Abstract
An active vibration control experiment of planar 3-RRR flexible parallel robots is implemented in this paper. Considering the direct and inverse piezoelectric effect of PZT material, a general motion equation is established. A strain rate feedback controller is designed based on the established general motion equation. Four control schemes are designed in this experiment: three passive flexible links are controlled at the same time, only passive flexible link 1 is controlled, only passive flexible link 2 is controlled, and only passive flexible link 3 is controlled. The experimental results show that only one flexible link controlled scheme suppresses elastic vibration and cannot suppress the elastic vibration of the other flexible links, whereas when three passive flexible links are controlled at the same time, they are able to effectively suppress the elastic vibration of all of the flexible links. In general, the experiment verifies that a strain rate feedback controller is able to effectively suppress the elastic vibration of the flexible links of plane 3-RRR flexible parallel robots.
1. Introduction
Recently, flexible parallel robots have been intensively studied because of their excellent performance. However, the elastic vibration problem of such robots is serious due to their inertial and driving forces. As a result, suppressing the unwanted elastic vibration is currently a very significant and challenging problem.
There are basically five design philosophies for suppressing unwanted elastic vibration that are classified into passive vibration control and active vibration control [1]. Passive vibration control means that unwanted vibration is suppressed by using advanced composite materials, optimizing the cross-sectional geometry of the elements, or using additional damping materials. Active vibration control means that unwanted vibration is suppressed by introducing a microprocessor-controlled actuator into the original mechanism or embedding some smart structures (actuators and sensors) into flexible elements. The surface-bonded lead zirconate titanate (PZT) sensor/actuator has been widely used for active vibration control of the flexible structure [2, 3]. PZT materials are able to dampen vibration and measure the vibration of distributed parameter systems because of their direct and inverse piezoelectric effect [4]. Photostrictive actuator as a new promising noncontact photoactuation technique was used for suppressing vibration of flexible structures [5].
During the past few decades, the question of active vibration control of flexible robots has been paid considerable attention, as indicated in survey papers [6–9]. Although there are many theoretical and experimental studies of active vibration control in space-based flexible structures and simple flexible beams [10–13], PZT materials are introduced into the vibration control of manipulators or mechanisms that only have a single link with a single actuator and sensor bonded [14, 15]. Meanwhile, compared with numerical simulation, the experimental study of the active vibration control of flexible manipulators is a more challenging work, especially for flexible parallel robots. Zhang et al. [16] have performed an experimental study of active vibration control of 3-PRR flexible parallel robots, for which the elastic vibration of flexible links during motion is suppressed by an SRF controller. The KED assumption is utilized. Zhang et al. [17] address the dynamic modeling and efficient modal control of a planar parallel manipulator (PPM) with three flexible linkages actuated by linear ultrasonic motors (LUSM). We performed studied dynamic modeling and dynamic analysis of planar 3-RRR flexible parallel robots [18–21].
The residual vibrations of the flexible links of planar 3-RRR flexible parallel robots are studied in this paper. In fact, the amplitudes of the residual vibration are greater than the elastic vibration during the motion and will be verified in the experimental study of this paper, and these residual vibrations influence the repeat positioning accuracy of the system seriously. Thus, it is important to suppress the residual vibration of flexible links to improve the repeat positioning accuracy of the system. Essentially, the dynamic responses measured by PZT sensors include unmodeled or unknown dynamics. Therefore, the vibrations of the flexible elements are very complicated and contain many frequency components that are closely spaced. To measure the modal coordinates or velocities more precisely, it is desirable to use as many PZT sensors as possible. However, the number of PZT sensors is limited by the available space of the flexible links and the real-time computing power of the computer. A trade-off must be made between the real-time computing power of the computer hardware and the number of sensors [22].
To solve the above problems, an experimental study of the active vibration control of planar 3-RRR parallel robots with three flexible links, each of which bonds with two pairs of PZT actuators and one PZT sensor film, is implemented in this paper. The moving platform of the planar parallel robots moves along a given trajectory, control experiments are implemented in real-time, and the controller is activated when rigid motion stops. The active control system consists of an industrial computer, a dSPACE controller with many I/O ports, smart flexible links with PZT actuators and PZT sensors, and a PZT driven power and charge amplifier. A strain rate feedback control algorithm is adopted to suppress the elastic vibration of the flexible links of the system [20].
The remainder of the paper is organized as follows. The rigid-elastic coupling dynamic model is established in Section 2. According to the direct and inverse piezoelectric equation of the PZT material, a strain rate feedback control algorithm is given. Section 3 introduces an experimental system setup and describes the working principle of the controller system and each component. In Section 4, the results of an experiment of vibration control are presented. Four experiment schemes are designed. The control performance of the four experiment schemes is analyzed; the experimental results verify the validity of the strain rate feedback controller for suppressing the residual vibration of flexible links. Finally, the conclusions are given in Section 5.
2. Dynamic Model of Planar 3-RRR Flexible Parallel Robots
2.1. Sketch of Planar 3-RR Parallel Robots
A sketch of the planar flexible 3-RRR parallel robots is constructed by the regular triangle moving platform , the static platform, and three symmetrical kinematic chains, , , and , as shown in Figure 2. Each kinematic chain has one active revolute (R) joint, followed by two consecutive passive revolute (R) joints. The active revolute joints are installed at , . , , and are the regular triangle’s three vertices. and . The vertices and are centers of the regular triangles and , respectively. O-XY is the global fixed frame. The parameters and are the angles between the -axis of the fixed frame and linkages and , respectively. is the angle between the -axis of the fixed frame and side of the regular triangle . , , , and are the lengths of the segments , , , and .
2.2. Motion Equations of the Beam Element
The flexible link can be modeled by connecting a series of beam elements. Figure 2 shows a beam element before and after deformation. O-XY is the global fixed frame, and the A-xy is the local moving frame, with the -axis coincident with the neutral line of the beam element. The original point is located at one node of the beam element before deformation. B is another node of the beam element. The - system is an intermediate coordinate frame, the origin of which is rigidly attached to the origin of the O-XY and the axes of which are parallel to the axes of the local moving frame A-xy. is the angle between the global fixed frame O-XY and the intermediate coordinate frame -.
Considering the general point in the element, let point be the corresponding point on the neutral line. Points and are their respective positions after deformation. The elastic deformation of the point in - is given by where is the nodal displacement vector, in which and are the axial displacements of two nodes A and B, respectively; and are the lateral displacements; and are the elastic rotational angles; and are the section curvatures; and is the shape function matrix. Assuming that the axial displacement of point is a linear function, the lateral displacement is a fifth-order hermit function, yieldingwhere
The deformation displacements of in A-xy can be written as [23]
Let . Then, the displacement of can be expressed in the global fixed frame bywhere is the direction cosine matrix, that is, the - system with respect to the - system, and is given by , where the vector is the location coordinates of the point in the - system and is given by , where the superscript T indicates the matrix transpose and the coupling quantity is the axial displacement caused by the transverse displacement of beam. The parameter can be obtained by taking the first derivative onwhere .
Equation (6) can be expressed compactly aswhere .
2.2.1. Kinetic Energy of the Beam Element
The kinetic energy of the beam element is mainly composed of translational energy and rotational energy. According to (7), the kinetic energy of the beam element is written as where is the material density, is the volume of the beam element, is the absolute rotation angle of small block in the global fixed frame -, is the moment of inertia about the center of mass of the beam element, and are the lumped masses of at the ends of the beam element, and are the lumped moment of inertia at the ends of beam element, and and are the absolute rotation angle of the two ends of the beam element in the global fixed frame -., , , , , , , , , , , , is a skew symmetric matrix defined as is the section moment of inertia of the beam element, and is the two-order unit matrix.
2.2.2. Strain Energy of the Beam Element
Nonlinear terms in the strain-displacement relationship are neglected [24]. Thus, the strain energy of the beam element can be written aswhere , , and is the elastic modulus of materials. and are the cross-sectional moment of inertia and the cross-sectional area of the beam element, respectively.
2.2.3. Motion Equations of the Beam Element
According to Lagrange’s equation, the dynamic equation of the beam element can be derived aswhere and are the generalized external forces and the quadratic velocity vector that contains the gyroscopic and the Coriolis force components, respectively.
The elemental dynamic equation has been established in the A-xy system. Before forming the dynamic equation of the system, (13) must be expressed in the O-XY system. Defining the coordinate transformation matrix Letwhere is the elemental nodal coordinate vector in the O-XY system. By taking the first and the second derivatives of (16) with respect to time,where and . Substituting (16) and (17) into (13) and premultiplying by matrix , the dynamic equation of the beam element can be expressed in the O- system bywhere and and are the element generalized mass and the stiffness matrices in the O-XY system, respectively. is the quadratic velocity vector in the O-XY system. is the generalized external forces vector in the O-XY system.
2.3. Constraint Equations
Different from the simple structure, the constraint relationships of the planar 3-RRR of flexible parallel robots, which include the rigid-body motion constraints, elastic deformation motion constraints, and dynamic constraints of the moving platform, are very complex and can be used to eliminate the correlation of the generalized coordinates.
2.3.1. Constraint Equations of the Rigid-Body Motion
The generalized coordinates are formed by rigid-body motion coordinates and elastic coordinates. As shown in Figure 1, the rigid-body motion coordinates include drive joint rotation angles , passive joint rotation angles , and translation displacement and rotation angle of the moving platform , and rigid-body motion coordinate vectors , , and are not independent. Because three kinematic chains of 3-RRR parallel robots are full symmetrical chains, only one chain is studied. As shown in Figure 3, a closed-loop vector equation can be established:Projecting (19) into and components yieldswhere and are the coordinates of the points and in the O-XY system, respectively.
2.3.2. Constraint Equations of the Elastic Deformation Motion
As shown in Figure 3, center point and vertex of the moving platform are moved to points and because of the elastic deformation motion of the flexible links and . P-xy is the local coordinate system with original point , and - is the elastic coordinate system with original point , , and are the coordinate transformation matrices for --, --, and --, respectively. Thus, . , , and are the elastic displacements and elastic rotational angle at the end point of the flexile link ; the section curvature is equal to zero at point . and , are the translational and rotational declinations of the moving platform because of the elastic vibration of the flexible links. Assuming that the moving platform is rigid, . Note that
Assuming that and are the coordinates of the points , in the O-XY system yieldswhere . denotes the description in p-xy.
Setting yieldswhere is the unit matrix.
2.3.3. Dynamic Constraints of the Moving Platform
Assuming that is the generalized joint constraint reaction force that the passive joint exerts on the moving platform, and are the mass and moment of inertia of the moving platform, respectively. Thus, the dynamic constraint of the moving platform can be expressed by
2.4. Motion Equations of Planar 3-RR Parallel Robots
Considering the above constraint (20)–(24), let be the generalized elastic coordinate vector of all of the flexible links and the moving platform in the - system; namely, . By assembling all of the elements in (18), according to the compatibility at the nodes, the equations of motion of the planar 3-RRR parallel robots are given aswhere , , and are the generalized mass, damping, and stiffness matrices, respectively; includes the gyroscopic force, the Coriolis force components, and the generalized external force.
3. Strain Rate Feedback Control Algorithm
Due to the direct and inverse piezoelectric effect of PZT material, PZT material is widely used for designing active vibration controllers of flexible multibody systems. Assuming that the PZT sensor film is perfectly bonded onto the flexible beam, as shown in Figure 4, the direct piezoelectric equation of PZT sensor can be expressed as [22]where , is Young’s modulus of the piezoelectric sensor, is the piezoelectric constant, is the width of the piezoelectric sensor, is the length of the piezoelectric sensor, is the capacitance of the piezoelectric sensor, is the length of the beam element, is the direct coordinates of the midpoint of the th sensor in the element coordinate frame, is the column vector of the 2nd line of , and denotes the second derivative to the variable .
As shown in Figure 5, two of the same PZT actuators are perfectly bonded onto the upper and lower surfaces of the beam element in the same position and the polarization directions of the two PZT actuators are also the same. Two adhesive surfaces are electrically grounded, and the other two surfaces are linked into input voltage by wire. According to inverse piezoelectric effect of the PZT material, the torque of the two ends of the PZT actuator pair is given by [25]where , , is the direct coordinate of the left end of the th PZT actuator, and is the direct coordinate of the right end of the th PZT actuator. is Young’s modulus of the PZT actuator, is the width of the PZT actuator, is the thickness of the PZT actuator, and is the thickness of the beam element.
Assuming there are PZT actuator pairs and PZT sensor films in this system, integrating all of the inverse piezoelectric equations of the PZT actuator pairs and elastodynamics yieldswhere is the input matrix; is the dimension input vector.
Assembling all of the direct piezoelectric equations of the PZT sensor films yieldswhere is the dimension output vector and is the output matrix.
According to (28) and (29), the general motion equation of the system can be expressed as
In this paper, the goal is to suppress the residual vibration of flexible links of planar 3-RRR flexible parallel robots so that the moving platform can accurately stop at a given position. Thus, the mass matrix is a positive definite symmetric constant matrix, the stiffness matrix is a symmetric constant matrix, and is a zero vector, assuming that the damping matrix barely includes structural damping. Considering that residual vibration of the system is decided by its lower-order modes, the real modal method is utilized for extracted lower-order modes of the controlled system. Assuming that the first lower-order modes are suppressed, the general motion equation of the system can be simplified aswhere is the first lower-order mode coordinates.
The strain rate feedback control is adopted to suppress the residual vibration of the flexible links. Here the derivation of output voltage of the sensor is fed back to the corresponding actuators pairs, yieldingwhere is feedback gain matrix.
Assuming ) is the damping ratio coefficients of the th mode coordinates, then the motion equation of the controlled system can be expressed as
Assuming that the damping ratio coefficient is accelerated to , the feedback gain matrix can be expressed aswhere and are the generalized inverse matrices of and , respectively.
According to (34), the strain rate feedback control leads to the increase of the damping of the system.
4. Experimental System Setup
The experimental setup of the active vibration control system, as shown in Figure 6, consists of a planar 3-RRR flexible parallel mechanism, a static platform, three Yaskawa servomotors, and SHIMPO reducers (reduction ratio is 1 : 5). The three passive links are all flexible and identical with dimensions of . The three active links are all rigid and identical with dimensions of . The links are insulated by surface oxidation. The static platform of the planar 3-RRR flexible parallel robots consists of a marble pedestal, a steel-framed structure, and a rectangular steel plate. The experimental setup also includes PZT actuators and PZT sensors, PZT drive power, a charge amplifier, a real-time semiphysical simulation system, dSPACE, and an industrial computer. The dimensions of each PZT actuator are , and the dimensions of each PZT sensor are . The piezoelectric constant of the piezoelectric actuator/sensor is c/N, and Young’s modulus of the piezoelectric actuator/sensor is MP. The smart beam shown in Figure 7 has two pairs of PZT actuators symmetrically bonded on the surface of the flexible beam and one PZT sensor is bonded on its middle.
The PZT drive power is manufactured by Harbin Core Tomorrow Science and Technology Co., Ltd., its main module is a 090716 amplifier, its analog input is V, its analog output voltage is V, its power is W, its average current is mA, and its working temperature range is . The PZT drive power is shown in Figure 8.
Figure 9 shows the YE5850 charge amplifier, which is manufactured by Jiangsu Lianneng Electronic Technology Co., Ltd. The amplifier is a bandwidth charge amplifier whose input voltage is proportional to its output voltage. Because the lower-cut-off frequency of the amplifier is very small, it is suitable for quasistatic calibration of piezoelectric pressure transducer. The maximum input charge and maximum output voltage of the amplifier are PC and V, respectively.
dSPACE (real-time semiphysical simulation system) is a control system development platform and test platform based on MATLAB/Simulink. dPACE can achieve a seamless connection with MATLAB/Simulink. dSPACE owns a hardware system that has a high-speed computing capability and friendly software environment for code generating, downloading, and debugging.
The DS1103PPC control card (see Figure 10) and DS2211 HIL I/O panel (see Figure 11) are used in the experiment. The DS1103PPC control card is the most powerful card to date and has abundant I/O ports. Figure 12 shows an industrial computer that is manufactured by YANHUA company. DS1103PPC control card is installed in the expansion slot of the industrial computer.
5. Experimental Results and Analysis
Assume that the motion trajectory of the moving platform of the system is designed as follows.
First Step. The midpoint of the moving platform moves to the coordinate from the origin of the fixed coordinate system along the linear trajectory of (35); the process takes 1 second.
Second Step. Move 0.3 seconds along the circular trajectory of (36), and then stop for 2.7 seconds.
Third Step. The second step is repeated 5 times.
Fourth Step. The moving platform returns to the initial position along the linear trajectory of (37).
The entire motion period takes 17 seconds.
The PZT sensor films are bonded onto passive flexible links, as shown in Figure 7; the vibration signal of one PZT sensor film is fed back to two pairs of PZT actuators. Thus, there are three PZT sensors and six pairs of PZT actuators in the whole system. Because the dSPACE controller has a time-lag for collecting data, the last 14 seconds of a motion period is chosen as the data collection time. The sampling frequency is set at 10000 Hz in the MATLAB/Simulation; thus, each sensor collects 140,000 data points.
Figures 13(a), 13(b), and 13(c) are the PSD (Power Spectrum Density) values of the uncontrolled vibration signal of sensors 1, 2, and 3, respectively. As shown in Figure 13, the first-order mode frequency of the system is 12.5 Hz; 40 Hz and 67.5 Hz are the second-order and third-order mode frequencies, respectively. The PSD values reflect the energy level of the vibration signal under different mode frequencies. The PSD value of the first-order mode is larger than that of the second-order and third-order mode frequencies; thus, the PSD value of first-order mode frequency can reflect suppression effect of the vibration signal. Modal analysis was implemented for 3-RRR planar parallel robots in [21] based on the modal analysis module of Ansys-Workbench software. The results indicate that the first three-order modes can completely reflect the dynamic characteristics of the system.
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Four control schemes are designed in this experiment. Scheme 1 involves three passive flexible links which are controlled at the same time; scheme 2 involves only passive flexible link 1 which is controlled; scheme 3 involves only passive flexible link 2 which is controlled; scheme 4 involves only passive flexible link 3 which is controlled.
Figures 14(a), 14(b), and 14(c) are the PSD value of the vibration signal of sensors 1, 2, and 3 with three passive flexible links being controlled at the same time, respectively. Figures 15(a), 15(b), and 15(c) are the PSD value of the vibration signal of sensors 1, 2, and 3 with only passive flexible link 1 being controlled, respectively; Figures 16(a), 16(b), and 16(c) are PSD the value of vibration signal of sensors 1, 2, and 3 with only passive flexible link 2 being controlled, respectively. Figures 17(a), 17(b), and 17(c) are the PSD value of vibration signal of sensors 1, 2, and 3 with only passive flexible link 3 being controlled, respectively.
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Table 1 shows the PSD value of three uncontrolled sensors with the above four control schemes regarding the first-order mode frequency. Without control, the three PSD values are 29.58 dB, 20.67 dB, and 17.92 dB. In scheme 1, the three PSD values are 27.37 dB, 14.61 dB, and 10.34 dB; compared with the uncontrolled case, three PSD values descend by 7.47%, 29.32%, and 42.3%, respectively. In scheme 2, the three PSD values are 27.08 dB, 20.65 dB, and 17.83 dB; compared with the uncontrolled case, the three PSD values descend by 8.45%, 0.1%, and 0.5%. In scheme 3, three PSD values are 29.6 dB, 14.14 dB, and 17.89 dB, respectively; compared with the uncontrolled case, PSD1 increases by 0.06%, PSD2 decreases by 31.59%, and PSD3 decreases by 0.17%. In scheme 4, the three PSD values are 29.6 dB, 14.14 dB, and 17.89 dB; compared with the uncontrolled case, the three PSD values descend by 0.47%, 2.03%, and 43.3%, respectively.
We can draw the following conclusions from Figures 13–17 and Table 1:(1)Each separate controlled flexible link only suppresses its elastic vibration and cannot suppress the elastic vibration of other flexible links.(2)The case in which three passive flexible links are controlled at the same time can effectively suppress elastic vibration of all flexible links.(3)Because coupling between flexible links exists, the control performance of three passive flexible links being controlled at the same time is worse than that of the corresponding separate controlled flexible link.
Figures 18(a), 18(b), 18(c), 18(d), and 18(e) are the vibration signals of passive flexible link 1 for the uncontrolled, scheme 1, scheme 2, scheme 3, and scheme 4, respectively. As shown in Figure 18, the elastic vibration of the passive flexible link 1 is suppressed in scheme 1 and scheme 2 (see Figures 18(b) and 18(c)), and the other schemes cannot effectively suppress the elastic vibration of passive flexible link 1 (see Figures 18(d) and 18(e)).
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Figures 19(a), 19(b), 19(c), 19(d), and 19(e) are the vibration signals of passive flexible link 2 for the uncontrolled, scheme 1, scheme 2, scheme 3, and scheme 4, respectively. As shown in Figure 19, the elastic vibration of the passive flexible link 2 is suppressed in scheme 1 and scheme 3 (see Figures 19(b) and 19(d)), and the other schemes cannot effectively suppress the elastic vibration of passive flexible link 2 (see Figures 19(c) and 19(e)).
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Figures 20(a), 20(b), 20(c), 20(d), and 20(e) are the vibration signals of passive flexible link 3 for the uncontrolled, scheme 1, scheme 2, scheme 3, and scheme 4, respectively. As shown in Figure 20, the elastic vibration of the passive flexible link 3 is suppressed in scheme 1 and scheme 4 (see Figures 20(b) and 20(e)), and the other schemes cannot effectively suppress elastic vibration of passive flexible link 2 (see in Figures 20(c) and 20(d)).
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From Figures 18–20, one can find that each separate controlled flexible link can only suppress the elastic vibration of itself and cannot suppress the elastic vibration of the other two flexible links. When three passive flexible links exert control simultaneously, all of the elastic vibrations of three passive flexible links can be suppressed. Because coupling of the elastic vibration between three passive flexible links exists, the control effect is slightly worse than that of each separate controlled flexible link controlling its own vibration; however, the whole control effect of scheme 1 is better than that of the other schemes. Meanwhile, the four control schemes can not only suppress residual elastic vibration of the corresponding passive flexible link but also suppress the elastic vibration of flexible links during the moving of the system.
Figures 21(a) and 21(b) are the control voltages of PZT actuator 1 with scheme 1 and scheme 2, respectively. Figures 22(a) and 22(b) are the control voltages of PZT actuator 2 with scheme 1 and scheme 2, respectively. Figures 23(a) and 23(b) are the control voltages of PZT actuator 3 with scheme 1 and scheme 3, respectively. Figures 24(a) and 24(b) are the control voltages of PZT actuator 4 with scheme 1 and scheme 3, respectively. Figures 25(a) and 25(b) are the control voltages of PZT actuator 5 with scheme 1 and scheme 4, respectively. Figures 26(a) and 26(b) are the control voltages of PZT actuator 6 with scheme 1 and scheme 4, respectively.
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From Figures 21–26, one can observe that the control voltages are consistent for suppressing the vibration of the same passive flexible link. Because the output voltage range of the PZT drive power is limited at V, when the feedback voltages of DAC of dSPACE go beyond V, the output voltages of the PZT drive power will be intercepted to V (feedback voltages are amplified 15 times). From Figures 21–26 and Table 1, one can observe that although the control voltage exerted on PZT actuator of passive flexible link 1 is very high (peak value), the control effect is not adequate, with the maximum decrease of PSD1 of 8.45%. The control voltages exerted on passive flexible links 2 and 3 are smaller than the control voltage of passive flexible link 1, but the control effect is better than passive flexible link 1 (passive flexible link 2 decreases by 31.59%; passive flexible link 3 decreases by 43.3%) because the control effect is closely related to the pose of the planar 3-RRR parallel robots and the motion trajectory of the moving platform. In general, due to the usage of mode filter technology, a time-lag exists between the control signal and the original signal. Thus, the control effect is not completely satisfying.
6. Conclusions
An active vibration control experiment of plane 3-RRR flexible parallel robots was studied in this paper. The strain rate feedback controller was designed based on the general motion equation, which considers the direct and inverse piezoelectric equation of the PZT actuator and the PZT sensor. Four control schemes are designed in the experiment: three passive flexible links are controlled at the same time: only passive flexible link 1 is controlled, only passive flexible link 2 is controlled, and only passive flexible link 3 is controlled. The experimental results indicate that each separate controlled flexible link only suppresses its own elastic vibration and cannot suppress the elastic vibration of the other flexible links, whereas three passive flexible links being controlled at the same time can effectively suppress the elastic vibration of all of the flexible links. The manufacture error and assembly error of the experiment platform, friction, time-lag, and gap between joints lead to the gain parameter not completely matching the theoretical value. The gain parameter must be optimized to improve the control performance. There are many high-frequency noise signals that come from the servomotor, and the rigid motion and flexibility of the joints will mix into the collected signals through the PZT sensor. Filter technology is used to remove high-frequency noise signals, but phase-lag exists in the filtered signal that influences the control performance. Thus, the performance of the strain rate feedback controller will be confined, and these issues will be considered to improve the controller performance in a future study.
Competing Interests
The authors declare that they have no competing interests.
Acknowledgments
This work was supported by the National Natural Science Foundation of China (Grants nos. U1501247, 61603103, and 51505092), the of Natural Science Foundation Guangdong Province (Grants nos. 2014A030313616, 2015A030310181, and 2016A030310293), the Science and Technology Planning Project of Guangdong Province (2014A010104017 and 2015B010101015), and the Science and Technology Innovation Project of Foshan (2015AG10018). These supports are greatly acknowledged.