Open access peer-reviewed chapter

On Variable Structure Control Approaches to Semiactive Control of a Quarter Car System

By Mauricio Zapateiro, Francesc Pozo and Ningsu Luo

Submitted: December 16th 2011Reviewed: May 31st 2012Published: September 5th 2012

DOI: 10.5772/50325

Downloaded: 1846

1. Introduction

Vehicle suspension systems are one of the most critical components of a vehicle and it have been a hot research topic due to their importance in vehicle performance. These systems are designed to provide comfort to the passengers to protect the chassis and the freigt [Zapateiro et al., 2012]. However, ride comfort, road holding and suspension deflection are often conflicting and a compromise of the requirements must be considered. Among the proposed solutions, active suspension is an approach to improve ride comfort while keeping suspension stroke and tire deflection within an acceptable level [Gao et al., 2010, Sun et al., 2011].

In semiactive suspension, the value of the damper coefficient can be controlled and can show reasonable performance as compared to that of an active suspension control. Besides, it does not require external energy. For instance, in the work by [Rashid et al., 2011] a semiactive suspension control of a quarter-car model using a hybrid-fuzzy-logic-based controlled is developed and implemented. [Wang et al., 2003] formulated a force-tracking PI controller for an MR-damper controlled quarter-car system. The preliminary results showed that the proposed semiactive force tracking PI control scheme could provide effective control of the sprung mass resonance as well as the wheel-hop control. Furthermore, the proposed control yields lower magnitudes of mass acceleration in the ride zone. [Yao et al., 2002] designed a semi active suspension system using a magnetorhelogical damper. The control law was formulated following the sky-hook technique in which the direction of the relative velocity between the sprung and unsprung masses is compared to that of the velocity of the unsprung mass. Depending on this result, an on-off action is performed. [Du et al., 2005] designed a semiactive static output Hcontroller for a quarter car system equipped with a magnetorheological damper. In this case, the control law was formulated in order to regulate the vertical acceleration as a measure to keep passengers’ comfort within acceptable limits. They also added a constraint in order to keep the transfer function form road disturbance to suspension deflection small enough to prevent excessive suspension bottoming.

Backstepping is a recursive design for systems with nonlinearities not constrained by linear bounds. The ease with which backstepping incorporated uncertainties and unknown parameters contributed to its instant popularity and rapid acceptance. Applications of this technique have been recently reported ranging from robotics to industry or aerospace [Chen Weng, 2010, Wang et al., 2009, Tong et al., 2009, Liu et al., 2010, Chen et al., 2010]. Backstepping control has also been explored in some works about suspension systems. For example, [Zapateiro et al., 2009a] designed a semiactive backstepping control combined with neural network (NN) techniques for a system with MR damper. In that work, the controller was formulated for an experimental platform, whose MR damper was modeled by means of an artificial neural network. The control input was updated with a backstepping controller. On the other hand, [Nguyen et al., 2001] studied a hybrid control of active suspension systems for quarter-car models with two-degrees-of-freedom. This hybrid control was implemented by controlling the linear part with Htechniques and the nonlinear part with an adaptive controller based on backstepping.

Some works on Quantitative Feedback Theory (QFT) applied to the control of suspension systems can be found in the literature. For instance, [Amani et al., 2004] analyzed Hand QFT controllers designed for an active suspension system in order to account for the structured and unstructured uncertainties of the system. As a result, the vertical body acceleration in QFT-controlled is lower than that of the H-controlled and its performance is superior. In the presence of a hydraulic actuator, the QFT-controlled system performance degrades but it is still comparable to that of the H-control. [Zapateiro et al., 2012] addressed a study leading to compare the performance of backstepping and QFT controllers in active and semiactive control of suspension systems. In this case, the nonlinearities were treated as uncertainties in the model so that the linear QFT could be applied to the control formulation. As a result, similar performances between both classes of controllers were achieved.

In this chapter, we will analyze three model-free variable structure controllers for a class of semiactive vehicle suspension systems equipped with MR dampers. The variable structure control (VSC) is a control scheme which is well suited for nonlinear dynamic systems [Glizer et al., 2012]. VSC was firstly studied in the early 1950’s for systems represented by single-input high-order differential equations. A rise of interest became in the 1970’s because the robustness of VSC were step by step recognized. This control method can make the system completely insensitive to time-varying parameter uncertainties, multiple delayed state perturbations and external disturbances [Pai, 2010]. Nowadays, research and development continue to apply VSC control to a wide variety of engineering areas, such as aeronautics (guidance law of small bodies [Zexu et al., 2012]), electric and electronic engineering (speed control of an induction motor drive [Barambones and Alkorta, 2011]). By using this kind of controllers, it is possible to take the best out of several different systems by switching from one to the other. The first strategy that we propose in this work, ϡ1, is based on the difference between the body angular velocity and the wheel angular velocity. The second strategy, ϡ2, more complex, is based both on the difference between the body angular velocity and the wheel angular velocity, and on the difference between the body angular position and the wheel angular position. In this case, the resulting algorithm can be viewed as the clipped control in [Dyke et al., 1996], but with some differences. Finally, the last strategy presented is based on a time variable depending on the absolute value of the difference between the body angular velocity and the wheel angular velocity, and on the difference between the body angular position and the wheel angular position. The study of the three variable structure controllers will be complemented with the comparison of a model-based controller which has been successfully applied by the authors in other works: backstepping. As it was mentioned earlier, backstepping is well suited to this kind of problems because it can account for robustness and nonlinearities. It has been used by the authors to analyze this particular problem [Zapateiro et al., 2012] with interesting results.

The chapter is organized as follows. Section 2 presents the mathematical details of the system to be controlled. In Section 3, the three variable structure controllers are developed. In Section 4, the backstepping control formulation details are outlined. Section 5 shows the numerical results, and in Section 6, the conclusions are drawn.

2. Suspension system model

The suspension system can be modeled as a quarter car model, as shown in Figure 1. The system can be viewed as a composition of two subsystems: the tyre subsystem and the suspension subsystem. The tyre subsystem is represented by the wheel mass muwhile the suspension subsystem consists of a sprung mass, ms, that resembles the vehicle mass. This way of seeing the system will be useful later on when designing the model-based semi active controller. The compressibility of the wheel pneumatic is kt, while csand ksare the damping and stiffness of the uncontrolled suspension system. The quarter car model equations are given by:

msx̥4+cs(x4-x2)+ksx3-fmr=0E1
mux̥2-cs(x4-x2)-ksx3+ktx1+fmr=0E2

where:

x1is the tyre deflection

x2is the unsprung mass velocity

x3is the suspension deflection

x4is the sprung mass velocity.

Figure 1.

Quarter car suspension model

Taking x1, x2, x3and x4as state variables allows us to formulate the following state-space representation:

  • Tyre subsystem:

x̥1=x2-dx̥2=-ktmux1+ϟuE3
  • Suspension subsystem:

x̥3=-x2+x4x̥4=-uE4

where ϟ=ms/mu, dis the velocity of the disturbance input and uis the acceleration input due to the damping subsystem. The input uis given by:

u=1ms(ksx3+cs(x4-x2)-fmr)E5

where fmris the damping force generated by the semiactive device. In this study, we assume that the semiactive device is magnetorheological (MR) damper. It is modeled according to the following Bouc-Wen model [Spencer et al., 1997]:

fmr=c0(v)z4+k0(v)z3+Ϗ(v)ϔE6
ϔ̥=-ϒ|z4|ϔ|ϔ|n-1-ϐz4|ϔ|n+Ϙz4E7

where ϔis an evolutionary variable that describes the hysteretic behavior of the damper, z4is the piston velocity, z3is the piston deflection and vis a voltage input that controls the current that generates the magnetic field; ϒ, ϐ, Ϙand nare parameters that are chosen so to adjust the hysteretic dynamics of the damper; c0(v)=c0a+c0bvrepresents the voltage-dependent damping, k0(v)=k0a+k0bvrepresents the voltage-dependent stiffness and Ϗ(v)=Ϗa+Ϗbvis a voltage-dependent scaling factor.

3. Variable structure controller formulation

Feedback control radically alters the dynamics of a system: it affects its natural frequencies, its transient response as well as its stability. The MR damper of the quarter-car model considered in this study is voltage-controlled, so the voltage (v) is updated by a feedback control loop.

It is well known that the force generated by the MR damper cannot be commanded; only the voltage vapplied to the current driver for the MR damper can be directly changed. One of the first control approaches involving an MR damper was proposed by [Dyke et al., 1996] and called it clipped optimal control. In this approach, the command voltage takes one of two possible values: zero or the maximum. This is chosen according to the following algorithm:

v=VmaxH{(fd-fmr)fmr}E8
=Vmax2sgn(fd-fmr)fmr+1,E9

where Vmaxis the maximum voltage to the current driver associated with saturation of the magnetic field in the MR damper, H()is the Heaviside step function, fdis the desired control force and fmris the measured force of the MR damper.

The sign part of equation (9) can be transformed in the following way:

sgnfd-fmrfmr=1,fd-fmrfmr>0-1,fd-fmrfmr<0=1,fd-fmr>0andfmr>0orfd-fmr<0andfmr<0-1,fd-fmr>0andfmr<0orfd-fmr<0andfmr>0=1,fd>fmrandfmr>0orfd<fmrandfmr<0-1,fd>fmrandfmr<0orfd<fmrandfmr>0=1,fd>fmrandfmr>01,fd<fmrandfmr<0-1,fd>fmrandfmr<0-1,fd<fmrandfmr>0

Finally, the full expression in equation (9) can be rewritten as a piecewise function in the following way:

Vmax2sgn(fd-fmr)fmr+1=Vmax,fd>fmrandfmr>0Vmax,fd<fmrandfmr<00,fd>fmrandfmr<00,fd<fmrandfmr>0

This algorithm for selecting the command signal is graphically represented in Figure 2. More precisely, the shadowed area in Figure 2 is the area where fd>fmrand fmr>0, or fd<fmrand fmr<0. Note that in that particular work, they used the voltage as the control signal because that is the way that current driver can be controlled.

Figure 2.

Graphical representation of the algorithm in equation (8) for selecting the command signal.

In this paper we consider the same idea of changing the voltage. This control signal is computed according to the following control strategies, computed as a function of the sprung mass velocity (x4), the unsprung mass velocity (x2), and the suspension deflection (x3):

ϡ1:v(x2,x4)=Vmax2sgn(x4-x2)+1E10
ϡ2:v(x2,x3,x4)=Vmax2sgnsgn(x4-x2)+x3+1E11
ϡ3:v(x2,x4)=Vmax2[sgn(r)+1],drdt=-100r|x4-x2|-10(x4-x2)E12

Variable structure controllers (VSC) are a very large class of robust controllers [Gao Hung, 1993]. The distinctive feature of VSC is that the structure of the system is intentionally changed according to an assigned law. This can be obtained by switching on or cutting off feedback loops, scheduling gains and so forth. By using VSC, it is possible to take the best out of several different systems (more precisely structures), by switching from one to the other. The control law defines various regions in the phase space and the controller switches between a structure and another at the boundary between two different regions according to the control law.

The three strategies presented in this section can be viewed as variable structure controllers, since the value of the control signal is set to be zero or one, as can be seen in the following transformations:

ϡ1:v(x2,x4)=Vmax2sgn(x4-x2)+1E13
=0,ifβϧ<0,Vmax,ifβϧ0E14
ϡ2:v(x2,x3,x4)=Vmax2sgnsgn(x4-x2)+x3+1E15
=0,ifβϧ<0,x3<1(regionIV),0,ifβϧ>0,x3<-1(regionI),Vmax,ifβϧ<0,x31(regionII),Vmax,ifβϧ0,x3-1(regionIII)E16
ϡ3:v(x2,x4)=Vmax2[sgn(r)+1]E17
=0,ifr<0,Vmax,ifr0,drdt=-100r|x4-x2|-10(x4-x2)E18

where βϧ=x4-x2. In Figure 3 we hace depicted the graphical representation of the strategy ϡ2for selecting the command signal.

Figure 3.

Graphical representation of the strategy ϡ2 for selecting the command signal.

Semi-active control have two essential characteristics. The first is that the these devices offer the adaptability of active control devices without requiring the associated large power sources. The second is that the device cannot inject energy into the system; hence semi-active control devices do not have the potential to destabilize (in the bounded input–bounded output sense) the system [Soong Spencer, 2002]. As a consequence, the stability of the closed-loop system is guaranteed.

4. Backstepping controller formulation

In this section we present the formulation of a model-based controller. The objective, as explained in the Introduction, is to make a comparison between this model-based controller and the VSC controllers. We will appeal to the backstepping technique that has been developed in previous works for this kind of systems.The objective is to design an adaptive backstepping controller to regulate the suspension deflection with the aid of an MR damper thus providing safety and comfort while on the road. The adaptive backstepping controller will be designed in such a way that, for a given ϑ>0, the state-dependent error variables e1and e2(to be defined later) accomplish the following Hperformance J<0:

J=0(eTRe-ϑ2wTw)dtE19

where e=(e1,e2)Tis a vector of controlled signals, R=diag{r1,r2}is a positive definite matrix and wis an energy-bounded disturbance.

In order to formulate the backstepping controller, the state space model (3) - (4) must be first written in strict feedback form [Krstic et al., 1995]. Therefore, the following coordinate transformation is performed [Karlsson et al., 2001]:

z1=x1+ϟϟ+1x3z2=1ϟ+1x2+ϟϟ+1x4z3=x3z4=-x2+x4E20

The system, represented in the new coordinates, is given by:

  • Tyre subsystem:

z̥1=z2-dz̥2=-kt[mu(ϟ+1)]-1z1+ϟkt[mu(ϟ+1)2]-1z3E21
  • Suspension subsystem:

z̥3=z4z̥4=ktmu-1z1-ktϟ[mu(ϟ+1)]-1z3-(ϟ+1)uE22

Substitution of the expression for u(5) into (22) yields:

z̥3=z4z̥4=ktmu-1z1-ktϟ[mu(ϟ+1)]-1z3-(ϟ+1)ms-1[ksx3+cs(x4-x2)-fmr]=-[ktmsϟ(ϟ+1)-1+(ϟ+1)ksmu](mums)-1z3+ktmu-1z1-(ϟ+1)ms-1csz4+(ϟ+1)ms-1fmr=di-akz3-acz4+affmrE23

where ak=[ktmsϟ(ϟ+1)-1+(ϟ+1)ksmu](mums)-1, ac=(ϟ+1)ms-1csand af=(ϟ+1)ms-1; di=ktms-1z1reflects the fact that the disturbance enters to the suspension subsystem through the tyre subsystem.

Assume that akand acin (23) are uncertain constant parameters whose estimated values are a̠kand a̠c, respectively. Thus, the errors between the estimates and the actual values are given by:

a̡k=ak-a̠kE24
a̡c=ac-a̠cE25

Let ad=kt[mu(ϟ+1)]-1, an=ϟkt[mu(ϟ+1)2]-1and am=ktmu-1. From (21) - (22), it can be shown that the transfer functions from d(t)and fmr(t)to z1(t)are:

Z1(s)D(s)=-s(s2+acs+ak)s4+acs3+(ad+ak)s2+adacs+adak-amanE26
Z1(s)Fmr(s)=anafs4+acs3+(ad+ak)s2+adacs+adak-amanE27

If the poles of the transfer functions (26) and (27) are in the left side of the splane, then we can guarantee the bounded input - bounded output (BIBO) stability of Z1(s)for any bounded input D(s)and Fmr(s). Thus, the disturbance input di(t)in (23) is also bounded. This boundedness condition will be necessary later in the controller stability condition.

Finally, since di(t)is the only disturbance input to the suspension subsystem, the vector wof the Hperformance objective as given in (19) becomes:

J=0(eTRe-ϑ2di2)dtE28

In order to begin with the adaptive backstepping design, we firstly define the following error variable and its derivative:

e1=z3E29
e̥1=z̥3=z4E30

Now, the following Lyapunov function candidate is chosen:

V1=12e12E31

whose first-order derivative is:

V̥1=e1e̥1=e1z4E32

Equation (30) can be stabilized with the following virtual control input:

z4d=-r1e1E33
z̥4d=-r1e̥1=-r1z4E34

where r1>0. Now define a second error variable and its derivative:

e2=z4-z4dE35
e̥2=z̥4-z̥4dE36

Therefore,

V̥1=e2z4=e1(e2-r1e1)=e1e2-r1e12E37

On the other hand, the derivatives of the errors of the uncertain parameter estimations are given by:

ḁ̡k=-a̠̥kE38
ḁ̡c=-a̠̥cE39

Now, an augmented Lyapunov function candidate is chosen:

V=V1+12e22+12rka̡k2+12rca̡c2E40

Thus, by using (35) - (39) and the fact that ak=a̡k+a̠kand ac=a̡c+a̠c, the derivative of Vyields:

V̥=e1e̥1+e2e̥2+rk-1a̡kḁ̡k+rc-1a̡cḁ̡c=e1e2-r1e12+e2di-akz3e2-acz4e2+affmre2-r1z4e2-rk-1a̡ka̠̥k-rc-1a̡cḁc=e1e2-r1e12+e2di+affmre2-r1z4e2-rk-1a̡ka̠̥k-(a̡k+a̠k)z3e2-(a̡c+a̠c)z4e2-rc-1a̡ca̠̥c=e1e2-r1e12+e2di-a̡k(z3e3+rk-1a̠̥k)-a̠kz3e2-a̡c(z4e2+rc-1a̠̥c)-a̠cz4e2+af+fmre2-r1z4e2E41

Now consider the following adaptation laws:

z3e1+rk-1a̠̥k=0E42
z4e2+rc-1a̠̥c=0E43

Substitution of (42) and (43) into (41) yields:

V̥=-r1e12+e2di+e2(e1-a̠kz3-a̠cz4+affmr-r1z4)E44

By choosing the following control law:

fmr=-e1-a̠kz3-a̠cz4-r1z4+r2e2+e2(2ϑ)-2afE45

with ϑ>0and r2>0, we get:

V̥=-r1e12+e2di-r2e22-e22(2ϑ)-2=-r1e12+e2di-r2e22-e22(2ϑ)-2+ϑ2di2-ϑ2di2=-r1e12-r2e22+ϑ2di2-(ϑdi-e2(2ϑ)-2)2V̥-r1e12-r2e22+ϑ2di2E46

The objective of guaranteeing global boundedness of trajectories is equivalently expressed as rendering V̥negative outside a compact region. As stated earlier, the disturbance input diis bounded as long as the poles of the transfer functions (26) and (27) are in the left side of the splane. When this is the case, the boundedness of the input disturbance diguarantees the existence of a small compact region DR2(depending on ϑand diitself) such that V̥is negative outside this set. More precisely, when r1e12+r2e22<ϑ2di2, V̥is positive and then the error variables are increasing values. Finally, when the expression r1e12+r2e22is greater than ϑ2di2, V̥is then negative. This implies that all the closed-loop trajectories have to remain bounded, as we wanted to show. Now, under zero initial conditions, from 46 we can write:

0V̥dt-0r1e12dt-0r2e22dt+0ϑ2di2dtE47

or, equivanlently,

V|t=-V|t=0-0eTRedt+ϑ20di2dtE48

Then, it can be shown that

J=0(eTRe-ϑ2di2)dt-V|t=0E49
(49)

Thus, the adaptive backstepping controller satisfies both the Hperformance and the asymptotic stability of the system.

The control force given by (45) can be used to drive an actively controlled damper. However, the fact that semiactive devices cannot inject energy into a system, makes necessary the modification of this control law in order to implement it with a semiactive damper; that is, semiactive dampers cannot apply force to the system, only absorb it. There are different ways to perform this [Zapateiro et al., 2009b, Arash et al., 2010]. In this work, we will calculate the MR damper voltage making use of its mathematical model. Thus, the following control law is proposed:

v=-e1-a̠zz3+a̠cz4+r1z4-r2e2-e2(2ϑ)-2+af(c0az4+k0az3+Ϗaϔ)af(c0bz4+k0bz3+Ϗbϔ)E50

provided that af(c0bz4+k0bz3+Ϗbϔ)0; otherwise, v=0.

The same process followed to obtain the control law (45) can be used to demonstrate that the control law (4) does stabilize the system. Begin by replacing (6) into (44) in order to obtain:

V̥=-r1e12+e2di+e2[e1-a̠kz3-a̠cz4+af(c0az4+k0az3+Ϗaϔ)+af(c0bz4+k0bz3+Ϗbϔ)v-r1z4]E51

Thus, by replacing the control law of (4) into (51) we also get V̥-r1e12-r2e22+ϑ2di2and, as previously stated, the stability of the system is guaranteed.

Finally, we can write the control law in terms of the state variables as follows:

v=-a̠c-r1+r2+(2ϑ)-2+afc0ax2+-1-a̠z-r1r2+r1(2ϑ)-2+afk0ax3-afc0bx2+afk0bx3+afc0bx4+afϏbϔ+z̠c+r1-r2-(2ϑ)-2+afc0ax4+afϏaϔ-afc0bx2+afk0bx3+afc0bx4+afϏbϔE52

5. Numerical simulations

In this section we will analyze the performance results obtained form simulations performed in Matlab/SImulink. The numerical values of the model that we used in this study. Thus: Ϗa=332.7N/m, Ϗb=1862.5NV/m, c0a=7544.1Ns/m, c0b=7127.3NsV/m, k0a=11375.7N/m, k0b=14435.0NV/m, ϒ=4209.8m-2, Ϙ=10246and n=2. This is a scaled version of the MR damper found in [Carrion Spencer, 2007]. The parameter values of the suspension system are [Karlsson et al., 2001]: ms=11739 kg, mu=300 kg, ks=252000 N/m, cs=10000 Ns/m and kt=300000 N/m. In order to facilitate the analysis, we will quantify the performance results by means of the indices shown in Table 0. Indices J1- J3show the ratio between the peak response of the controlled suspension system (displacement, velocity and acceleration) and that of the uncontrolled system. Indices J4- J6are the normalized ITSE (integral of the time squared error) signals that indicate how much the displacement, velocity and acceleration are attenuated compared to the uncontrolled case. Index J7is the relative maximum control effort with respect to the weight of the suspension system. Small indices indicate good control performance. Two scenarios are considered: an uneven road, simulated by random vibrations and the presence of a bump on the road.

We assume that the car has laser sensors that allow us to read the position of the sprung and unsprung masses. Since the velocities are needed for control implementation, these are obtained by first low-pass filtering the displacement readings and then applying a filter of the form s(ϙs+1)qthat approximates the derivative of the signal. In this filter, ϙis a sufficiently small constant that can be obtained from the ratio between the two-norm of the second derivative of the signal and the noise amplitude; qis the order of the filter which should be at lest equal to 2. Choosing parameters this way, allows for minimizing the error between the real and the estimated signal derivatives [Braci Diop, 2003].

IndexDefinition
J1=max|x3(t)|contmax|x3(t)|uncNorm. peak suspension deflection.
J2=max|x4(t)|contmax|x4(t)|uncNorm. peak sprung mass velocity.
J3=max|x̥4(t)|contmax|x̥4(t)|uncNorm. peak sprung mass acceleration.
J4=0Ttx3cont2(t)dt0Ttx3unc2(t)dtNorm. suspension deflection ITSE.
J5=0Ttx4cont2(t)dt0Ttx4unc2(t)dtNorm. sprung mass velocity ITSE.
J6=0Ttx̥4cont2(t)dt0Ttx̥4unc2(t)dtNorm. sprung mass acceleration ITSE.
J7=max|fmr(t)|wsMaximum control effort.

Table 1.

Performance indices.

In the first scenario, the unevenness of the road was simulated by random vibration, as shown in Figure 4. This figure also compares the performance of the three ϡcontrollers. What we can see for this figure, is that the three VSC controllers perform in a similar way and satisfactorily control the deflection of the tyre subsystem. In Figure 5, we see the performance of the same controllers at regulating the suspension deflection. Once again, the three controllers accomplish the objective in a similar way. This visual observations can be confirmed by analyzing the performance indices of Table 1. In Figures 6 and 7, we can see a comparison of the ϡ3controller and the backstepping controller. A notable superiority of the VSC controller is observed over the backstepping controller. It can be due to the fact that this kind of controllers are more sensitive to the fast-changing dynamics of a signal, in this case, the velocity, which can make it react faster. The performance indices of Table 1 also show that it is harder for the backstepping controller to keep the peak acceleration, velocity and displacement under acceptable limits, despite its control effort is much higher than that of the VSC controllers.

Figure 4.

Uneven road disturbance and tyre subsystem response.

Figure 5.

Uneven road disturbance and tyre subsystem response.

Indexϡ1ϡ2ϡ3Backstepping
J10.12880.12800.09930.5144
J20.14850.14880.21570.9800
J30.22050.28030.28031.2586
J40.00590.00580.00530.2317
J50.00900.00890.01810.5852
J60.01890.01870.03100.9615
J70.12680.12790.14710.4538

Table 2.

Performance indices of the random unevenness disturbance case.

Figure 6.

Uneven road disturbance and tyre subsystem response.

Figure 7.

Uneven road disturbance and car subsystem response.

In the second scenario a bump on the road is simulated as seen in Figure 8. In this case, the VSC controllers have a similar performance and it happened in the previous scenario. The performance indices of Table 2 confirm this fact. In comparison, the ϡ3controller seems to perform slightly better, specially at reusing the peak response of the suspicion and tyre deflections as can be seen in Figure 10 and 11 where a comparison between then ϡ3and backstepping controllers is illustrated. These results are in the line than those of the first scenario. It is worth noting the fact that the VSC controllers perform better with less control effort.

Figure 8.

Bump on the road disturbance and tyre subsystem response.

Figure 9.

Bump on the road disturbance and tyre subsystem response.

Indexϡ1ϡ2ϡ3Backstepping
J10.83170.83250.45840.4271
J21.15071.15051.34301.3892
J31.11571.26231.26231.3007
J40.16050.16250.22410.0703
J50.18270.17970.26810.4702
J60.41680.41130.58841.0308
J70.36130.36140.41000.4431

Table 3.

Performance indices of the road bump disturbance case.

Figure 10.

Bump on the road disturbance and tyre subsystem response.

Figure 11.

Bump on the road disturbance and car subsystem response.

6. Conclusions

In this chapter we presented the problem of the vibration control in vehicles. One model-based and three variable structure controllers were analyzed and compared in order to study their performance during typical road disturbances. The performance of the controller were also analyzed for the particular situation in which the suspension system is made up of a magnetorheological damper, which is well-known to be a nonlinear device. All of the controllers performed satisfactorily at regulating the suspension deflection while keeping the acceleration, velocity and displacement variables within acceptable limits. One important result obtained in this work was that despite the simplicity of these controllers, they performed significantly better than the model-based controller. It is to be noted that further studies -theoretical and experimental- should be performed in order to get a better insight of the performance of such controllers and the possibilities of being used in real systems.

Acknowledgement

M. Zapateiro has been supported by the ‘Juan de la Cierva’ fellowship from the Government of Spain. This study has also been partially supported by Secretaría de Estado de Investigación, Desarrollo e Innovación (formerly,Ministry of Science and Innovation) through DPI2011-27567-C02-02, DPI2011-28033-C03-01 and DPI 2011-27567-C02-01.

© 2012 The Author(s). Licensee IntechOpen. This chapter is distributed under the terms of the Creative Commons Attribution 3.0 License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

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Mauricio Zapateiro, Francesc Pozo and Ningsu Luo (September 5th 2012). On Variable Structure Control Approaches to Semiactive Control of a Quarter Car System, Advances on Analysis and Control of Vibrations - Theory and Applications, Mauricio Zapateiro de la Hoz and Francesc Pozo, IntechOpen, DOI: 10.5772/50325. Available from:

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