## Journal of the Brazilian Society of Mechanical Sciences and Engineering

##
*Print version* ISSN 1678-5878*On-line version* ISSN 1806-3691

### J. Braz. Soc. Mech. Sci. & Eng. vol.26 no.4 Rio de Janeiro Oct./Dec. 2004

#### https://doi.org/10.1590/S1678-58782004000400008

**TECHNICAL PAPERS**

**Robust control to parametric uncertainties in smart structures using linear matrix inequalities **

**Samuel da Silva ^{I}; V. Lopes Júnior^{I}; E. Assunção^{II}**

^{I}Universidade Estadual Paulista – UNESP; Mechanical Engineering Department; Av. Brasil, n.º 56, Centro; 15385-000 Ilha Solteira, SP. Brazil; samuel@dem.feis.unesp.br; vicente@dem.feis.unesp.br

^{II}Universidade Estadual Paulista – UNESP; Electrical Engineering Department; Av. Brasil, n.º 56, Centro; 15385-000 Ilha Solteira, SP. Brazil; edvaldo@dee.feis.unesp.br

**ABSTRACT**

The study of algorithms for active vibrations control in flexible structures became an area of enormous interest, mainly due to the countless demands of an optimal performance of mechanical systems as aircraft and aerospace structures. Smart structures, formed by a structure base, coupled with piezoelectric actuators and sensor are capable to guarantee the conditions demanded through the application of several types of controllers. This article shows some steps that should be followed in the design of a smart structure. It is discussed: the optimal placement of actuators, the model reduction and the controller design through techniques involving linear matrix inequalities (LMI). It is considered as constraints in LMI: the decay rate, voltage input limitation in the actuators and bounded output peak (output energy). Two controllers robust to parametric variation are designed: the first one considers the actuator in non-optimal location and the second one the actuator is put in an optimal placement. The performance are compared and discussed. The simulations to illustrate the methodology are made with a cantilever beam with bonded piezoelectric actuators.

**Keywords:** Robust control, LMI, optimal placement of piezoelectric

**Introduction**

Nowadays it is needed an optimal performance in structural systems in order to obtain lighter and stronger structures, static and dynamic stability and reduction of vibrations caused by external sources (Anthony, 2000). It is possible to use modern techniques of active control associated with intelligent materials to execute these demands. These materials are composed by piezoelectric ceramic (PZT - *Lead Zirconate Titanate*), commonly used as distributed actuators, and piezoelectric plastic films (PVDF - *PolyVinyliDeno Floride*), highly indicated for distributed sensors (Clark et al., 1998).

The design process of such system encompasses three main phases: structural design; optimal placement of sensor/actuator (PVDF and PZT); and controller design. Consequently, for optimal design purposes, the structure, the sensor/actuator placement and the controller have to be considered simultaneously, (Gonçalves et al., 2002). This article addresses the last two phases. The purpose is aimed to develop an integrated controller design procedure for uncertainties parametric rejection, where the PZTs are bonded in optimal locations.

The location of sensor/actuator is an extremely important step and affects the signals for the controller. Several authors studied the problem of optimal placement of PZT in the active structural control using different methodologies. The techniques more mentioned in the literature use genetic algorithms (GA) in a procedure of discrete optimization (placement of PZT) and continuous optimization (controller). This technique can find good results, but not necessarily the optimal solution, (Silva and Lopes Jr., 2002). It happens because the objective function involves the controller design, then for each location candidate the controller must be synthesized and evaluated its performance. This technique has many citations in literature, as example, Simpson and Hansen (1996) that used a simple model of an interior aircraft to determine the optimal location of PZT. Furuya and Haftka (1993) found the optimal placement of 8 actuators in a structure with 1507 candidate positions.

Geromel (1989) presented a procedure of convex analysis and global optimization for actuator location using LMI. Oliveira and Geromel (2000) proposed a linear output feedback controller design with joint selection of sensor and actuator. The approach of the present article uses a different methodology, which was proposed by Panossian et al. (1998) in a practical application and described in details in Gawronski (1998). This proposal involves the computation of the H_{¥} norm systems as the objective function, and it is not necessary the controller design to evaluate the performance of the candidate location.

Many strategies have been used for control design. For example: Lopes Jr. et al. (2003) presented the control of a beam using pole allocation and classical techniques optimization. Liu and Zhang (2000) showed the control of vibrations in a space truss structure using independent modal space control (IMSC). There are many classical strategies that can be used when the mathematical model is available, for instance pole allocation and optimal control (LQR). However, if the model has uncertainties these methods are not indicated. There are many robust techniques well known in structural control literature, as for instance, Moreira et al. (2001) designed a reduced order H_{¥} controller for an intelligent structure satellite applications considering dynamic uncertainties requirements.

The objective of this work is to use a recent technique, LMI, to design a robust control considering parametric uncertainties. However, the methodology has forward application for any kind of uncertainties. LMI contributes to overcome many difficulties in control design. In the last decade, LMI has been used to solve many problems that until then was unfeasible through others methodologies, (Boyd et al. 1994).

The major advantage of LMI design is to enable specifications such as stability degree requirements, decay rate, input limitation in the actuators and output peak bounder. It is also possible to assume that the model parameters involve uncertainties. The LMI is a very useful tool for problems with constraints, where the parameters vary in a range of values. Once formulated in terms of LMI a problem can be solved efficiently by convex optimization algorithms, (Gahinet et al., 1995).

The main proposal of this article is to present a clear methodology for active vibration control with robust requirements. It is considered as constraint design: decay rate; quadratic stability; limited input and output; and robustness to parametric uncertainties. We considered linear system with polytopic uncertainty in a procedure that was first proposed by Geromel et al. (1991). In the following, a brief review of structural state-space model is presented and the strategy for actuator placement is shown. A LMI controller is discussed for vibration attenuation of some natural modes. Finally, a numerical application using a cantilever beam with bonded PZT is presented for illustration purpose.

**Nomenclature**

A = dynamic matrix

b = width of the beam

B = input matrix

C = output matrix

d = dielectric constant

e = reduction error

E = Young's modulus

G = transfer function

I = identity matrix

k = number of exogenous inputs

K = state-feedback gain

M = generated moment by pair of PZT

n = number of modes

N = number of states

p = number of uncertainties parameters

P = positive definited matrix

q = modal displacement

= modal velocity

r = number of outputs

R = number of candidate sensor locations

s = number of control inputs

S = number of candidate actuator locations

t = thickness of the beam

T = placement matrix

u = vector of controlled inputs

v = number of vertexes

V = voltage applied by pair of PZT

w = vector of disturbance inputs

x = state-space vector

y = vector of measured outputs

Greek Symbolsz

= modal damping

v= natural frequency

s= H: placement indexb

= bounded output energy

r= maximum value of amplitude on PZT

a= decay rate

µ= optimization variable relative to compute HW_{¥}norm

= convex space

Subscripts

m = relative to ith mode

r = relative to retained state (modes of nominal model)

t = relative to truncated states (modes of residual model)

b = relative to structure (beam)

p = relative to PZT

1 = relative to the disturbance input

2 = relative to the controlled input

**Structural State-Space Models**

A linear differential inclusion (LDI) system, in modal state-space form, considering the matrices with appropriate dimensions and assumed to be known is given by:

where V is a polytope that is described by a list of vertexes in a convex space.

The modal state-space realization is characterized by the block-diagonal dynamic matrix and the related input and output matrices, (Gawronski, 1998):

where i=1,2,...,n, *A _{mi}, B*

_{1mi},

*B*

_{2mi}and

*C*are 2x2, 2xk, 2xs and rx2 blocks, respectively. These blocks can be obtained in several different forms and also it is possible to convert in another realization through a linear transformation. One possible form to block

_{mi}*A*can be written by:

_{mi}(t)It is assumed that the natural frequencies vary equally in both, positive and negative, sides, so the natural frequencies corresponding to model obtained by finite element method (FEM) can be taken as nominal parameters. In this paper we considered state feedback and parametric variations only in the low frequency modes (modes of the retained model), described by polytopic LDI (PLDI):

where *v* is the number of vertexes of the polytopic system. The number of vertexes is given by 2^{p}, where p is the number of uncertainty parameters. The operator *Co* means that the matrix *A _{r,1}*; ...;

*A*define a convex space.

_{r,v} The state vector *x* of the modal coordinates system consists of *n* independent components, *x _{i}*, that represent a state of each mode. The

*x*(

_{i}*i*th state component), related to eq. (3), is defined (Gawronski, 1998):

The use of models obtained by FEM demands high number of degrees of freedom (dof). So, the order of the representation is generally very large, causing numeric difficulties. Besides that, the complexity of the controller is model depend, above all, of the order of the plant in study. Therefore, the synthesis of a low order plant is fundamental for a controller success.

A reduced-order model is obtained by truncating the states. Let *x* and the state (*A*, *B*_{1},* B*_{2}, *C)* be partitioned considering the canonical modal decomposition. From the Jordan canonical form can be obtained:

where *A _{r}(t)* is given by eq. (4). Nothing about performance specifications for high frequency modes was included in the design.

The main problem is to find the order and the retained states that best reproduces the response of the complete system. The choice depends mainly on the definition of the reduction index used. In general, systems norms are used to evaluate the reduction error, (Gawronski, 1998).

Different methods of model reduction through LMI were proposed, for the cases of local and global optimization, using as index the performance systems norms, for instance Assunção et al. (2002) uses H_{¥} norm.

In this work the H_{¥} norm is used as reduction index. The norm of the *ith* natural mode (*A _{mi}*, B

_{2mi},

*C*) can be calculated in different forms. However, this article uses LMI to the computation of the H

_{mi}_{¥}norm. Assunção and Teixeira (2001) demonstrate in full detail as to compute this norm. The H

_{¥}norm system can be found from the following optimization problem:

This norm also corresponds to the peak gain of frequency response function. The H_{¥} norm system is the same the largest norm of the modes. The H_{¥} reduction error is defined as:

where *G* is the transfer function of the nominal system and *G _{r}* is the transfer function of the nominal model.

**Placement of Actuators and Sensors using H¥ Norm**

The actuator should be placed at a location to excite the desired modes in a most effective way. The optimal placement problem consists of to determine the location of a small set of actuators and sensors such that the H_{¥} norm of the system is the closest possible of the norm case using large set of actuator and sensor.

The H_{¥} placement index, s* _{ik}*, evaluates the

*kth*actuator (sensor) at the

*i*th mode. It is defined in relation to all the modes and all the admissible actuators as:

It is convenient to represent the placement index as a placement matrix:

where the *kth* column consists of indexes of the *kth* actuator for every mode, and the *ith* row is a set of the indexes of the *ith* mode for all actuators.

The actuators with small indices can be removed as the least significant. The largest value indices are optimal placement actuator. Similarly, it is possible to determine the optimal placement of the sensors, (Gawronski, 1998).

**State-Feedback Analysis via LMI**

The problem to be investigated is the state-feedback control, with the following linear control law:

where *K* must be found. It is considered to be known all retained states, *x _{r}*. Therefore it is not necessary to use a dynamic observer. It is assumed that the reduced model is representative, so, it is not necessary to include any requirements to treat with dynamic uncertainties. The goal of the present paper is to work with only parametric uncertainties described by polytopics.

The system described by eq. (6) can be rewritten in closed-loop:

The system of eq. (12) is quadratically stable if and only if the following LMI is feasible:

where the symbols *>0 *and *<0* means positive and negative definited, respectively, *A _{r,i}* is

*ith*vertex polytopic system,

*i*=1,2,...,

*v*,

*v*is the number of vertexes and

*Y=KQ*, (Boyd et al., 1994).

Assuming that it is desired to bound the output peak energy and that *Q* satisfies inequalities (13). Defining the ellipsoid, (Folcher and Ghaoui, 1994):

The ellipsoid is said to be invariant if:

where *x _{r}*(0), the initial state, is given.

The maximum output energy given a certain initial state is:

Supposing there exists a Lyapunov function *V(x _{r})=x_{r}^{T}Q^{-1}x_{r}* such that,

then the condition given by the inequalities (17) is equivalent on LMI to:

It is possible to conclude from inequalities (18) that for a given feedback gain *K*, the output energy of system does not exceed *x _{r}*(0)

*(0). Then in this case, the output energy is bounded above*

^{T}Q^{-1}x_{r}*x*(0)

_{r}*(0), where*

^{T}Q^{-1}x_{r}*Q*satisfies the LMI:

where *i*=1,2,.., *v*. Regarding *Y* as a variable, it can find a state-feedback gain that guarantees output energy less than b by solving the LMI problem:

When the initial condition is known, it is also possible to find an upper bound on the norm of the control input, eq. (11). Given *Q*>0 and *Y* which satisfy the quadratic stabilization condition, inequalities (13), and be limited in the ellipsoid from condition given by eq. (14), the upper bound of the control input can be written as:

Therefore, the constraints ||* u*||

**<****r**is enforced at all times

*t*>0 if the LMIs below hold:

where r is the maximum value of amplitude on actuators.

In the same way, it can be possible to impose a decay rate on the closed-loop:

Besides, the under largest decay rate can be found solving the generalized eigenvalue problem (GEVP), (Boyd et al. 1993). In summary, the controller design is the result of the following convex optimization problem, considering r and b known:

This problem can be solved using interior-point methods, (Gahinet et al., 1995). For each initial condition, the input *u* and the output *y* assure:

The optimal feedback gain is given by:

where *Y* and *Q* are solutions from problem given by inequalities (24).

**Numerical Application**

To verify the proposed methodology, an aluminum cantilever beam, as shown on fig. 1, was considered. The system is discretized by FEM 10 elements (2 dof by node), then the total number of structural dof used was 22. For the cantilever condition the system have *N*=40 states. The properties of the beam are given in table 1.

The number of electrical dof changes as a function of the number of PZT considered (2 dof by PZT), (Lopes Jr. et. al., 2000). The PZT size is equal to the discrete finite element size. The properties of PZT, based on material designation PSI-5A-S4 (Piezo Systems, Inc.), are given in table 2.

In order to test the proposed optimization method, the optimal location of actuator, a pair of PZT bonded on the beam surface is considered. The objective in this test was to control the first two vibration modes. It was considered to be possible to bond the PZT in all elements. It was, also, considered finding an optimal location to a displacement sensor to state-feedback. The sensor position candidates consider all nodes on vertical direction.

If two PZT elements are fixed on both sides of the beam and the voltage applied on this elements are in-phase, a longitudinal motion is obtained. If the voltages applied on PZT elements are out-of-phase, then it generates moments at the end of the PZT elements, causing lateral motions, as showed at figs. 2 and 3.

The PZTs actuators used in this article are driven out-phase, which means that they generate a pair of moments as shown in fig. 3. The relationship between the generated moments and applied voltage is given by, (Brennan et al. 1994):

Using eq. (27) and the properties showed on tables 1 and 2, the relationship between the applied voltage and the generated moment is 1836.4/N.m. This means that for a voltage of 110 V, a moment of the order of 0.06 N.m will be generated.

The placement indices computed from eq. (9) of each candidate sensor/actuator for the first two modes are shown in fig. 4. The largest value index is for the PZT actuator bonded in element 1 and sensor on node the free end of the beam (node 10). In our case, for accelerometer, the placement of the sensor in the free end of the beam is not a practical location

For the design is considered a disturbance input as showed in fig. 5. In this figure it is also shown the PZT bonded in element 1 and the sensor in a suboptimal configuration.

The magnitude plots for transfer function of the complete system and reduced-order model are shown in fig. 6. The transfer functions H_{1} and H_{2} are relative with the stace-space realization (*A,B*_{1}*,C*) and (*A,B*_{2}*,C*), respectively. A fourth order model is determined by truncating the system model following the described methodology. The H_{¥} reduction error is about 0.5%. This value was found through H_{¥} norm problem, given by optimization problem described in inequality (7). First, it is computed the H_{¥} norm for the complete model (this value corresponds to the peak gain). In the following the H_{¥} norm relative to the reduced model is found. If the reduction error, given by eq. (8), is lower that an specified value, it means that the reduced model is representative of the complete system.

A mathematical model provides a map from inputs to responses. The quality of a model depends on how closely its response matches those one of the plant. Since no single fixed model can respond exactly like the true plant, we need, at the very last, a set of maps. The term uncertainty refers to the differences or error between models and reality, and whatever it is used to express error, it is called a representation of uncertainty, (Gonçalves et al., 2002).

Even with accurate models, the simple inclusion of sensors and actuators on the host structure cause change on the dynamic properties of the system. The computation of these uncertainties can be difficult in practical situations, or it has a high computational cost. To solve this problem the model with parametric uncertainties can be quantified by range of parameter values. The parameter uncertainty ranges can be described as parameter box. The controller that satisfies all systems described inside this convex space is said robust to parametric variations. It is enough to solve the optimization problem from eq. (24) for all vertex system simultaneously.

It was considered, in this example, that the system can have a possible variation of ± 10% in the first and second natural frequencies, so we have 2 uncertainty parameters:

and 4 vertexes of a polytopic system (2^{p}, where p=2).

The uncertainties are shown at figure 7. The vertexes of the parameter box are combination of the minimum and maximum values of the parameters of the system. It is supposed that the system can assume any combination of values inside the box.

Figure 8 shows the magnitude plots transfer function for all four open-loop system.

To test the proposed methodology, firstly we considered a design based on PZT actuator in a particular case non-optimal place position (in this example, in the element 8). The LMI controller was designed considering all vertex system simultaneously. In this case, it was obtained a robust controller that mathematically guarantees the performance specifications in all convex space. The controller is the result of the solution of LMI problem from inequalities (24), whith r = 1, b =2, and *x _{r}*(0)= [-0.05 0 -0.05 0]

^{T}. Next we redesigned the control law with the PZT actuator in the optimal placement (element 1), and considering the same parameters r , b and

*x*(0). During the control, the maximum voltage on PZT was considered as 100 V.

_{r}Figure 9 compares the magnitude plots of the controlled and uncontrolled system in the nominal condition for PZT located in element 8 and in the optimal placement. The nominal condition is shown on figure 7.

Figure 10 shows the displacement in the time domain for the closed-loop system, considering initial condition *x _{r}*(0) for the two cases considering system in nominal condition.

Figures 11 and 12 show the magnitude plots of the controlled and uncontrolled system considering the four extreme conditions (vertexes of the polytopic systems).

Comparing the figs. 9 until 12 it is possible to observe (in this case) that the effort of the controller with PZT bonded in the 8^{th} element is larger than in the optimal placement. Besides, the attenuation of the interested modes is bigger when the PZT is in an optimal placement. As a result of the active damping the peaks at the resonance of the controlled modes are reduced.

**Conclusions**

The main theoretical contribution of this research work was to propose and to motivate the use of LMI in the structural control community.

First was showed a brief review of structural state-space model in modal coordinates and a reduction model. After this, a strategy for placement of actuators and sensors using H_{¥} norm was presented. This technique of optimal location could be implemented using others norms, for instance, H_{2} norm. In the following a LMI controller was proposed for amplitude attenuation of some modes. To illustrate this procedure was considered the control of a cantilever beam modeled by FEM. In this particular example the state-space model had 40 states. After the reduction procedure it was obtained a model with 4 states that well represented the complete dynamic system. Moreover, we designed a LMI controller robust to parametric variations and compared the amplitude attenuation for PZT in optimal and non-optimal location.

The authors are encouraged by the results obtained and it seems that the methodology developed can be extended to other practical systems, for example, smart plates and space truss structures. An experimental investigation is being implemented in the Vibration Laboratory of UNESP/Ilha Solteira to check the results obtained in the numerical simulations.

**Acknowledgements**

The authors acknowledge the support of the Research Foundation of the State of São Paulo (FAPESP-Brazil) and of the National Council of Scientific and Technological Development (CNPq-Brazil). The authors would like to thank the Associate Editor and the reviewers for their valuable comments.

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Paper accepted November, 2004. Technical Editor: José Roberto de F. Arruda.