Performance of Variable Negative Stiffness MRE Vibration Isolation System

Li, Run-pu; Du, Cheng-bin; Guo, Fei; Yu, Guo-jun; Lin, Xiao-guo

doi:https://doi.org/10.1155/2015/837657

Advances in Materials Science and Engineering

On this page

Abstract Introduction Conclusion Acknowledgments References Copyright Related Articles

Research Article | Open Access

Volume 2015 | Article ID 837657 | https://doi.org/10.1155/2015/837657

Performance of Variable Negative Stiffness MRE Vibration Isolation System

Run-pu Li,¹Cheng-bin Du,¹Fei Guo,¹Guo-jun Yu,²and Xiao-guo Lin³

Academic Editor: Kaveh Edalati

Received04 Jul 2015

Revised14 Sept 2015

Accepted29 Sept 2015

Published21 Oct 2015

Abstract

Magnetorheological elastomer (MRE) vibration isolation devices can improve a system’s vibration response via adjustable stiffness and damping under different magnetic fields. Combined with negative stiffness design, these MRE devices can reduce a system’s stiffness and improve the vibration control effect significantly. This paper develops a variable negative stiffness MRE isolation device by combining an improved separable iron core with laminated MREs. The relationship between the negative stiffness and the performance of the device is obtained by mathematical transformation. Its vibration response under simple harmonic excitation at small amplitude and the impact of the volume fraction of soft magnetic particles on the isolation system are also analyzed. The results show that the negative stiffness produced by the magnetic force is a major factor affecting the capacity of the isolation system. Compared to devices of the same size, the isolation system equipped with low-particle volume fraction MREs demonstrates better performance.

1. Introduction

The isolation system has been widely used in high-precision measurement, automotive suspension, shipping shaft systems, and disaster prevention and reduction systems to reduce environmental disturbances [1–4]. Environmental disturbances mainly come from the ground vibrations transferred by the support system, such as post and purlin, in which increased structural flexibility by a small-stiffness isolation system is a main method for protecting engineering structures or equipment. However, environmental disturbances are also caused by a variable weight or position of the structure or equipment, under which a large-stiffness isolation system is required to improve the structural stability and thus minimize the disturbance of the engineering structure or equipment [5]. Inevitability, this indicates that different engineering structures may place different stiffness requirements on the isolation system. The adjustable range of the isolation system thereby serves as a critical performance index, and an isolation system with a large isolation range can be applied in a wide application area. Passive isolators are used most commonly in isolation because they are easily manufactured and cheaply equipped, but their limited frequency range and fixed stiffness have restricted their scope of application in the field. Fortunately, the stiffness of a system of two springs combined in series can be expressed as the ratio of their product to their sum. When a negative stiffness spring is connected in series with a positive one, the combined stiffness is infinite in theory. Therefore, the adjustment of the stiffness of each spring will directly affect the spring system’s combined stiffness and the isolation system’s bandwidth. Sarlis introduced a preloaded linear elastic spring into the passive isolation system and provided the damping system with negative stiffness by mounting an anchor frame and a movable frame [6]. Because the preloaded linear spring combination can provide negative stiffness by a certain connection method, Mochida et al. hinged three linear springs to form a combination that can be applied to foundation isolation, which provides negative stiffness [7]. Mizuno et al. used a voice coil motor as a linear actuator to generate a suspension system with negative stiffness and a pair of plate springs with normal stiffness and damping; the control strategy based on the Laplace transform was also introduced [8]. In the above literature, the system’s adjustable stiffness range is restricted by the fixed stiffness values of springs. This paper, using adjustable stiffness MREs as viscoelastic springs, devises a variable negative stiffness isolation unit and presents research conducted on the isolation performance.

Magnetorheological elastomers (MREs) are an intelligent composite material with actively controllable mechanical properties. The main ingredients of MREs are micron-sized soft magnetic particles and viscoelasticity polymer matrix. Micron-sized soft magnetic particles are dispersed directionally or distributed randomly in the polymer matrix curing without magnetic field or with that for higher material properties. The mechanical properties of MREs, such as damping feature, Young’s modulus, and shear modulus, may be transiently reversed under an external magnetic field. Being free of sedimentation and easily encapsulated, MREs are widely used in dampers, brakes, and deflection sensors [9–11]. Because conventional passive rubber isolators cannot change their mechanical properties, which results in problems pertaining to their lack of adaptability, many new options have been tested. A novel MRE seismic isolator with a laminated structure of steel and MRE layers was developed for real-time controllability of stiffness and damping [12], but the flexibility of this device is limited because the MR effect of MREs was increased only by the magnetic field. Yang et al. [13] assembled two permanent magnets into the MRE seismic isolator up and down. The main contribution mentioned above is the magnetic control. However, magnetic force is another method for the large range of excitation frequencies because wideband natural frequencies make the seismic isolator adaptable.

Based on the magnetic force between an electromagnet and a permanent magnet, Mizuno et al. probed into the negative stiffness effects on the active isolation system [5]. Kim et al. [14] investigated the isolation of a support system with a single degree of freedom by using an electromagnet connected in series with a linear spring. The result showed that an adjustable passive isolation system with negative stiffness has a large range for adjusting stiffness on the whole; thus, the limitation of conventional passive vibration isolation systems—that is, being inapplicable to broadband excitation—can be resolved. Because the electromagnetic force supplying an active force can provide the vibration isolation system with negative stiffness, Li et al. [15] developed a vibration control system with adjustable negative stiffness using the stiffness and damping of a common rubber. A combination of passive isolation and semiactive isolation is also a novel method wherein the MREs with controllable stiffness and damping serve as a semiactive control component [16]. MRE isolation units, by use of an electromagnet or permanent magnets, provided variable stiffness to give the isolation system a wideband variation range of stiffness, optimizing the isolation performance of the system. Incontestably, the focus of the isolation system is on the variation of stiffness and damping. Adding constant-stiffness rubber or springs is a conventional isolator strategy capable of mitigating the effects of one type of earthquake [12]. Further, the feasibility and practicality of laminated MRE isolators, similar to laminated rubber bearing structures, have been developed by specialists and scholars. The electromagnet was utilized for generating a magnetic field and controlling MRE stiffness in the literature [12, 13]. The concept of “negative changing stiffness” was first mentioned in the context of MRE isolator systems. In the literature, the stiffness of the MRE structure can be increased and decreased by adjusting a hybrid magnetic system such that the natural frequency of the system dodges the natural frequency [13]. In this study, however, an equivalent negative spring whose stiffness equals the ratio of an added magnetic force and displacement is joined to an equivalent normal spring whose stiffness is controlled by a hybrid magnetic system (two electromagnets) in series. The hybrid magnetic system not only changes the stiffness of MREs decreasingly and increasingly but also accommodates the added magnetic force for negative stiffness. Thus, the performance and the influence factor of this variable negative stiffness MRE vibration isolation system should be researched and confirmed in theory before the manufacturing process.

The mechanical properties of MREs are sensibly influenced by the particle volume fraction, such as storage Young’s modulus, storage shear modulus, loss factors [17], linear strain and the tensions induced in the MRE [18], and strain energy [19]. Because the added force is supplied by magnetic force and MREs, stiffness is directly related to the magnetic flux density inside MRE material. Thus, the effect of magnetic flux density and the volume fraction of MREs is researched and analyzed as the major influence factor. It is worth mentioning that setting a compact structure consisting of steel layers and laminated MREs inside the electromagnetic coil may increase the magnetic flux density; however, the air gap cannot be avoided because of the vertical displacement loaded by the mass or disturbance acting on the isolation that results in a decreased magnetic field inside the MRE material [12, 13]. This is also the reason why the iron core is separable.

In this study, the performance of variable negative stiffness MRE vibration isolation systems is analyzed in theory; further work will be given in next part. After the introduction, the structure and workflow are detailed and expatiated. Second, the Fourier transformation is used to deduce the impact of the magnetic force that produced the negative stiffness on the MRE isolation system’s performance. In Section 3, the impacts of particle volume fractions of MREs on the isolation system’s vibration characteristics are analyzed. Finally, the vibration characteristics of the isolation system under simple harmonic motion at a small amplitude are investigated.

2. System Sketch

The schematic diagram of the tunable negative stiffness MRE isolation device is depicted in Figure 1. The MRE isolation device mainly consists of isolated plates made of steel, laminated MREs, separable iron cores with telescopic strut/sleeve, and two electromagnets. The intermediate plate is connected with two cylindrical hollow laminated MRE blocks (upper and lower). Each laminated MRE block is composed of a circular iron plate and laminated MREs. The electromagnet, via a separable iron core, attracts the neighboring plate to produce a magnetic force that provides the system with negative stiffness as an actuator.

The alterable magnetic flux density can drive the two MRE layer blocks with variable stiffness ; also, there is a linear relation between the magnetic force generated by the magnetic fields and the displacement of the steel plate. When the displacement of the steel plate is small enough, the stiffness can be defined by the added magnetic force. The special frameworks of the MRE isolation system can be simplified into two springs in series, and the total stiffness of this MRE isolation system becomes a reciprocal value [8]:

The theoretical stiffness would be negative when the direction of relative displacement with respect to that of the added magnetic force is below zero. The initial equilibrium state is shown as in Figure 2(a); the distance between the isolated plate and the base plate is , equal to that of a shaking plate. A generalized force , which may be an increment of a force or a mass, is hypothetically applied to the isolated plate as shown in Figure 2(b), and the distance increases or decreases by . At the same time, the electromagnets generate an added magnetic force in a direction opposite to the hypothetically generalized force, and the absolute value is ; the stiffness is then for negative stiffness. The total stiffness of the system becomes extremely large if the absolute value of the stiffness is close to that of the negative stiffness ; thus, the isolation plate is safe from vibration. When the system is subjected to a generalized force, a displacement in the positive direction appears as shown in Figure 2(b); in the meantime, the added magnetic force makes the isolated plate move backward in the reverse or negative direction. The same state is then turned up on the isolation system as shown in Figure 2(c) if the absolute value of the stiffness is close to that of the negative stiffness because the above negative displacement and the forward displacement cancel each other out.

(a)

(b)

(c)

3. Magnetic Force

An equivalent physical model of variable negative stiffness MRE isolation systems is illustrated in Figure 3. The equivalent model consists of two masses modeled by the isolated plate, two parallel springs and parallel dashpots modeled by laminated MREs, and two parallel magnetic forces generated by the electromagnets applied to the plates. Considering kinetic equilibrium, the equation of the equivalent model can be written as follows:where and represent the masses of the upper and lower isolated plates, respectively, and are the mass displacements relative to the equilibrium position, and are the damping coefficients of the laminated MRE block, and are the stiffness values of the laminated MRE block, is the magnetic force applied to the plate, and is the inputted excitation load (Figure 3).

From (2) and (3), we obtain a Fourier transform representation:

It can be obtained as follows:

If the displacement of the intermediate plate of the damping target object decreases to null, then the control strategy is as follows:

From the equation mentioned above, the magnetic field force mainly falls into two parts: the first part is the displacement feedback part related to the equivalent resonant frequency and elastic force; the other is the velocity feedback part related to the damping force. The stiffness of the MREs is adjusted by changing the external magnetic field strength and setting . This is meant to make the isolator’s nondamping natural frequency equal to the external exciting frequency [20]. At this time, the system’s isolation efficiency can be expressed as a ratio of external exciting power to the power of the magnetic force applied to the plates. Considerwhere is the damping ratio and is the natural frequency.

The system’s isolation efficiency can be used to illustrate the capacity of the system’s energy dissipation. The system’s energy dissipation varies with damping ratio as shown in Figure 4. It can be seen from the diagram that the negative stiffness produced by the magnetic force contributes to the system’s energy dissipation as the frequency ratio increases, which satisfies the control strategy for minimal displacement of the intermediate plate in the damping target object mentioned above. The isolation system shows a lower overall stiffness under the negative stiffness effect resulting from the magnetic force; also, the negative stiffness generated by the magnetic force and positive stiffness resulting from the MRE deformation should be in harmony with each other in the spring system. Thus, the influences of magnetic force on the vibration isolation capacity should be analyzed further. Many factors can affect the magnitude of the magnetic force in this system, such as current intensity, number of windings, gap size, and material permeability. In this part, the magnetic field strength is selected as the independent variable on vibration isolation capacity because the magnetic field strength can be changed by the above elements.

Now suppose that an external excitation acts upon the above plate , and the magnetic force applied to the intermediate plate of the damping target object is . The following power balance equation for the intermediate plate is then obtained from (3):

Under an external magnetic field with average magnetic flux density , the magnetic energy between the positive and negative displacements of the intermediate plate during vibration is , and the magnetic force can be expressed as the magnetic energy’s differential in the direction of the plate displacement . Considerwhere , , , , , and are vacuum magnetic conductibility, MRE cross section area, number of turns in the coil, current in the coil, leakage coefficient of the coil, and original distance between the surrounding plates, respectively. The magnetic forces can then be expressed as follows:

If the displacements are small, the magnetic forces can be seen as linear functions of the relative displacement, and the resulting negative stiffness can be expressed as

Assuming that the stiffness values of the intermediate plate’s upper and lower support systems are equal, . The isolation system’s equivalent magnetic force can then be expressed aswhere and are stiffness values of the upper and lower support systems, respectively—namely, the stiffness values of MREs, each of which is a function of the external magnetic fields and . is the equivalent stiffness.

Equation (8) can be simplified aswhere points to the equivalent viscous damping coefficient. If the displacement of the upper plate is the sine exciting displacement (), thenwhere the phase angle is ; thus, the transmissibility of the isolation system is

Chen et al. [21] proposed a kind of MRE-based natural rubber. The test results indicated that the mechanical properties of prestructured natural rubber-based MREs, such as absolute modulus and relative modulus, are relatively good. In this paper, the impact of the external magnetic field with respect to the system isolation transmissibility is studied assuming that the MREs are equipped within. The relation between the system’s transmissibility and dimensionless frequency ratio is shown in Figure 5. It is shown that the damping characteristics correlated to peak transfer rate are affected by magnetic flux density, and the natural frequency is negatively correlated with the external magnetic field. As the external magnetic field increases, the value of the transmissibility decreases, which can be explained by the fact that the system stiffness is reduced by the negative stiffness produced by the magnetic force. The transmissibility of the isolation system with negative stiffness unconsidered is shown in Figure 6 for comparison. Contrary to the case given in Figure 5, the smaller relative change in peak frequency is observed with the increased magnetic flux density in this nonnegative stiffness case, and the damping related to the peak transmissibility is dependent on the magnetic flux density as seen in the literature [16]. The most likely reason for the similar tendency of transmissibility is that the system considered here can be reduced as MRE isolators when the negative effects mentioned above are ignored. When the prestructured magnetic field strength is 600 mT and the external magnetic field strength is 0.4 mT, the soft magnetic particles of the MREs would reach magnetic saturation [21]. This is also one of the reasons why the variation of the phase angle is minimized by further increasing the magnetic flux density in Figure 7. As seen from (12), the negative stiffness of the system is a function of magnetic field, which dominates the mechanical properties of MREs introduced into the isolation system for a viscoelasticity component. Thus, it is necessary to discuss the impact of soft magnetic particles in MREs on the isolation performance.

4. The Particle Volume Fraction of MREs

MREs prepared with a magnetic field character have a higher equivalent damping coefficient and energy dissipation than those prepared without a magnetic field [22], so the MREs prepared with a magnetic field in the isolation system should be chosen as viscoelastic components in the isolation system. When the magnetic particle chains in MREs are perpendicular to the plane of plates, Young’s modulus of MREs is correlated with the soft magnetic particles in MREs [23]. Considerwhere is the number of magnetic particles per unit of MREs, denotes the center distance of adjacent particles in a particle chain, and is the magnetic dipole moment [24]:where is the magnetic conductivity of MREs, is the susceptibility of soft magnetic particles, and are the average radius and volume of the soft magnetic particles, respectively, is the external magnetic intensity, and is the mathematical constant.

The magnetic dipole moment can be expressed as in the first-order expression. Because the volume fraction of MREs can directly affect the susceptibility of soft magnetic particles, the mechanical properties of MREs under the external magnetic field, such as damping controllability and shear modulus, vary greatly with different volume fractions [11, 25, 26]. Assuming that the MRE particle chain is a straight chain [27], the volume fraction can be expressed as the ratio of the particle volume to the sum of the particle volume and the surrounding matrix as well as the ratio of the total volume of the particles to that of MREs:

MRE stiffness can be expressed as a ratio of the product of its modulus and cross section area to unit thickness. According to the equations mentioned above, the stiffness of MREs can be obtained as follows:

Here, the magnetic flux leakage is neglected; from (12) and (20), the natural frequency of the isolation system is a function of the MRE volume fraction. Consider

The impact of MRE particle volume fraction on the transmissibility is obtained from (12) and (18). Figure 8 indicates that transmissibility varies with frequency. The dimensions of the system are as follows: the damping ratio is 0.05, the MRE cross section area is 31,400 mm², and the maximum displacement is 4 mm. It can be seen from the figure that an increased particle volume fraction results in an increased peak frequency; for isolation systems with identical size, the volume fractions had a remarkable influence on their natural frequencies. This can be explained because the particle volume fraction can affect the stiffness and modulus of MREs, and the system’s negative stiffness can lead to softened overall stiffness.

According to (21), the system’s natural frequency was negatively correlated to the MRE volume fraction. This is because the MREs show a more significant magnetorheological effect and magnetic anisotropy with a larger volume fraction. Such a phenomenon is more obvious if the external magnetic field is parallel to MRE particle chains [28, 29]. When the external magnetic field is comparatively larger and the induced field of soft magnetic particles reaches saturation, the maximum magnetic dipole moment of the soft magnetic particles could be approximately taken as 2.1 V [30]. At this time, the equivalent stiffness of the isolation system can be expressed as . If the magnetic flux leakage is neglected, the isolation system’s natural frequency is a function of MRE volume function. Consider

5. Conclusion

This paper proposed an isolation system for MREs with negative stiffness whose separable iron core is replaced by a conventional cylindrical core, which provides negative stiffness for the conventional laminated MRE isolation core. To verify the effectiveness of the negative stiffness and the laminated MRE, the transmissibility with and without negative stiffness and that with different particle volume fractions were discussed; the following conclusions can be obtained:(i)The frequency and the system transmissibility decrease as the magnetic strength increases and there is lower transmissibility without negative stiffness.(ii)The vibration isolation performance of the one equipped with MREs with a low volume fraction is better than the one with high particle fraction.(iii)The negative stiffness effect produced by the magnetic force is conducive to the energy dissipation for the isolation system.

Conflict of Interests

The authors declare that there is no conflict of interests regarding the publication of this paper.

Acknowledgments

This study was supported by the Jiangsu Province Science and Technology Support Program, China (Grant no. BE2012180), National Natural Science Foundation of China (Grant no. 51508237), Natural Science Foundation of Jiangsu Province (BK20140560), and Natural Science Foundation of Zhejiang Province (Y15E080043).

References

H. Yoshioka, Y. Takahashi, K. Katayama, T. Imazawa, and N. Murai, “An active microvibration isolation system for hi-tech manufacturing facilities,” Journal of Vibration and Acoustics, Transactions of the ASME, vol. 123, no. 2, pp. 269–275, 2001.
View at: Publisher Site | Google Scholar
X. M. Dong, M. Yu, Z. Li, C. Liao, and W. Chen, “Neural network compensation of semi-active control for magneto-rheological suspension with time delay uncertainty,” Smart Materials and Structures, vol. 18, no. 1, Article ID 015014, 2009.
View at: Publisher Site | Google Scholar
Z. Yang, C. Qin, Z. Rao, N. Ta, and X. Gong, “Design and analyses of axial semi-active dynamic vibration absorbers based on magnetorheological elastomers,” Journal of Intelligent Material Systems and Structures, vol. 25, no. 17, pp. 2199–2207, 2014.
View at: Publisher Site | Google Scholar
S. Nagarajaiah and S. Sahasrabudhe, “Seismic response control of smart sliding isolated buildings using variable stiffness systems: an experimental and numerical study,” Earthquake Engineering and Structural Dynamics, vol. 35, no. 2, pp. 177–197, 2006.
View at: Publisher Site | Google Scholar
T. Mizuno, M. Takasaki, D. Kishita, and K. Hirakawa, “Vibration isolation system combining zero-power magnetic suspension with springs,” Control Engineering Practice, vol. 15, no. 2, pp. 187–196, 2007.
View at: Publisher Site | Google Scholar
A. A. Sarlis and M. C. Constantinou, “Negative stiffness device and method,” US Patent 20150000217, 2014.
View at: Google Scholar
Y. Mochida, N. Kida, and S. Ilanko, “Base isolator of vertical seismic vibration using a negative stiffness mechanism,” in Vibration Engineering and Technology of Machinery, vol. 23 of Mechanisms and Machine Science, pp. 1113–1119, Springer, 2015.
View at: Publisher Site | Google Scholar
T. Mizuno, T. Toumiya, and M. Takasaki, “Vibration isolation system using negative stiffness,” JSME International Journal, Series C: Mechanical Systems, Machine Elements and Manufacturing, vol. 46, no. 3, pp. 807–812, 2003.
View at: Publisher Site | Google Scholar
L. E. Faidley, Y. Han, K. Tucker, S. Timmons, and W. Hong, “Axial strain of ferrogels under cyclic magnetic fields,” Smart Materials and Structures, vol. 19, no. 7, Article ID 075001, 2010.
View at: Publisher Site | Google Scholar
S. Monz, A. Tschöpe, and R. Birringer, “Magnetic properties of isotropic and anisotropic CoFe₂O₄-based ferrogels and their application as torsional and rotational actuators,” Physical Review E: Statistical, Nonlinear, and Soft Matter Physics, vol. 78, no. 2, Article ID 021404, 2008.
View at: Publisher Site | Google Scholar
R. L. Snyder, V. Q. Nguyen, and R. V. Ramanujan, “Design parameters for magneto-elastic soft actuators,” Smart Materials and Structures, vol. 19, no. 5, Article ID 055017, 2010.
View at: Publisher Site | Google Scholar
Y. Li, J. Li, W. Li, and B. Samali, “Development and characterization of a magnetorheological elastomer based adaptive seismic isolator,” Smart Materials and Structures, vol. 22, no. 3, Article ID 035005, 2013.
View at: Publisher Site | Google Scholar
J. Yang, S. S. Sun, H. Du, W. H. Li, G. Alici, and H. X. Deng, “A novel magnetorheological elastomer isolator with negative changing stiffness for vibration reduction,” Smart Materials and Structures, vol. 23, no. 10, Article ID 105023, 2014.
View at: Publisher Site | Google Scholar
Y.-B. Kim, W.-G. Hwang, C.-D. Kee, and H.-B. Yi, “Active vibration control of a suspension system using an electromagnetic damper,” Proceedings of the Institution of Mechanical Engineers Part D: Journal of Automobile Engineering, vol. 215, no. 8, pp. 865–873, 2001.
View at: Publisher Site | Google Scholar
Z. Li, X. Wang, M. Behrooz, N. Maus, and F. Gordaninejad, “A tunable ‘negative’ stiffness system for vibration control,” in Active and Passive Smart Structures and Integrated Systems, vol. 8341 of Proceedings of SPIE, International Society for Optics and Photonics, March 2012.
View at: Publisher Site | Google Scholar
M. Behrooz, X. Wang, and F. Gordaninejad, “Modeling of a new semi-active/passive magnetorheological elastomer isolator,” Smart Materials and Structures, vol. 23, no. 4, Article ID 045013, 2014.
View at: Publisher Site | Google Scholar
R. Li and L. Z. Sun, “Viscoelastic responses of silicone-rubber-based magnetorheological elastomers under compressive and shear loadings,” Journal of Engineering Materials and Technology, Transactions of the ASME, vol. 135, no. 2, Article ID 021008, 2013.
View at: Publisher Site | Google Scholar
I. Bica, “The influence of the magnetic field on the elastic properties of anisotropic magnetorheological elastomers,” Journal of Industrial and Engineering Chemistry, vol. 18, no. 5, pp. 1666–1669, 2012.
View at: Publisher Site | Google Scholar
T. L. Sun, X. L. Gong, W. Q. Jiang, J. F. Li, Z. B. Xu, and W. H. Li, “Study on the damping properties of magnetorheological elastomers based on cis-polybutadiene rubber,” Polymer Testing, vol. 27, no. 4, pp. 520–526, 2008.
View at: Publisher Site | Google Scholar
G. J. Liao, X.-L. Gong, S. H. Xuan, C. J. Kang, and L. H. Zong, “Development of a real-time tunable stiffness and damping vibration isolator based on magnetorheological elastomer,” Journal of Intelligent Material Systems and Structures, vol. 23, no. 1, pp. 25–33, 2012.
View at: Publisher Site | Google Scholar
L. Chen, X. Gong, and Q. Kong, “Preparation and characterization of magnetorheological elastomers based on natural rubber,” Journal of Experimental Mechanics, vol. 22, no. 3, pp. 372–378, 2007.
View at: Google Scholar
X. Zhang, S. Peng, W. Wen, and W. Li, “Analysis and fabrication of patterned magnetorheological elastomers,” Smart Materials and Structures, vol. 17, no. 4, Article ID 045001, 2008.
View at: Publisher Site | Google Scholar
Y. Han, W. Hong, and L. E. Faidley, “Field-stiffening effect of magneto-rheological elastomers,” International Journal of Solids and Structures, vol. 50, no. 14-15, pp. 2281–2288, 2013.
View at: Publisher Site | Google Scholar
Y. Shen, M. F. Golnaraghi, and G. R. Heppler, “Experimental research and modeling of magnetorheological elastomers,” Journal of Intelligent Material Systems and Structures, vol. 15, no. 1, pp. 27–35, 2004.
View at: Publisher Site | Google Scholar
F. Guo, C.-B. Du, and R.-P. Li, “Viscoelastic parameter model of magnetorheological elastomers based on abel dashpot,” Advances in Mechanical Engineering, vol. 2014, Article ID 629386, 12 pages, 2014.
View at: Publisher Site | Google Scholar
L. C. Davis, “Model of magnetorheological elastomers,” Journal of Applied Physics, vol. 85, no. 6, pp. 3348–3351, 1999.
View at: Publisher Site | Google Scholar
M. R. Jolly, J. D. Carlson, and B. C. Muñoz, “A model of the behaviour of magnetorheological materials,” Smart Materials and Structures, vol. 5, no. 5, pp. 607–614, 1996.
View at: Publisher Site | Google Scholar
G. Binasch, P. Grünberg, F. Saurenbach, and W. Zinn, “Enhanced magnetoresistance in layered magnetic structures with antiferromagnetic interlayer exchange,” Physical Review B, vol. 39, no. 7, article 4828, 1989.
View at: Publisher Site | Google Scholar
G. Schubert, P. Harrison, and Z. Guo, “Characterisation of the magneto-rheological effect of silicone rubber-iron particle composites under large strain,” in Proceedings of the 8th European Solid Mechanics Conference (ESMC '12), Graz, Austria, July 2012.
View at: Google Scholar
J. M. Ginder, M. E. Nichols, and L. D. Elie, “Controllable-stiffness components based on magnetorheological elastomers,” in Smart Structures and Materials 2000: Smart Structures and Integrated Systems, Proceedings of the SPIE, pp. 418–425, The International Society for Optical Engineering, June 2000.
View at: Publisher Site | Google Scholar

Copyright

Copyright © 2015 Run-pu Li et al. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

PDF Download Citation

Download other formats

Order printed copies

Views

1448

Downloads

1117

Citations