relative vibration energy as a function of damage position and intensity of damage plasticity.</p>
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<p>Relative vibration energy as a function of damage position and the MR damper activation level.</p>
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<p>Relative vibration energy as a function of damage position and intensity of damage plasticity.</p>
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