﻿ Finite Frequency Fuzzy <i>H</i><sub>∞</sub> Control for Uncertain Active Suspension Systems With Sensor Failure
 IEEE/CAA Journal of Automatica Sinica  2018, Vol. 5 Issue(4): 777-786 PDF
Finite Frequency Fuzzy H Control for Uncertain Active Suspension Systems With Sensor Failure
Zhenxing Zhang1, Hongyi Li2,3, Chengwei Wu4, Qi Zhou3,5
1. School of Mathematics and Physics, Bohai University, Jinzhou 121013, China;
2. College of Engineering, Bohai University, Jinzhou 121013, China;
3. School of Automation, Guangdong University of Technology, Guangzhou 510006, China;
4. Department of Control Science and Engineering, School of Astronautics, Harbin Institute of Technology, Harbin 150001, China;
5. College of Information Science and Technology, Bohai University, Jinzhou 121013, China
Abstract: This paper investigates the problem of finite frequency fuzzy H control for uncertain active vehicle suspension systems, in which sensor failure is taken into account. TakagiSugeno (T-S) fuzzy model is established for considered suspension systems. In order to describe the sensor fault effectively, a corresponding model is introduced. A vital performance index, H performance, is utilized to measure the drive comfort. In the framework of Kalman-Yakubovich-Popov theory, the H norm from external perturbation to controlled output is optimized effectively in the frequency domain of 4 Hz-8 Hz to enhance ride comfort level. Meanwhile, three suspension constrained requirements, i.e., ride comfort level, manipulation stability, suspension deflection are also guaranteed. Furthermore, sufficient conditions are developed to design a fuzzy controller to guarantee the desired performance of active suspension systems. Finally, the proposed control scheme is applied to a quarter-vehicle active suspension, and simulation results are given to illustrate the effectiveness of the proposed approach.
Key words: Active vehicle suspension systems     finite frequency control     sensor failure     Takagi-Sugeno fuzzy model
Ⅰ. INTRODUCTION

Nowadays, vehicles have become common traffic tools, and it is of great importance to guarantee the comfort and safety of vehicles. There exists a vital part in every vehicle, i.e. the vehicle suspension system, which can isolate the vibration between its chassis and the road surface effectively to make people feel comfortable when they drive [1]-[3]. A vehicle suspension system consists of a fluctuation absorber, spring and damper. The function of a fluctuation absorber is to filter the vibration between human body and road surface. The spring is responsible for bearing the weight of car body, the weight of passengers and isolating the road disturbance. Therefore, it contributes to improving ride comfort. The damper's purpose is to reduce the destabilization between the human body and the wheels. Since ride comfort level is a crucial index to evaluate a vehicle, developing appropriate control approaches for the suspension systems has become an active research field [4], [5].

With regards to suspension systems, ride comfort level, manipulation stability, suspension deflection and actuator saturation are crucial problems, which should be tackled with control strategies. However, the requirements mentioned above are incompatible. For instance, improving drive comfort level will lead to larger suspension deflection and smaller damping in wheel bounce. Active suspension systems provide a way to address these requirements. For example, intelligent approaches, such as, adaptive method [6]-[9], neural networks/fuzzy systems [10], [11], and sliding mode control [12], [13] have been applied to such systems. Gao $\textit{et al.}$ in [14] employed the input delay method to transform the sampled suspension systems into a delayed continuous version and presented a sampled control scheme. For the unavailable states case, an output-feedback control strategy has been proposed for active suspension systems in [15], in which road holding, ride comfort, maximum actuator control force and suspension deflection were regarded as the control objectives to be satisfied. By integrating the adaptive approach into the self-organizing fuzzy sliding mode controller, the author in [16] presented an effective control strategy to ameliorate the performance of the suspension systems. The authors in [17] proposed a robust adaptive control algorithm for suspension systems in the presence of input saturation. In the framework of adaptive backstepping control, the authors in [18] designed an adaptive controller for uncertain active suspension systems and improved the system performance. Using both adaptive technique and neural networks, both a state-feedback controller and an observer-based adaptive neural controller were designed in [19]. By constructing an extended sate observer, a nonlinear tracking control scheme was developed for active suspension systems in [20].

Due to the existence of uncertainty in the payload or the amount of passengers and the coupling phenomenon, the suspension systems have become complex nonlinear systems. Takagi-Sugeno (T-S) fuzzy model is a valid approach and practical tool for depicting complex nonlinear systems [21]-[26]. By using T-S fuzzy model, nonlinear systems can be regarded as a summation of a set of linear subsystems with associated membership functions, which can be further analyzed by employing the linear system theory. Compared with other kinds control schemes [27], [28], T-S fuzzy model can approximate controlled systems with arbitrary accuracy. Using the fuzzy modeling approach, a sliding mode controller with adaptive parameters was designed for suspension systems in [29]. To simultaneously address both input delay and actuator fault problems, the active suspension system was described as a T-S fuzzy model in [30], and a reliable fuzzy controller was designed to ensure the desired performance.

The goal of designing a control scheme for active suspension systems to enhance drive comfort level is to design a robust controller that rejects the vertical disturbance between passengers and the road surface [31]. The authors in [32] applied the ${H}_{\infty }$ control theory to a full-vehicle suspension model and derived sufficient conditions that ensured the robust performance of suspension systems. In [33], by utilizing a parameter-dependent controller design method, both a state-feedback controller and an output-based controller were designed, which achieved good active suspension performance. Note that these design approaches are merely considered in entire frequency domain. According to the standard ISO2361, the vertical vibration in the finite frequencies from 4 Hz-8 Hz is the most sensitive range for human body. Since ${H}_{\infty }$ control is an effective approach to guarantee constrained requirements of suspension systems, therefore, how to apply the ${H}_{\infty }$ control approach to active suspension systems in finite frequency domain is a significant work. Until now, there have been several techniques used for finite frequency domain control, e.g. the weighting function approach [34], and the grid frequency axis method [35]. The weighting function approach is quite useful, but additional weight leads to increased complexity of systems and selecting appropriate wight functions needs much time and energy. Although the grid frequency axis method performs well in practice, it cannot guarantee the desired system performance in the design process. Another technique that addresses finite frequency problem is the generalized Kalman-Yakubovic-Popov (KYP) lemma, which builds bridges between the frequency inequality of transfer function and the linear matrix inequality (LMI) associated with state space [36], [37]. It allows us to utilize the LMI to depict frequency characteristics of dynamic systems. Sun $\textit{et al.}$ in [38] presented an ${H}_{\infty}$ control method for active suspension systems in finite frequency range, where the actuator input delay was taken into consideration. Considering partial unmeasurable states in suspension systems, a dynamic output-feedback control scheme was developed to stabilize the suspension systems and achieve constrained requirements in finite frequency domain [39].

It should be pointed out that it is inevitable for active suspension systems to suffer from failure due to the sensor aging and driving for a long time, which should not be neglected. Many related results have been published, see for example, [40]-[42] and the references therein. Feng $\textit{et al.}$ in [43] established a sensor failure model and proposed a dissipative reliable filtering approach to guarantee performance of filtering error systems. By constructing a reaction force observer, the fault-tolerant control problem for a flexible arm with sensor fault was solved in [44]. The authors in [45] established a fault detection scheme and designed a sliding mode controller for full-vehicle suspension systems with sensor failure. However, to the authors' best knowledge, the problem of fuzzy state-feedback control for active suspension systems in finite frequency domain has not been investigated in existing literature, which is an interesting yet challenging issue.

Motivated by the discussion aforementioned, this paper focuses on the finite frequency fuzzy ${H}_{\infty}$ control problem for uncertain active vehicle suspension systems. The considered active suspension system is described as a T-S fuzzy model. In the framework of generalized KYP lemma, a fuzzy state-feedback control scheme is proposed to improve drive comfort level and guarantee suspension constrained requirements. The main contributions of this paper can be summarized as follows:

1) Compared with the results in [46], T-S fuzzy model, which is an effective strategy to describe complex nonlinear systems, is applied to modeling active suspension systems in the framework of finite frequency control. Moreover, the uncertain parameters are described effectively.

2) Sensor failure, a ubiquitous issue, which can decrease, and even deteriorate the system performance, is taken into consideration to guarantee the reliability of the active vehicle suspension systems.

3) Sufficient conditions are derived to design the controller to improve the drive comfort level in concerned finite frequency domain and guarantee active suspension constrained requirements.

Finally, simulation results are provided to demonstrate the usefulness of the control scheme proposed in this paper.

The rest of this paper is as follows. Section Ⅱ provides problem formulation. The main results are presented in Section Ⅲ. Simulation results are given in Section Ⅳ to demonstrate the validity of the control method. The conclusion is given in Section Ⅴ.

$\mathit{Notations:}$ The superscripts $T$ and $-1$ are employed to denote the matrix transposition and inverse, respectively. The orthogonal complement of matrix $\mathcal{P}$ is represented by $\mathcal{P}^{\perp }$. The block diagonal matrix is expressed by $\text{diag}\{\ldots \}$. The symbol $[\mathcal{A}]_{s}$ is equivalent to $\mathcal{A}+\mathcal{A} ^{T}.$ $\mathcal{I}$ and $0$ stand for the identity and zero matrix with appropriate dimensions, respectively. $\mathcal{P}>0$ is adopted to represent that $\mathcal{P}$ is a positive definite matrix. The mark $(\star )$ is utilized to denote the term which has a symmetric property. $\{\cdot \}_{\theta }$ $(\theta =1, 2, \ldots )$ means the $\theta$-th line of a matrix. If the dimension of a matrix is not described in details, we assume that it has an appropriate dimension.

Ⅱ. PROBLEM FORMULATION

Targeted at proposing a reliable fuzzy finite frequency control strategy, this section introduces some lemmas which will be utilized in this paper, describinges a quarter-vehicle model, models uncertain vehicle suspension systems, establishes a sensor failure model and provides control objectives of active suspension systems. Next, the corresponding descriptions will be presented.

The following lemmas correspond to the Generalized KYP lemma, Projection theorem and Reciprocal Projection theorem.

Lemma 1 [47]: Given a linear system $(\mathcal{\bar{A}}, \mathcal{\bar{B}}, \mathcal{\bar{C}}, \mathcal{\bar{D}})$ and a symmetric matrix $\bar{\Gamma} ,$ the following conditions are equivalent,

1) The following finite frequency inequality holds,

 $\begin{equation*} \left[ \begin{array}{c} \Psi (j\sigma ) \\ \mathcal{I} \end{array} \right] ^{T}\bar{\Gamma} \left[ \begin{array}{c} \Psi (j\sigma ) \\ \mathcal{I} \end{array} \right] <0, \ \bar{\sigma}_{1}\leq \sigma \leq \bar{\sigma}_{2}. \end{equation*}$

2) There exist a symmetric matrix $\mathcal{P}$ and a positive definite matrix $\mathcal{Q}$ such that

 $\begin{equation*} \left[ \begin{array}{cc} \Gamma \lbrack \mathcal{P}, \mathcal{Q}, \mathcal{\bar{C}}, \mathcal{\bar{D}}] & \left[ \begin{array}{cc} \mathcal{\bar{C}}&\mathcal{\bar{D}} \end{array} \right] ^{T} \\ \star&-\mathcal{I} \end{array} \right] <0 \end{equation*}$

where

 $\begin{array}{l} \Gamma [{\cal P}, {\cal Q}, \bar {\cal C}, \bar {\cal D}] = {\left[ {\begin{array}{*{20}{c}} {\bar {\cal A}}&{\bar {\cal B}}\\ {\cal I}&0 \end{array}} \right]^T}\left[ {\begin{array}{*{20}{c}} { - {\cal Q}}&{{\cal P} + j{{\bar \sigma }_c}{\cal Q}}\\ {{\cal P} - j{{\bar \sigma }_c}{\cal Q}}&{ - {{\bar \sigma }_1}{{\bar \sigma }_2}{\cal Q}} \end{array}} \right]\\ \;\;\;\;\;\;\;\;\;\;\;\;\;\;\;\;\;\;\;\;\;\;\;\;\;\;\; \times \left[ {\begin{array}{*{20}{c}} {\bar {\cal A}}&{\bar {\cal B}}\\ {\cal I}&0 \end{array}} \right] + \left[ {\begin{array}{*{20}{c}} 0&{{{\bar {\cal C}}^T}{{\bar \Gamma }_{12}}}\\ \star &{{{[{{\bar {\cal D}}^T}{\Pi _{12}}]}_s} + {{\bar \Gamma }_{22}}} \end{array}} \right] \end{array}$

$\bar{\sigma}_{c}=(\bar{\sigma}_{1}+\bar{\sigma}_{2})/2$, $\bar{\Gamma}_{12}$ and $\bar{\Gamma} _{22}$ denote the top right and bottom right corners of matrix $\bar{\Gamma} ,$ respectively.

Lemma 2 [48]: For the given matrices $\Theta$, $\Gamma$, $\Lambda ,$ there is a matrix $\mathcal{F}$ such that

 $\begin{equation*} \Gamma \mathcal{F}\Lambda +(\Gamma \mathcal{F}\Lambda )^{T}+\Theta <0 \end{equation*}$

if and only if the following inequalities hold,

 $\begin{equation*} \Gamma ^{\perp }\Theta \Gamma ^{\perp T}<0, \ \Lambda ^{T^{\perp }}\Theta \Lambda ^{T^{\perp ^{T}}}<0. \end{equation*}$

Lemma 3 [48]: The inequality $\Upsilon +\mathcal{\vartheta }+ \mathcal{\vartheta }^{T}<0$ is equivalent to the following form

 $\begin{equation*} \left[ \begin{array}{cc} \Upsilon +\mathcal{P}-\left[ W\right] _{s}&\mathcal{\vartheta }^{T}+ \mathcal{W}^{T} \\ \star&-\mathcal{P} \end{array} \right] <0 \end{equation*}$

where $\mathcal{P}$ is a given positive definite symmetric matrix.

A. Description Of A Quarter-Vehicle Model

In this paper, the quarter-vehicle model depicted in Fig. 1 is considered, which is governed via the following equations,

 $\begin{eqnarray*} m_{s}\ddot{z}_{s}(t)+c_{s}[\dot{z}_{s}(t)-\dot{z} _{u}(t)]+k_{s}[z_{s}(t)-z_{u}(t)] &\hspace{-0.2cm}=&\hspace{-0.2cm}u(t), \\ m_{u}\ddot{z}_{u}(t)+c_{s}[\dot{z}_{u}(t)-\dot{z} _{s}(t)]+k_{s}[z_{u}(t)-z_{s}(t)] \\ +\, k_{t}(z_{u}(t)-z_{r}(t))+c_{t}[\dot{z}_{u}(t)-\dot{z}_{r}(t)] &\hspace{-0.2cm}=&\hspace{-0.2cm}-u(t) \end{eqnarray*}$

where the sprung mass $m_{s}$ and the unsprung mass $m_{u}$ denote the car chassis and the mass of the wheel assembly, respectively. $u(t)$ is the actuator force. $c_{s}$, $k_{s}$, $k_{t}$, $c_{t}$, $z_{s}$ and $z_{u}$ denote damping and stiffness of the suspension system, compressibility and damping of the tyre, and the movements of the sprung and unsprung masses, respectively. $z_{r}$ represents the road movement input.

In order to facilitate describing the above equations in the state space form, define the following variables,

 $\begin{eqnarray*} x_{1}(t) &\hspace{-0.25cm}=&\hspace{-0.25cm}z_{s}(t)-z_{u}(t)\\ x_{2}(t) &\hspace{-0.25cm}=&\hspace{-0.25cm}z_{u}(t)-z_{r}(t) \\ x_{3}(t) &\hspace{-0.25cm}=&\hspace{-0.25cm}\dot{z}_{s}(t), \text{ }x_{4}(t)=\dot{z}_{u}(t)\\ z_{1}(t) &\hspace{-0.25cm}=&\hspace{-0.25cm}\ddot{z}_{s}(t)\\ z_{2}(t) &\hspace{-0.25cm}=&\hspace{-0.25cm}\left[ \begin{array}{cc} \frac{z_{s}(t)-z_{u}(t)}{z_{\max }}&\frac{k_{t}(z_{u}(t)-z_{r}(t))}{ (m_{s}+m_{u})g} \end{array} \right] ^{T} \end{eqnarray*}$

where $x_{1}(t)$ is the suspension deflection, $x_{2}(t)$ stands for the tyre deflection, $x_{3}(t)$ and $x_{4}(t)$ denote sprung mass speed and unsprung mass speed, respectively. By choosing speed input as disturbance input, we have $w(t)=\dot{z}_{r}(t).$ Define

 $\begin{equation*} x(t)=\left[ x_{1}(t)\text{ }x_{2}(t)\text{ }x_{3}(t)\text{ }x_{4}(t)\right] ^{T}. \end{equation*}$

Thus, the quarter-vehicle model can be described as

 $\begin{eqnarray} \dot{x}(t) &\hspace{-0.25cm}=&\hspace{-0.25cm}\mathcal{A}x(t)+\mathcal{B}u(t)+\mathcal{B}_{1}w(t) \notag \\ z_{1}(t) &\hspace{-0.25cm}=&\hspace{-0.25cm}\mathcal{C}_{1}x(t)+\mathcal{D}_{1}u(t) \label{active suspension system} \\ z_{2}(t) &\hspace{-0.25cm}=&\hspace{-0.25cm}\mathcal{C}_{2}x(t) \notag \end{eqnarray}$ (1)

where

 $\begin{eqnarray*} \mathcal{A} &\hspace{-0.25cm}=&\hspace{-0.25cm}\left[ \begin{array}{cccc} 0&0&1&-1 \\ 0&0&0&1 \\ -\frac{k_{s}}{m_{s}}&0&-\frac{c_{s}}{m_{s}}&\frac{c_{s}}{m_{s}} \\ \frac{k_{s}}{m_{u}}&-\frac{k_{t}}{m_{u}}&\frac{c_{s}}{m_{u}}&-\frac{ c_{s}+c_{t}}{m_{u}} \end{array} \right] \\ \mathcal{B}&\hspace{-0.25cm}=&\hspace{-0.25cm}\left[ \begin{array}{c} 0 \\ 0 \\ \frac{1}{m_{s}} \\[2mm] -\frac{1}{m_{u}} \end{array} \right] , \mathcal{B}_{1}=\left[ \begin{array}{c} 0 \\ -1 \\ 0 \\ \frac{c_{t}}{m_{u}} \end{array} \right] \\ \mathcal{C}_{1} &\hspace{-0.25cm}=&\hspace{-0.25cm}\left[ \begin{array}{cccc} -\frac{k_{s}}{m_{s}}&0&-\frac{c_{s}}{m_{s}}&\frac{c_{s}}{m_{s}} \end{array} \right] \\ \mathcal{C}_{2} &\hspace{-0.25cm}=&\hspace{-0.25cm}\left[ \begin{array}{cccc} \frac{1}{z_{\max }}&0&0&0 \\ 0&\frac{k_{t}}{(m_{s}+m_{u})g}&0&0 \end{array} \right] \\ \mathcal{D}_{1} &\hspace{-0.25cm}=&\hspace{-0.25cm}\frac{1}{m_{s}}. \end{eqnarray*}$
B. T-S Fuzzy Modelling

The vehicle mass is regarded as a varying parameter since vehicle load is often uncertain due to variation in the payload or the number of passengers. Based on the mechanical structure, the unsprung mass is assumed to be a varying parameter. Accordingly, the vehicle suspension system including both the sprung mass $m_{s}$ and the unsprung mass $m_{u}$ in (1) is an uncertain model. Assuming that they vary in a given range, that is

 $\begin{equation*} m_{s\min }\leq m_{s}\leq m_{s\max } \end{equation*}$
 $\begin{equation*} m_{u\min }\leq m_{u}\leq m_{u\max } \end{equation*}$

the following equalities can be obtained,

 $\begin{eqnarray*} \max \frac{1}{m_{s}} &\hspace{-0.2cm}=&\hspace{-0.2cm}\frac{1}{m_{s\min }}=\hat{m}_{s}, \min \frac{1}{m_{s} }=\frac{1}{m_{s\max }}=\check{m} \\ \max \frac{1}{m_{u}} &\hspace{-0.2cm}=&\hspace{-0.2cm}\frac{1}{m_{u\min }}=\hat{m}_{u}, \min \frac{1}{m_{u} }=\frac{1}{m_{u\max }}=\check{m}_{u}. \end{eqnarray*}$

According to [49], $\frac{1}{m_{s}}$ and $\frac{1}{m_{u}}$ can be shown as

 $\begin{eqnarray*} \frac{1}{m_{s}} &\hspace{-0.2cm}=&\hspace{-0.2cm}\mathcal{M}_{1}(\phi _{1}(t))\hat{m}_{s}+\mathcal{M} _{2}(\phi _{1}(t))\check{m}_{s}\\ \frac{1}{m_{u}} &\hspace{-0.2cm}=&\hspace{-0.2cm}\mathcal{N}_{1}(\phi _{2}(t))\hat{m}_{u}+\mathcal{N} _{2}(\phi _{2}(t))\check{m}_{u} \end{eqnarray*}$

where $\phi _{1}(t)=\frac{1}{m_{s}}$ and $\phi _{2}(t)=\frac{1}{m_{u}}$ denote premise variables, and

 $\begin{equation*} \mathcal{M}_{1}(\phi _{1}(t))+\mathcal{M}_{2}(\phi _{1}(t))=1 \end{equation*}$
 $\begin{equation*} \mathcal{N}_{1}(\phi _{2}(t))+\mathcal{N}_{2}(\phi _{2}(t))=1. \end{equation*}$

In order to establish the fuzzy model, the membership functions can be described as

 $\begin{eqnarray*} \mathcal{M}_{1}(\phi _{1}(t)) &\hspace{-0.2cm}=&\hspace{-0.2cm}\frac{\frac{1}{m_{s}}-\check{m}_{s}}{\hat{m} _{s}-\check{m}_{s}}, \text{ }\mathcal{M}_{2}(\phi _{1}(t))=\frac{\hat{m}_{s}- \frac{1}{m_{s}}}{\hat{m}_{s}-\check{m}_{s}} \\ \mathcal{N}_{1}(\phi _{2}(t)) &\hspace{-0.2cm}=&\hspace{-0.2cm}\frac{\frac{1}{m_{u}}-\check{m}_{u}}{\hat{m} _{u}-\check{m}_{u}}, \text{ }\mathcal{N}_{2}(\phi _{2}(t))=\frac{\hat{m}_{u}- \frac{1}{m_{u}}}{\hat{m}_{u}-\check{m}_{u}}. \end{eqnarray*}$

The membership functions named Heavy, Light, Heavy and Light are depicted in Fig. 2. The following T-S fuzzy model depicts the active suspension systems with uncertainty.

 Download: larger image Fig. 2 (a) Membership functions $\mathcal{M}_{1}(\phi _{1}(t))$ and $\mathcal{M}_{2}(\phi_{1}(t))$; (b) Membership functions $\mathcal{N}_{1}(\phi _{2}(t))$ and $\mathcal{N}_{2}(\phi _{2}(t))$.

$\mathit{Model\ Rule\ i}$: IF $\phi _{1}(t)$ is $\mathcal{M}_{\theta }(\phi _{1}(t)),$ and $\phi _{2}(t)$ is $\mathcal{N}_{\theta }(\phi _{2}(t))$, THEN

 $\begin{eqnarray*} \dot{x}(t) &\hspace{-0.2cm}=&\hspace{-0.2cm}\mathcal{A}_{i}x(t)+\mathcal{B}_{i}u(t)+\mathcal{B}_{1i}w(t) \\ z_{1}(t) &\hspace{-0.2cm}=&\hspace{-0.2cm}\mathcal{C}_{1i}x(t)+\mathcal{D}_{1i}u(t) \\ z_{2}(t) &\hspace{-0.2cm}=&\hspace{-0.2cm}\mathcal{C}_{2i}x(t) \end{eqnarray*}$

where $\theta =1, 2$, $i=1, \ldots , 4.$ $\mathcal{M}_{1}(\phi _{1}(t))$ represents Heavy and $\mathcal{M}_{2}(\phi _{1}(t))$ represents Light; $\mathcal{N}_{1}(\phi _{2}(t))$ represents Heavy and $\mathcal{N}_{2}(\phi _{2}(t))$ represents Light.

According to fuzzy blending, the whole fuzzy model can be shown as follows:

 $\begin{eqnarray} \dot{x}(t) &\hspace{-0.2cm}=&\hspace{-0.2cm}\underset{i=1}{\overset{4}{\sum }}\omega _{i}(\phi (t))\left[ \mathcal{A}_{i}x(t)+\mathcal{B}_{i}u(t)+\mathcal{B}_{1i}w(t)\right] \notag \\ z_{1}(t) &\hspace{-0.2cm}=&\hspace{-0.2cm}\underset{i=1}{\overset{4}{\sum }}\omega _{i}(\phi (t))\left[ \mathcal{C}_{1i}x(t)+\mathcal{D}_{1i}u(t)\right]\\ z_{2}(t) &\hspace{-0.2cm}=&\hspace{-0.2cm}\underset{i=1}{\overset{4}{\sum }}\omega _{i}(\phi (t))\mathcal{C }_{2i}x(t) \notag \end{eqnarray}$ (2)

where

 $\begin{eqnarray*} \omega _{1}(\phi (t)) &\hspace{-0.2cm}=&\hspace{-0.2cm}\mathcal{M}_{1}(\phi _{1}(t))\times \mathcal{N} _{1}(\phi _{2}(t)) \\ \omega _{2}(\phi (t)) &\hspace{-0.2cm}=&\hspace{-0.2cm}\mathcal{M}_{1}(\phi _{1}(t))\times \mathcal{N} _{2}(\phi _{2}(t)) \\ \omega _{3}(\phi (t)) &\hspace{-0.2cm}=&\hspace{-0.2cm}\mathcal{M}_{2}(\phi _{1}(t))\times \mathcal{N} _{1}(\phi _{2}(t)) \\ \omega _{4}(\phi (t)) &\hspace{-0.2cm}=&\hspace{-0.2cm}\mathcal{M}_{2}(\phi _{1}(t))\times \mathcal{N} _{2}(\phi _{2}(t)) \end{eqnarray*}$

$\omega _{i}(\phi (t))$ represents the grade of membership satisfying

 $\begin{eqnarray*} \omega_{i}(\phi (t))\geq 0, \quad \underset{i=1}{\overset{4}{\sum }}\omega _{i}(\phi(t))=1. \end{eqnarray*}$

For brevity, we define $\omega _{i}=\omega _{i}(\phi (t)),$ $i=1, \ldots , 4,$ in the following analysis.

C. Sensor Failure

Due to the extreme working environment, aging of machinery and overtime operation, it is inevitable for active suspension systems to undergo failure. To address it thoroughly and improve the reliability, the failure model is described as [23],

 $\begin{equation*} \tilde{x}_{j}(t)=\beta _{\varepsilon j}x_{j}(t), \text{ }j=1, 2, \ldots , l \end{equation*}$

where

 $\begin{equation*} 0\leq \underline{\beta }_{\varepsilon j}\leq \beta _{\varepsilon j}\leq \bar{ \beta}_{\varepsilon j} \end{equation*}$

with $0\leq \beta _{\varepsilon j}\leq 1$. $\beta _{\varepsilon j}$ denoting the sensor failure coefficient.

$\mathit{Remark\ 1:}$ For the lower and upper bounds $\underline{\beta }_{\varepsilon j}$, $\bar{ \beta}_{\varepsilon j}$, the details can be consulted from [23], [40].

Then, one can obtain

 $$$\tilde{x}(t)=\beta _{\varepsilon }x(t)$$$ (3)

where

 $\begin{equation*} \beta _{\varepsilon }=\text{diag}\{\beta _{\varepsilon _{1}}, \ldots , \beta _{\varepsilon l}\}. \end{equation*}$
D. Fuzzy State-Feedback Control

This subsection constructs a fuzzy controller for system (1) in the framework of T-S fuzzy model.

$\mathit{Control\ Rule\ i}$: IF $\phi _{1}(t)$ is $\mathcal{M}_{\theta }(\phi _{1}(t)),$ and $\phi _{2}(t)$ is $\mathcal{N}_{\theta }(\phi _{2}(t))$, THEN

 $\begin{equation*} u(t)=\mathcal{K}_{i}\tilde{x}(t), \text{ }i=1, \ldots , 4. \end{equation*}$

The overall fuzzy controller is shown as follows,

 $$$u(t)=\underset{i=1}{\overset{4}{\sum\limits }}\omega _{i}\mathcal{K}_{i}\tilde{x} (t). \label{controller}$$$ (4)

Based on (2), (3) and (4), the closed-loop system can be obtained,

 $\begin{eqnarray} \dot{x}(t) &\hspace{-0.2cm}=&\hspace{-0.2cm}\underset{i=1}{\overset{4}{\sum }}\underset{j=1}{\overset{4}{ \sum }}\omega _{i}\omega _{j}\left[ \mathcal{\bar{A}}_{ij}x(t)+\mathcal{\bar{ B}}_{ij}w(t)\right] \notag \\ z_{1}(t) &\hspace{-0.2cm}=&\hspace{-0.2cm}\underset{i=1}{\overset{4}{\sum }}\underset{j=1}{\overset{4}{ \sum }}\omega _{i}\omega _{j}\mathcal{\bar{C}}_{ij}x(t) \label{close loop} \\ z_{2}(t) &\hspace{-0.2cm}=&\hspace{-0.2cm}\underset{i=1}{\overset{4}{\sum }}\omega _{i}\mathcal{C} _{2i}x(t) \notag \end{eqnarray}$ (5)

where

 $\begin{eqnarray*} \mathcal{\bar{A}}_{ij} &\hspace{-0.2cm}=&\hspace{-0.2cm}\mathcal{A}_{i}+\mathcal{B}_{i}\mathcal{K} _{j}\beta _{\varepsilon }, \text{ }\mathcal{\bar{B}}_{ij}=\mathcal{B}_{1i} \\ \mathcal{\bar{C}}_{ij} &\hspace{-0.2cm}=&\hspace{-0.2cm}\mathcal{C}_{1i}+D_{1i}\mathcal{K}_{j}\beta _{\varepsilon }. \end{eqnarray*}$
E. Control Objectives

In the process of designing an active suspension system controller, the ride comfort is the first factor which should be considered. According research of body acceleration, the frequency between 4 Hz-8 Hz is the most sensitive range for human body. Therefore, it is necessary to minimize the the transfer function from disturbance $w(t)$ to the controlled output $z_{1}(t)$ to improve the drive comfort. Denote the transfer function from $w(t)$ to $z_{1}(t)$ as $\Psi (j\sigma )$. Thus, the finite frequency ${H_{\infty }}$ control problem is to propose a fuzzy control scheme such that the following inequality holds for all nonzero $w(t)\in \mathcal{L}_{2}[0, \infty )$,

 $$$\underset{\bar{\sigma}_{1}\leq \sigma \leq \bar{\sigma}_{2}}{\sup } \left\Vert \Psi(j\sigma )\right\Vert _{\infty }<\gamma \label{performance}$$$ (6)

where $\gamma$ means a predefined positive constant, and define the upper and lower bounds of the concerned frequency as $\bar{\sigma}_{1}$ and $\bar{\sigma}_{2}$, respectively. Meanwhile, the following three constrained requirements should be guaranteed:

1) In order to improve drive stability, the dynamic load is less than static load

 $$$\ k_{t}(z_{u}(t)-z_{r}(t))<(m_{s}+m_{u})g. \label{limit 1}$$$ (7)

2) Considering the limitation of vehicle mechanical structure, the suspension deflection is allowed to change in a specified range, that is

 $$$\left\vert z_{s}(t)-z_{u}(t)\right\vert \leq z_{\max }. \label{limit 11}$$$ (8)

3) Considering the limitation of vehicle engine power, there exists output saturation in the actuator. Thus, the output force must be restricted within

 $$$\left\vert u(t)\right\vert \leq u_{\max }. \label{limit 2}$$$ (9)
Ⅲ. MAIN RESULTS

In this section, sufficient conditions are provided to guarantee that the closed-loop system (5) is asymptotically stable and satisfies the desired performance requirements.

$\mathit{Theorem\ 1:}$ For the given scalars $\gamma ,$ $\eta ,$ $\delta$ and control gain $\mathcal{K}_{i},$ provided that there exist symmetric matrixes $\mathcal{P}$, $\mathcal{P}_{1}>0,$ $Q>0$ and general matrix $\mathcal{F}$, such that the following conditions hold for $i,$ $j=1, \ldots , 4,$

 $\left[ {\begin{array}{*{20}{c}} {{\Omega _{ij}}}&{{\Phi _{ij}}}\\ \star &{\Lambda \ } \end{array}\ } \right] < 0$ (10)
 $\left[ {\begin{array}{*{20}{c}} {{\Gamma _{ij}}}&{{\Xi _{ij}}}\\ \star &{\Psi \ } \end{array}\ } \right] < 0$ (11)
 $\left[ {\begin{array}{*{20}{c}} { - {\cal I}}&{\sqrt \delta {{\cal K}_i}{\beta _\varepsilon }}\\ \star &{ - {u_{{{\max }^2}}}{{\cal P}_1}\ } \end{array}\ } \right] < 0$ (12)
 $\left[ {\begin{array}{*{20}{c}} { - {\cal I}}&{\sqrt \delta {{\{ {{\cal C}_{2i}}\} }_\theta }}\\ \star &{ - {{\cal P}_1}\ } \end{array}\ } \right] < 0, \;\;\;\theta = 1, 2$ (13)

where

 $\begin{array}{l} {\Phi _{ij}} = \left[ {\begin{array}{*{20}{c}} {{{\cal F}^T}{{\bar {\cal B}}_{ij}}}&{{{\cal F}^T}}\\ 0&0 \end{array}} \right]\\ \Lambda = \left[ {\begin{array}{*{20}{c}} { - \eta {\cal I}}&0\\ \star &{ - {{\cal P}_1}} \end{array}} \right]\\ {\Xi _{ij}}{\rm{ }} = \left[ {\begin{array}{*{20}{c}} 0&0\\ {{{\cal F}^T}{{\bar {\cal B}}_{ij}}}&{\bar {\cal C}_{ij}^T} \end{array}} \right]{\rm{ }}\\ \Psi {\rm{ }} = {\rm{ }}\left[ {\begin{array}{*{20}{c}} { - {\gamma ^2}{\cal I}}&0\\ 0&{ - {\cal I}} \end{array}} \right]{\rm{ }}\\ {\Omega _{ij}}{\rm{ }} = {\rm{ }}\left[ {\begin{array}{*{20}{c}} { - {{[{\cal F}]}_s}}&{{{\cal F}^T}{{\bar {\cal A}}_{ij}} + {{\cal P}_1}}\\ \star &{ - {{\cal P}_1}} \end{array}} \right] \end{array}$ (14)
 ${\Gamma _{ij}}{\rm{ }} = {\rm{ }}\left[ {\begin{array}{*{20}{c}} { - {\cal Q}}&{{\cal P} + j{{\bar \sigma }_c}{\cal Q} - {\cal F}}\\ \star &{ - {{\bar \sigma }_1}{{\bar \sigma }_2}{\cal Q} - {{[{{\cal F}^T}{{\bar {\cal A}}_{ij}}]}_s}} \end{array}} \right]$ (15)

and $\bar{\sigma}_{c}=(\bar{\sigma}_{1}+\bar{\sigma}_{2})/2$ is a known scalar. Then, the system (5) is asymptotically stable and control objectives (6)-(9) hold with the disturbance under the range $w_{\max }=(\delta -\mathcal{V}(0))/\eta .$

$\mathit{Proof:}$ Consider the following Lyapunov function

 $\begin{equation*} \mathcal{V}(t)=x^{T}(t)\mathcal{P}_{1}x(t) \end{equation*}$

where $\mathcal{P}_{1}$ is a positive definite symmetric matrix. Its derivative can be obtained as follows,

 $\begin{eqnarray} \mathcal{\dot{V}}(t) &\hspace{-0.2cm}=&\hspace{-0.2cm}\dot{x}^{T}(t)\mathcal{P}_{1}x(t)+x^{T}(t)\mathcal{P} _{1}\dot{x}(t) \notag \\ &\hspace{-0.2cm}\leq &\hspace{-0.2cm}\overset{4}{\underset{i=1}{\sum }}\overset{4}{\underset{j=1}{\sum }} \omega _{i}\omega _{j}[(\mathcal{\bar{A}}_{ij}x(t))^{T}\mathcal{P} _{1}x(t)\!\!+\!\!x^{T}(t)\mathcal{P}_{1} \!\!\times\!\! (\mathcal{\bar{A}}_{ij}x(t))] \notag \\ &\hspace{-0.2cm}=&\hspace{-0.2cm}\overset{4}{\underset{i=1}{\sum }}\overset{4}{\underset{j=1}{\sum }} \omega _{i}\omega _{j}[x^{T}(t)(\mathcal{\bar{A}}_{ij}\mathcal{P}_{1}+ \mathcal{P}_{1}\mathcal{\bar{A}}_{ij}^{T})x(t)]. \label{jianleyoujia} \end{eqnarray}$ (16)

By employing the Schur complement, inequality (10) can be converted into

 $$$\left[ \begin{array}{cc} \frac{1}{\eta }\mathcal{F}^{T}\mathcal{\bar{B}}_{ij}\mathcal{\bar{B}} _{ij}^{T}\mathcal{F}+\mathcal{F}^{T}\mathcal{P}_{1}^{-1}\mathcal{F}-\left[ \mathcal{F}\right] _{s}&\mathcal{F}^{T}\mathcal{\bar{A}}_{ij}+\mathcal{P} _{1} \\ \star&-\mathcal{P}_{1} \end{array} \right] <0. \label{1}$$$ (17)

Defining matrix $\mathcal{W}^{-1}=\mathcal{F},$ and utilizing the congruence transformation on (17) by diag$\{\mathcal{F}^{-1}, \mathcal{P} _{1}^{-1}\}$, it can be found that

 $\begin{equation*} \left[ \begin{array}{cc} \frac{1}{\eta }\mathcal{\bar{B}}_{ij}\mathcal{\bar{B}}_{ij}^{T}+\mathcal{P} _{1}^{-1}-\left[ \mathcal{W}\right] _{s}&\mathcal{\bar{A}}_{ij}\mathcal{P} _{1}^{-1}+\mathcal{W}^{T} \\ \star&-\mathcal{P}_{1}^{-1} \end{array} \right] <0. \end{equation*}$

Letting

 $\begin{equation*} \Upsilon =\frac{1}{\eta }\mathcal{\bar{B}}_{ij}\mathcal{\bar{B}}_{ij}^{T}, \ \mathcal{\vartheta }=\mathcal{P}_{1}^{-1}\mathcal{\bar{A}}_{ij}^{T} \end{equation*}$

by adopting Lemma 3, it is easy to find that the following inequality holds,

 $\begin{equation*} \mathcal{P}_{1}^{-1}\mathcal{\bar{A}}_{ij}+\mathcal{\bar{A}}_{ij}^{T} \mathcal{P}_{1}^{-1}+\frac{1}{\eta }\mathcal{\bar{B}}_{ij}\mathcal{\bar{B}} _{ij}^{T}<0 \end{equation*}$

then

 $$$\mathcal{\bar{A}}_{ij}\mathcal{P}_{1}+\mathcal{P}_{1}\mathcal{\bar{A}} _{ij}^{T}+\frac{1}{\eta }\mathcal{P}_{1}\mathcal{\bar{B}}_{ij}\mathcal{\bar{B }}_{ij}^{T}\mathcal{P}_{1}<0 \label{according}$$$ (18)

which implies

 $$$\mathcal{\bar{A}}_{ij}\mathcal{P}_{1}+\mathcal{P}_{1}\mathcal{\bar{A}} _{ij}^{T}<0. \label{proofend}$$$ (19)

According to (16) and (19), we can obtain that $\mathcal{\dot{V}}(t)<0$. Accordingly, the closed-loop system (5) with $w(t)=0$ is asymptotically stable.

Next, the proof of finite frequency ${H}_{\infty }$ performance is shown.

According to Schur complement, (11) can be rewritten as

 $$$\mathcal{J}\Xi \mathcal{J}^{T}+{H}\Pi {H}^{T}+\left[ \Gamma \mathcal{F}\Lambda \right] _{s}<0 \label{111}$$$ (20)

where

 $\begin{eqnarray*} \mathcal{J} &\hspace{-0.2cm}=&\hspace{-0.2cm}\left[ \begin{array}{cc} \mathcal{I}&0 \\ 0&\mathcal{I} \\ 0&0 \end{array} \right] \\ \Xi &\hspace{-0.2cm}=&\hspace{-0.2cm}\left[ \begin{array}{cc} -\mathcal{Q}&\mathcal{P}+j\bar{\sigma}_{c}\mathcal{Q} \\ \ast&-\bar{\sigma}_{1}\bar{\sigma}_{2}\mathcal{Q} \end{array} \right] \\ \Pi &\hspace{-0.2cm}=&\hspace{-0.2cm}\left[ \begin{array}{cc} \mathcal{I}&0 \\ \ast&-\gamma ^{2}\mathcal{I} \end{array} \right] \\ H &\hspace{-0.2cm}=&\hspace{-0.2cm}\left[ \begin{array}{ccc} 0&\mathcal{\bar{C}}_{ij}&0 \\ 0&0&\mathcal{I} \end{array} \right] ^{T} \\ \Gamma &\hspace{-0.2cm}=&\hspace{-0.2cm}\left[ \begin{array}{ccc} -\mathcal{I}&\mathcal{\bar{A}}_{ij}&\mathcal{\bar{B}}_{ij} \end{array} \right] ^{T} \\ \Lambda &\hspace{-0.2cm}=&\hspace{-0.2cm}\left[ \begin{array}{ccc} 0&\mathcal{I}&0 \end{array} \right]. \end{eqnarray*}$

Based on Lemma 2, through (20), the following two inequalities hold,

 $\begin{eqnarray} \mathcal{W}^{T}(\mathcal{J}\Xi \mathcal{J}^{T}+{H}\Pi {H} ^{T})\mathcal{W} &\hspace{-0.2cm}<&\hspace{-0.2cm}0 \notag \\ \mathcal{U}(\mathcal{J}\Xi \mathcal{J}^{T}+{H}\Pi {H}^{T}) \mathcal{U}^{T} &\hspace{-0.2cm}<&\hspace{-0.2cm}0 \label{second} \end{eqnarray}$ (21)

where

 $\begin{eqnarray*} \mathcal{W} &\hspace{-0.2cm}=&\hspace{-0.2cm}\left[ \begin{array}{ccc} \mathcal{I}&0&0 \\ 0&0&\mathcal{I} \end{array} \right] ^{T} \\ \mathcal{U} &\hspace{-0.2cm}=&\hspace{-0.2cm}\left[ \begin{array}{ccc} \mathcal{\bar{A}}_{ij}^{T}&\mathcal{I}&0 \\[2mm] \mathcal{\bar{B}}_{ij}^{T}&0&\mathcal{I} \end{array} \right]. \end{eqnarray*}$

Based on (21), the following inequality can be obtained,

 $\begin{equation*} \left[\!\! \begin{array}{cc} \mathcal{\bar{A}}_{ij}&\mathcal{\bar{B}}_{ij} \\ \mathcal{I}&0 \end{array} \!\!\right] ^{T}\Xi \left[\!\! \begin{array}{cc} \mathcal{\bar{A}}_{ij}&\mathcal{\bar{B}}_{ij} \\ \mathcal{I}&0 \end{array} \!\!\right] +\left[\!\! \begin{array}{cc} \mathcal{\bar{C}}_{ij}&0 \\ 0&\mathcal{I} \end{array} \!\!\right] ^{T}\Pi \left[\!\! \begin{array}{cc} \mathcal{\bar{C}}_{ij}&0 \\ 0&\mathcal{I} \end{array} \!\!\right] <0. \end{equation*}$

Thus, the following inequality holds,

 $\begin{equation*} \left[ \begin{array}{cc} \mathcal{\bar{A}}_{ij}&\mathcal{\bar{B}}_{ij} \\ \mathcal{I}&0 \end{array} \right] ^{T}\Xi \left[ \begin{array}{cc} \mathcal{\bar{A}}_{ij}&\mathcal{\bar{B}}_{ij} \\ \mathcal{I}&0 \end{array} \right] +\left[ \begin{array}{cc} 0&0 \\ \star&-\gamma ^{2}\mathcal{I} \end{array} \right]\\ \ \ \ \ \ \ \ \ \ \ \ \ \ \ \ \ \ \ \ \ \ \ \ +\left[ \begin{array}{cc} \mathcal{\bar{C}}_{ij}&0 \end{array} \right] ^{T}\left[ \begin{array}{cc} \mathcal{\bar{C}}_{ij}&0 \end{array} \right] <0. \label{QQ} \end{equation*}$ (22)

Utilizing Schur complement, (22) can be transformed into the following form,

 $$$\left[ \begin{array}{cc} \Gamma \left[ \mathcal{P}, \mathcal{Q}, \mathcal{\bar{C}}, \mathcal{\bar{D}} \right]&\left[ \begin{array}{cc} \mathcal{\bar{C}}_{ij}&0 \end{array} \right] ^{T} \\ \star&-\mathcal{I} \end{array} \right] <0. \label{equivalent}$$$ (23)

According to Lemma 1, (23) is equivalent to the expression in (6).

Computing the derivative of the Lyapunov function yields

 $\begin{eqnarray*} \mathcal{\dot{V}}(t) &\hspace{-0.2cm}=&\hspace{-0.2cm}2x^{T}(t)\mathcal{P}_{1}\dot{x}(t) \\ &\hspace{-0.2cm}\leq &\hspace{-0.2cm}\underset{i=1}{\overset{4}{\sum }}\underset{j=1}{\overset{4}{\sum }} \omega _{i}\omega _{j}[2x^{T}(t)\mathcal{P}_{1}\mathcal{\bar{A}} _{ij}x(t)+2x^{T}(t)\mathcal{P}_{1}\mathcal{\bar{B}}_{ij}w(t)]. \end{eqnarray*}$

Due to

 $2x^{T}(t)\mathcal{P}_{1}\mathcal{\bar{B}}_{ij}w(t)\leq$
 $$$\ \ \ \ \frac{1}{\eta }x^{T}(t)\mathcal{P}_{1}\mathcal{\bar{B}}_{ij} \mathcal{\bar{B}}_{ij}^{T}\mathcal{P}_{1}^{T}x(t)+\eta w^{T}(t)w(t), \forall \eta >0 \label{fangsuo}$$$ (24)

by employing (18) and (24), the following inequality holds,

 $$$\mathcal{\dot{V}}(t)\leq \eta w^{T}(t)w(t). \label{integrate}$$$ (25)

Integrating (25) on both sides from $0$ to $t,$ it can be obtained that

 $\begin{equation*} \mathcal{V}(t)-\mathcal{V}(0)\leq \eta \int_{0}^{t}w^{T}(t)w(t)dt\leq \eta \left\Vert w(t)\right\Vert _{2}^{2}=\eta w_{\max }. \end{equation*}$

Therefore, the following inequality can be obtained,

 $\begin{equation*} x^{T}(t)\mathcal{P}_{1}x(t)\leq \mathcal{V}(0)+\eta w_{\max }=\delta. \end{equation*}$

Consider the control input

 $\begin{eqnarray*} \underset{t\geq 0}{\max }\left\vert u(t)\right\vert ^{2} &\hspace{-0.2cm}\leq&\hspace{-0.2cm}\underset{ t\geq 0}{\max }\left\Vert \underset{i=1}{\overset{4}{\sum }}\omega _{i}[x^{T}(t)\beta _{\varepsilon }^{T}\mathcal{K}_{i}^{T}\mathcal{K} _{i}\beta _{\varepsilon }x(t)]\right\Vert _{2} \\ &\hspace{-0.2cm}=&\hspace{-0.2cm}\underset{t\geq 0}{\max }\left\Vert \underset{i=1}{\overset{4}{\sum }} \omega _{i}\{x^{T}(t)\mathcal{P}_{1}^{\frac{1}{2}}\mathcal{P}_{1}^{-\frac{1}{ 2}}\beta _{\varepsilon }^{T}\mathcal{K}_{i}^{T}\right. \\ &&\left. \times \mathcal{K}_{i}\beta _{\varepsilon }\mathcal{P}_{1}^{-\frac{1 }{2}}\mathcal{P}_{1}^{\frac{1}{2}}x(t)\}\right\Vert _{2} \\ &\hspace{-0.2cm}\leq &\hspace{-0.2cm}\delta \lambda _{\max }\{\underset{i=1}{\overset{4}{\sum }}\omega _{i}[\mathcal{P}_{1}^{-\frac{1}{2}}\beta _{\varepsilon }^{T}\mathcal{K} _{i}^{T}\mathcal{K}_{i}\beta _{\varepsilon }\mathcal{P}_{1}^{-\frac{1}{2} }]\} \end{eqnarray*}$

and the constrained output

 $\begin{eqnarray*} \underset{t\geq 0}{\max }\left\vert \{z_{2}(t)\}_{\theta }\right\vert ^{2} &\hspace{-0.2cm}\leq &\hspace{-0.2cm}\underset{t\geq 0}{\max }\left\Vert \underset{j=1}{\overset{4}{\sum }} \omega _{i}[x^{T}(t)\{\mathcal{C}_{2i}^{T}\}_{\theta }\{\mathcal{C} _{2i}\}_{\theta }x(t)]\right\Vert _{2} \\ &\hspace{-0.2cm}=&\hspace{-0.2cm}\underset{t\geq 0}{\max }\left\Vert \underset{i=1}{\overset{4}{\sum }} \omega _{i}[x^{T}(t)\mathcal{P}_{1}^{\frac{1}{2}}\mathcal{P}_{1}^{-\frac{1}{2 }}\{\mathcal{C}_{2i}^{T}\}_{\theta }\right. \\ &&\left. \times \{\mathcal{C}_{2i}\}_{\theta }\mathcal{P}_{1}^{-\frac{1}{2}} \mathcal{P}_{1}^{\frac{1}{2}}x(t)]\right\Vert _{2}\\ &\hspace{-0.2cm}\leq&\hspace{-0.2cm}\delta \lambda _{\max }\{\underset{i=1}{\overset{4}{\sum }}\omega _{i} \mathcal{P}_{1}^{-\frac{1}{2}}\{\mathcal{C}_{2i}^{T}\}_{\theta }\{\mathcal{C} _{2i}\}_{\theta }\mathcal{P}_{1}^{-\frac{1}{2}}\}\\ &&& \theta =1, 2 \end{eqnarray*}$

where $\lambda _{\max }\{\cdot \}$ is the maximum eigenvalue. Then, the constrained requirements (7), (8) and (9) are guaranteed if the following two inequalities hold,

 $$$\delta \mathcal{P}_{1}^{-\frac{1}{2}}\beta _{\varepsilon }^{T}\mathcal{K} _{i}^{T}\mathcal{K}_{i}\beta _{\varepsilon }\mathcal{P}_{1}^{-\frac{1}{2} } $ $$\delta \mathcal{P}_{1}^{-\frac{1}{2}}\{\mathcal{C}_{2i}^{T}\}_{\theta }\{ \mathcal{C}_{2i}\}_{\theta }\mathcal{P}_{1}^{-\frac{1}{2}}<\mathcal{I}, \text{ }\theta =1, 2. \label{output2}$$ $(27) Using the Schur complement, (12) and (13) are equivalent to (26) and (27), respectively. Note that in (14) and (15), the term$\mathcal{F}^{T}\mathcal{ \bar{A}}_{ij}$contains coupling term$\mathcal{F}^{T}\mathcal{B}_{i} \mathcal{K}_{j}$, and it cannot be directly solved by MATLAB LMI tool. Hence, the synthesis conditions are proposed in the following content.$\mathit{Theorem\ 2:}$For the given constants$\gamma , \eta , \delta , $and$ \mathcal{\hat{{K}}}_{i}$, provided that there exist symmetric matrixes$ \mathcal{\hat{P}}$,$\mathcal{\hat{P}}_{1}>0, \mathcal{\hat{Q}}>0$and general matrix$\mathcal{\hat{F}}$such that the following inequalities hold for$i, j=1, \ldots , 4, $$ \left[ {\begin{array}{*{20}{c}} {{{\hat \Omega }_{ij}}}&{{{\hat \Phi }_{ij}}}\\ \star &{\hat \Lambda } \end{array}} \right] < 0 $(28) $ \left[ {\begin{array}{*{20}{c}} {{{\hat \Gamma }_{ij}}}&{{{\hat \Xi }_{ij}}}\\ \star &\Psi \end{array}} \right] < 0 $(29) $ \left[ {\begin{array}{*{20}{c}} { - {\cal I}}&{\sqrt \delta {\beta _\varepsilon }{{\hat {\cal K}}_j}}\\ \star &{ - {u_{{{\max }^2}}}{{\hat {\cal P}}_1}} \end{array}} \right] < 0 $(30) $ \left[ {\begin{array}{*{20}{c}} { - {\cal I}}&{\sqrt \delta {{\{ {{\cal C}_{2i}}\} }_\theta }\hat {\cal F}}\\ \star &{ - {{\hat {\cal P}}_1}} \end{array}} \right] < 0, \;\;\theta = 1, 2 $(31) where $ \begin{eqnarray*} \hat{\Phi}_{ij} &\hspace{-0.2cm}=&\hspace{-0.2cm}\left[ \begin{array}{cc} \mathcal{B}_{1i}&\mathcal{\hat{F}} \\ 0&0 \end{array} \right] \\ \hat{\Lambda} &\hspace{-0.2cm}=&\hspace{-0.2cm}\left[ \begin{array}{cc} -\eta \mathcal{I}&0 \\ \star &-\mathcal{\hat{P}}_{1} \end{array} \right] \\ \hat{\Xi}_{ij} &\hspace{-0.2cm}=&\hspace{-0.2cm}\left[ \begin{array}{cc} 0&0 \\ \mathcal{B}_{1i}&\mathcal{\hat{F}}^{T}\mathcal{C}_{1i}^{T}+\mathcal{\hat{K} }_{j}^{T}\mathcal{D}_{1i}^{T} \end{array} \right] \\ \hat{\Omega}_{ij} &\hspace{-0.2cm}=&\hspace{-0.2cm}\left[ \begin{array}{cc} -[\mathcal{\hat{F}}]_{s}&\mathcal{A}_{i}\mathcal{\hat{F}}+\mathcal{B}_{i} \mathcal{\hat{K}}_{j}+\mathcal{\hat{P}}_{1} \\ \star &-\mathcal{\hat{P}}_{1} \end{array} \right] \\ \hat{\Gamma}_{ij} &\hspace{-0.2cm}=&\hspace{-0.2cm}\left[ \begin{array}{cc} -\mathcal{\hat{Q}}&\mathcal{\bar{P}}+j\bar{\sigma}_{c}\mathcal{\hat{Q}}- \mathcal{\hat{F}}^{T} \\ \star &-\bar{\sigma}_{1}\bar{\sigma}_{2}\mathcal{\hat{Q}}+[\mathcal{A}_{i} \mathcal{\hat{F}}+\mathcal{B}_{i}\mathcal{\hat{K}}_{j}]_{s} \end{array} \right] \end{eqnarray*} $and$\bar{\sigma}_{c}=(\bar{\sigma}_{1}+\bar{\sigma}_{2})/2$is an available scalar. Then, the closed-loop system (5) is asymptotically stable and control objectives (6)-(9) hold with the disturbance under the range$w_{\max }=(\delta -\mathcal{V}(0))/\eta.$Moreover, the control gain$\mathcal{K}_{j}, j=1, \ldots , 4$is given by $ \begin{equation*} \mathcal{K}_{j}=\hat{\mathcal{K}_{j}}\mathcal{\hat{F}}^{-1}\beta _{\varepsilon }^{-1}. \end{equation*} \mathit{Proof:}$Define$\mathcal{J}_{1}=\text{diag}\{\Theta^{-1}, \Theta^{-1}, \mathcal{I} , \Theta^{-1}\}, \mathcal{J}_{2}=\text{diag}\{\Theta^{-1}, \Theta^{-1}, \mathcal{I}, \mathcal{I}\}, \mathcal{J}_{3}=\text{diag}\{\mathcal{I} , \Theta^{-1}\}.$Pre- and post-multiply$\mathcal{J}_{1}^{T}, \mathcal{J} _{2}^{T}, \mathcal{J}_{3}^{T}$by$\mathcal{J}_{3}^{T}$and the transpositions of (10)-(19), respectively. Define $ \begin{eqnarray*} \mathcal{\hat{Q}} &\hspace{-0.2cm}=&\hspace{-0.2cm}\Theta^{-T}\mathcal{Q}\Theta^{-1}, \text{ }\mathcal{\hat{ P}}=\Theta^{-T}\mathcal{P}\Theta^{-1}\\ \mathcal{\hat{P}}_{1} &\hspace{-0.2cm}=&\hspace{-0.2cm}\Theta^{-T}\mathcal{P}_{1}\Theta^{-1}, \text{ } \mathcal{\hat{K}}_{j}=\mathcal{K}_{j}\beta _{\varepsilon }\Theta^{-1} \\ \mathcal{\hat{F}} &\hspace{-0.2cm}=&\hspace{-0.2cm}\Theta^{-1}. \end{eqnarray*} $Thus, (28)-(31) can be obtained.$\mathit{Remark\ 2:}$It should be pointed out that the work [14], [17], [38], [39] failed to address the fuzzy control problem of active suspension systems in finite frequency domain. Until now, there are few relevant results. Combining T-S fuzzy model and finite frequency domain approach, Theorem 2 gives the sufficient conditions to design a state-feedback controller for active suspension systems, and the performance of the active suspension system can be improved effectively.$\mathit{Remark\ 3:}$Obviously, the inequalities in (28)-(31) cannot be solved directly because there exist complex variables in (29). Inspired by the results in [50], the inequality with complex variables can be converted into a real variable with distensible dimension. This implies $ \begin{equation*} \Phi _{1}+j\Phi _{2}<0 \end{equation*} $is equivalent to $ \begin{equation*} \left[ \begin{array}{cc} \Phi _{1}&\Phi _{2} \\ -\Phi _{2}&\Phi _{1} \end{array} \right] <0 \end{equation*} $which means that (29) can be addressed by the above approach. Ⅳ. SIMULATION RESULTS In this section, the proposed fuzzy${H}_{\infty}$control strategy in finite frequency domain is applied to a quarter-vehicle model to demonstrate its validity. Consider the quarter-vehicle model shown in Fig. 1. Its parameters are presented in Table Ⅰ. Assume sprung mass$m_{s}$is defined as [$780$kg,$1020$kg] and unsprung mass is defined as [$45$kg,$55$kg]. Given the scalars$\bar{\sigma}_{1}=4$Hz (8$\pi $rad/s),$\bar{\sigma}_{2}=8$Hz (16$\pi $rad/s),$\delta =1, \eta =1\times 10^{3}, z_{\max }=0.1$m,$ u_{\max }=2000$N$.$The failure matrix is defined as follows: $ \begin{equation*} \beta _{\varepsilon }=\text{diag}\{0.9, 0.8, 0.6, 0.9\}. \end{equation*} $Table 1 QUARTER-VEHICLE MODEL PARAMETERS By solving LMIs (28)-(31), in the case of optimal$ \gamma (\gamma _{\min }= 3.9984), $the control gains can be obtained as $ \begin{eqnarray*} \mathcal{K}_{1} &\hspace{-0.2cm}=&\hspace{-0.2cm}10^{4}\times \left[ \begin{array}{cccc} -0.0413&-0.3948&-2.0088&-0.1128 \end{array} \right] \\ \mathcal{K}_{2} &\hspace{-0.2cm}=&\hspace{-0.2cm}10^{4}\times \left[ \begin{array}{cccc} 0.4812&-4.0402&-1.6482&-0.1222 \end{array} \right] \\ \mathcal{K}_{3} &\hspace{-0.2cm}=&\hspace{-0.2cm}10^{4}\times \left[ \begin{array}{cccc} 0.0717&-0.2190&-1.9249&-0.1164 \end{array} \right] \\ \mathcal{K}_{4} &\hspace{-0.2cm}=&\hspace{-0.2cm}10^{4}\times \left[ \begin{array}{cccc} 0.6196&-4.1277&-1.5524&-0.1267 \end{array} \right]. \end{eqnarray*} $After obtaining control gains, we illustrate the effectiveness of the control method proposed in this paper. Fig. 3 describes the responses of body vertical acceleration in the frequency domain in the open and closed-loop system. Obviously, compared with the frequency response in the open-loop system, the counterpart in the closed-loop system (5) under control has the minimum value of${H}_{\infty }$norm between the frequency range 4-8 Hz, which clearly illustrates that ride comfort level has been improved.  Download: larger image Fig. 3 Responses of body vertical acceleration in frequency domain. In view of the evaluation of active suspension characteristics with respect to the three performance requirements (7), (8) and (9), the road disturbance signal is given as follows, $ \begin{equation*} w(t)=\left\{ \begin{array}{c} \mathcal{A}\sin (-\pi ft), \ \ \ \text{if 0}\leq t\leq \mathcal{T}\text{ } \\ 0, \quad \quad \quad \quad \text{otherwise } \end{array} \right. \end{equation*} $with$\mathcal{A}$,$f$, and$\mathcal{T}$denoting amplitude, frequency and period, respectively. Define$\mathcal{A}=0.1$m,$f=5$Hz (in the frequency range$4$Hz-$8$Hz) and$\mathcal{T}=0.2$s ($\mathcal{T}=1/f$). Fig. 4 shows the body vertical acceleration for active suspension systems, and it can be obtained that the body acceleration under control in finite frequency is less than that of the open-loop system. Fig. 5 demonstrates the ratio of suspension deflection where the maximum limitation is less than 1, which satisfies the performance constrained requirements. Fig. 6 plots the ratio of dynamic tyre load and static load, which shows that the ratio is strictly less than 1. Fig. 7 shows that the actuator force is less than the$u_{\max }=2000$N. In order to highlight the advantage of finite frequency control strategy, we give comparisons of vertical body acceleration between the entire frequency range and the finite frequency that are presented in Fig. 8. It can be observed from Fig. 8, vertical body acceleration under finite frequency control is more stable than entire frequency control, which demonstrates the effectiveness of the proposed strategy.  Download: larger image Fig. 4 The body acceleration for active suspension system.  Download: larger image Fig. 5 The ratio of suspension deflection and the maximum limitation.  Download: larger image Fig. 6 The ratio of dynamic tyre load and static load.  Download: larger image Fig. 7 The actuator force.  Download: larger image Fig. 8 The time-domain response of body acceleration. According to these simulation results, it is obvious that the finite frequency fuzzy${H}_{\infty}$control design algorithm not only guarantees the stability of active suspension systems, but also improves drive comfort level and achieves suspension constrained requirements effectively. Ⅴ. CONCLUSION This paper has studied the fuzzy${H}_{\infty}$control problem for uncertain active suspension systems subject to sensor failure in the finite frequency domain. Using T-S fuzzy model, active suspension systems with uncertainty have been described as a fuzzy model. The${H}_{\infty}$performance index has been adopted to measure drive comfort level. Based on the KYP lemma, the optimized objective, that is, to minimize the${H}_{\infty}\$ norm from disturbance to controlled output has been achieved. At the same time, three suspension constrained requirements have also been ensured. Moreover, sufficient conditions have been derived to design the fuzzy controller that guarantees the desired performance of the active suspension systems. Finally, simulation results have been presented to validate the effectiveness of the proposed control method.

REFERENCES