# Research on Aircraft Attack Angle Control Considering Servo-Loop Dynamics

Authors: Xiaodong Liu; Yan Wang; Wanwei Huang; Zongxia Jiao
Journal: International Journal of Aerospace Engineering
 (2015)

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## Abstract

This paper presents a novel robust attack angle control approach, which can effectively suppress the impacts from system uncertainties and servo-loop dynamics. A second-order linear model of electromechanical servo loop is considered in the modeling and design processes. With regard to the block-structure models facing attack angle control, the multiple robust surfaces and dynamic surface control (DSC) approaches are both employed. By means of Lyapunov function method, the stability conditions of attack angle control systems are, respectively, given without/with considering the servo-loop dynamics in design process. Computer simulation results present that, compared with the attack angle control scheme which does not consider the servo-loop dynamics in design process, the proposed scheme can guarantee that the whole attack angle control system possesses the better comprehensive performances. Moreover, it is easy to be realized in engineering application.


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## Body

## 1. Introduction

In aircraft attitude control system, the existing system uncertainties, including modeling errors, parameter perturbations, and external disturbances, can badly affect the flight performances and even lead to the failure of flight task [1]. As a result, the impacts of system uncertainties on control performances must be highly valued and then effectively suppressed in the design process of aircraft attitude control law [2–4]. Besides that, the servo-loop dynamics, which is not absolutely ideal, can also affect the performances of the whole attitude control system. Concretely speaking, if the attitude control law is previously designed without considering the servo-loop dynamics, the whole attitude control system will not keep the satisfactory performance when the servo loop is added into the closed-loop system. Therefore, it is necessary to explore the robust attitude control methods with consideration of servo-loop dynamics, in order to further improve the comprehensive performance of the whole attitude control system. Taking the pitching channel into consideration, the attack angle control approach with consideration of a second-order linear model of electromechanical servo loop will be explored in this paper.With regard to the aircraft flight system, the multiple robust surfaces method combined with backstepping method is generally employed [1, 4–6]. However, the traditional integrator backstepping technique suffered from the problem of “explosion of terms,” which can lead to the performance degradation (even the serious instability) of flight control system. In order to solve this problem, Swaroop et al. [7] proposed a kind of dynamic surface control (DSC) method, where the model is not directly differentiated through introducing some groups of low-pass filters. As a result, DSC approach is more appropriately used in the control system with multilevel framework than traditional backstepping approach, and it has been widely applied in the area of flight guidance and control [8–10]. In this paper, taking the pitching channel as an example, DSC method will be employed into the design of attack angle control law on the condition that the servo-loop dynamics is considered. In addition, because sliding mode control (SMC) possesses a series of attractive characteristics, especially the strong robust property against parameter perturbations and external disturbances [11–13], it has been paid more attentions and widely applied in aircraft control areas [3, 6]. Based on this, the SMC theory will be also introduced in the design process of subsystem control.The remainder of this paper is organized as follows. Section2 provides the design models facing attack angle control without/with considering the servo-loop dynamics. Based on as-built models, the dynamic surface attack angle control laws are, respectively, designed without/with considering the servo-loop dynamics in Section 3. In Section 4, the computer simulation results are presented; meanwhile the conclusions and future works are given in Section 5.


## 2. Problem Description

Only considering the pitching channel of aircraft, the attitude motion equations are shown as follows [1]:
(1)α˙=-CYqSmV+ωz1+gcos⁡θV,ω˙z1=Cz1qSLJz1,
where α and θ, respectively, denote the attack angle and the flight path angle; m and V, respectively, denote the mass and the velocity of aircraft; g denotes the acceleration of gravity; ωz1 and Jz1, respectively, denote the pitching angular speed and pitching moment of inertia; q=0.5ρV2 denotes the dynamic pressure and ρ denotes the air density; S and L, respectively, denote the reference area and the reference length for calculating the aerodynamic forces and aerodynamic moments. In addition, CY denotes the aerodynamic lift coefficient, Cz1 denotes the pitching moment coefficient, and the expressions of them in a certain flight extent are shown as follows:
(2)CY=CYαα+CYδzδz,Cz1=Cz1αα+Cz1δzδz,
where δz denotes the output angle of servo loop, CYα denotes the aerodynamic lift coefficient with respect to α, and CYδz denotes the aerodynamic lift coefficient with respect to δz. Meanwhile, Cz1α denotes the pitching moment coefficient with respect to α, and Cz1δz denotes the pitching moment coefficient with respect to δz. Note that (1)-(2) can be used to construct the actual model in simulation.Subsequently, when the servo-loop dynamics is not considered in the design period, the design model facing attack angle control is obtained as follows:(3)α˙=a1α+ωz1+fθ+dα,ω˙z1=a2α+b2δz+dω,
where dα and dω denote system uncertainties, which involves the modeling errors from the actual model to the design model. Moreover,
(4)a1=-CYαqSmV,fθ=gcos⁡θV,a2=Cz1αqSLJz1,b2=Cz1δzqSLJz1≠0.For DC electromechanical servo system, it is usually simplified into a second-order linear model, which is shown as follows:(5)Gs=δzsδzds=ωn2s2+2ξnωns+ωn2,
where ωn and ξn, respectively, denote the angular frequency of natural oscillation and the damping coefficient of servo loop and δzd denotes the command input of servo loop. Moreover, the value selection of ωn and ξn should reflect the demands on the bandwidth and the dynamic properties of servo loop.In fact, (5) can be rewritten in the time-domain form, which is shown as follows:
(6)δ¨z=-2ξnωnδ˙z-ωn2δz+ωn2δzd+dδ,
where dδ denotes the system uncertainty.Therefore, when the servo-loop dynamics is considered in the design period, the design model facing attack angle control will be transformed into(7)α˙=a1α+ωz1+fθ+dα,ω˙z1=a2α+b2δz+dω,δ¨z=-2ξnωnδ˙z-ωn2δz+ωn2δzd+dδ.
At this time, we can see that the original design model (3) with two-layer structure changes into another one (7) with three-layer structure, which directly reflects the deference between the modeling processes without/with considering the servo-loop dynamics.The establishment of design models (3) and (7) lays the foundation for the next design of aircraft attack angle control laws.


## 3. Dynamic Surface Attack Angle Controller Design

With regard to a class of system with strict feedback form, just as system (3) and system (7), multiple robust surfaces method combined with backstepping method is generally employed. However, the traditional integrator backstepping technique suffered from the problem of “explosion of terms”; therefore the other improved control method—DSC—will be applied in this section, where the model is not directly differentiated through introducing some groups of low-pass filters.Owing to the simple design and strong robust property of SMC, it will be introduced in the design process of subsystem control. Furthermore, the reaching law approach [14, 15] can effectively guarantee the better dynamic performance of reaching process; therefore it will be employed to construct the SMC scheme in this section.The following two assumptions are useful in the next design and analysis.Assumption 1.
The uncertainty terms in system are all bounded; that is,dα≤Δα, dω≤Δω, and dδ≤Δδ.Assumption 2.
When the DSC method is applied, the filter outputyfo is in a neighborhood of the filter input yfi; that is, yfo-yfi≤Δf.


### 3.1. Without Consideration of Servo-Loop Dynamics

Aiming at the two-layer design model (3), the dynamic surface attack angle control law can be designed as in the following steps.Step A1. Design the robust surface variable for the 1st-layer subsystem:
(8)s1=α-αd,
where αd denotes the command of attack angle.Step A2. Calculate the virtual command of the 2nd-layer subsystem:
(9)ωz1d=-a1α+α˙d-k1s1-q1sgn⁡s1-fθ,k1>0,q1>0.Step A3. In order to get the differential information of ωz1d, we introduce a filter:
(10)ηω˙z1c+ωz1c=ωz1d,ωz1c0=ωz1d0,η>0.
Based on Assumption 2, we can get ωz1c=ωz1d+dfω, where dfω≤Δfω. In fact, we can adjust the parameter η to make the boundary Δfω arbitrarily small.Step A4. Design the robust surface variable for the 2nd-layer subsystem:
(11)s2=ωz1-ωz1c.Step A5. Calculate the command input of servo loop:
(12)δzd=-a2α-k2s2-q2sgn⁡s2+ω˙z1cb2,k2>0,q2>0.Theorem 3.
When the servo-loop dynamics is not considered, by means of Steps A1–A5, the actual attack angleα will tend to the desired one αd, if the following conditions in (13) are all satisfied:
(13)k1k2>14,q1>Δα+Δfω,q2>Δω.Proof.
Choose a Lyapunov function as follows:(14)V=12s12+12s22.
Then, with the differential operation on (14), one can get
(15)V˙=s˙1s1+s˙2s2.
According to (3), (8), and (11), one can get
(16)s˙1=α˙-α˙d=a1α+ωz1+fθ+dα-α˙d=a1α+s2+ωz1c+fθ+dα-α˙d.
Owing to ωz1c=ωz1d+dfω, (16) can be transformed into
(17)s˙1=a1α+s2+ωz1d+fθ+ds1-α˙d,
where ds1=dα+dfω is bounded with ds1≤Δs1=Δα+Δfω.
Substituting (9) into (17), one can get
(18)s˙1=s2-k1s1-q1sgn⁡s1+ds1.
In similar, according to (3), (11), and (12), one can get
(19)s˙2=ω˙z1-ω˙z1c=a2α+b2δzd+dω-ω˙z1c=-k2s2-q2sgn⁡s2+dω.
Substituting (18)-(19) into (15), we can get
(20)V˙=s2-k1s1-q1sgn⁡s1+ds1s1+-k2s2-q2sgn⁡s2+dωs2=-k1s12-k2s22+s1s2-q1s1+ds1s1-q2s2+dωs2≤-2k1k2s1s2+s1s2-q1s1+Δs1s1-q2s2+Δωs2=-2k1k2-1s1s2-q1-Δs1s1-q2-Δωs2.
Then, under the satisfaction of conditions in (13), we can further get that V˙≤0 always exists. Moreover, when and only when both s1=0 and s2=0 coexist, V˙=0 is tenable. As a result, s1→0 and s2→0 are both realized, which means that the actual attack angle α will tend to the desired one αd.Obviously, the derivation of Theorem3 is carried out based on the condition of δz=δzd, which reflects that the servo-loop dynamics is not considered at this time. However, when the servo-loop dynamics is considered in the design, δz is not equal to δzd anymore; that is, δz=δzd+dm. In fact, we can make dm≤Δm tenable by means of stable control system design, which will be presented in the next subsection.


### 3.2. With Consideration of Servo-Loop Dynamics

In this subsection, aiming at the three-layer design model (7), the dynamic surface attack angle control law can be designed as in the following steps.Step B1. Design the robust surface variable for the 1st-layer subsystem:
(21)s1=α-αd.Step B2. Calculate the virtual command of the 2nd-layer subsystem:
(22)ωz1d=-a1α+α˙d-k1s1-q1sgn⁡s1-fθ,k1>0,q1>0.Step B3. In order to get the differential information of ωz1d, we introduce a filter:
(23)η1ω˙z1c+ωz1c=ωz1d,ωz1c0=ωz1d0,η1>0.Step B4. Design the robust surface variable for the 2nd-layer subsystem:
(24)s2=ωz1-ωz1c.Step B5. Calculate the virtual command of the 3rd-layer subsystem:
(25)δzd=-a2α-k2s2-q2sgn⁡s2+ω˙z1cb2,k2>0,q2>0.Step B6. In order to get the differential information of δzd, we introduce another filter:
(26)η2δ˙zc+δzc=δzd,δzc0=δzd0,η2>0.Step B7. Design the robust surface variable for the 3rd-layer subsystem:
(27)s3=cδz-δzc+δ˙z-δ˙zc,c>0.Step B8. Calculate the command input of servo loop:
(28)δzd*=2ξnωn-cδ˙z+ωn2δz-k3s3m-q3sgn⁡s3+cδ˙zc+δ¨zcωn2-1,mmmmmmmmmmk3>0,q3>0.Theorem 4.
When the servo-loop dynamics is considered, by means of Steps B1–B8, the actual attack angleα will tend to the desired one αd, if the following conditions in (29) are all satisfied:
(29)k1k2>14,q1>Δα+Δfω,q2>Δω+b2Δm,q3>Δδ.Proof.
Choose a Lyapunov function as follows:(30)V=12s12+12s22+12s32.
Then, with the differential operation on (30), one can get
(31)V˙=s˙1s1+s˙2s2+s˙3s3.
According to (7), (27), and (28), one can get
(32)s˙3=cδ˙z-δ˙zc+δ¨z-δ¨zc=cδ˙z-δ˙zc-2ξnωnδ˙z-ωn2δz+ωn2δzd*+dδ-δ¨zc=-k3s3-q3sgn⁡s3+dδ.
When the fourth condition in (29) is satisfied, we can get that V˙b=s˙3s3≤0 always exists. Moreover, when and only when s3=0 exists, V˙b=0 is tenable. Subsequently, we can further get δz→δzc. Then, based on Assumption 2, we can conclude that there is δz=δzd+dm with dm≤Δm.
Subsequently, as similar with the proof process of Theorem3, we can also get the following equations:
(33)s˙1=α˙-α˙d=s2-k1s1-q1sgn⁡s1+ds1s˙2=ω˙z1-ω˙z1c=-k2s2-q2sgn⁡s2+ds2,
where ds2=dω+b2dm and ds2≤Δs2=Δω+b2Δm.
According to (33), we can further get
(34)V˙a=s˙1s1+s˙2s2=s2-k1s1-q1sgn⁡s1+ds1s1+-k2s2-q2sgn⁡s2+ds2s2=-k1s12-k2s22+s1s2-q1s1+ds1s1-q2s2+ds2s2≤-2k1k2s1s2+s1s2-q1s1+Δs1s1-q2s2+Δs2s2=-2k1k2-1s1s2-q1-Δs1s1-q2-Δs2s2.
When the first three conditions in (29) are all satisfied, we can get that V˙a≤0 always exists. Moreover, when and only when both s1=0 and s2=0 coexist, V˙a=0 is tenable. As a result, s1→0 and s2→0 are also realized, which means that the actual attack angle α will tend to the desired one αd.According to (8)–(12), we can calculate the servo-loop command δzd on the condition that the servo-loop dynamics is not considered. Meanwhile, according to (21)–(28), we can calculate new servo-loop command δzd* on the condition that the servo-loop dynamics is considered. This directly reflects the difference between the design processes without/with considering the servo-loop dynamics.


### 3.3. The Improved Control Laws

In order to avoid the high-frequency chattering at control input, which resulted from the signum term in control laws, the following saturation function will be employed to replace the signum function:(35)sat⁡s=sκ,s≤κ,sgn⁡s,s>κ,κ>0.
After introducing the saturation function (35), the final dynamic surface control laws without/with consideration of servo-loop dynamics can be, respectively and comprehensively, expressed by
(36)s1=α-αd,ωz1d=-a1α+α˙d-k1s1-q1sat⁡s1-fθ,ηω˙z1c+ωz1c=ωz1d,ωz1c0=ωz1d0,s2=ωz1-ωz1c,δzd=-a2α-k2s2-q2sat⁡s2+ω˙z1cb2,s1=α-αd,ωz1d=-a1α+α˙d-k1s1-q1sat⁡s1-fθ,η1ω˙z1c+ωz1c=ωz1d,ωz1c0=ωz1d0,s2=ωz1-ωz1c,δzd=-a2α-k2s2-q2sat⁡s2+ω˙z1cb2,η2δ˙zc+δzc=δzd,δzc0=δzd0,s3=cδz-δzc+δ˙z-δ˙zc,δzd*=2ξnωn-cδ˙z+ωn2δz-k3s3m-q3sat⁡s3+cδ˙zc+δ¨zcωn2-1.It can be proved that if the signum functions are replaced by the saturation functions, the Lyapunov asymptotic stability presented in Theorems3 and 4 will degenerate into Lyapunov bounded stability under the same conditions. Moreover, we can adjust the parameter κ to make the convergence boundary arbitrarily small.Until now, the attack angle control laws have been finished without/with considering the servo-loop dynamics. These two control schemes will be verified and compared by means of computer simulations in the next section.


## 3.1. Without Consideration of Servo-Loop Dynamics

Aiming at the two-layer design model (3), the dynamic surface attack angle control law can be designed as in the following steps.Step A1. Design the robust surface variable for the 1st-layer subsystem:
(8)s1=α-αd,
where αd denotes the command of attack angle.Step A2. Calculate the virtual command of the 2nd-layer subsystem:
(9)ωz1d=-a1α+α˙d-k1s1-q1sgn⁡s1-fθ,k1>0,q1>0.Step A3. In order to get the differential information of ωz1d, we introduce a filter:
(10)ηω˙z1c+ωz1c=ωz1d,ωz1c0=ωz1d0,η>0.
Based on Assumption 2, we can get ωz1c=ωz1d+dfω, where dfω≤Δfω. In fact, we can adjust the parameter η to make the boundary Δfω arbitrarily small.Step A4. Design the robust surface variable for the 2nd-layer subsystem:
(11)s2=ωz1-ωz1c.Step A5. Calculate the command input of servo loop:
(12)δzd=-a2α-k2s2-q2sgn⁡s2+ω˙z1cb2,k2>0,q2>0.Theorem 3.
When the servo-loop dynamics is not considered, by means of Steps A1–A5, the actual attack angleα will tend to the desired one αd, if the following conditions in (13) are all satisfied:
(13)k1k2>14,q1>Δα+Δfω,q2>Δω.Proof.
Choose a Lyapunov function as follows:(14)V=12s12+12s22.
Then, with the differential operation on (14), one can get
(15)V˙=s˙1s1+s˙2s2.
According to (3), (8), and (11), one can get
(16)s˙1=α˙-α˙d=a1α+ωz1+fθ+dα-α˙d=a1α+s2+ωz1c+fθ+dα-α˙d.
Owing to ωz1c=ωz1d+dfω, (16) can be transformed into
(17)s˙1=a1α+s2+ωz1d+fθ+ds1-α˙d,
where ds1=dα+dfω is bounded with ds1≤Δs1=Δα+Δfω.
Substituting (9) into (17), one can get
(18)s˙1=s2-k1s1-q1sgn⁡s1+ds1.
In similar, according to (3), (11), and (12), one can get
(19)s˙2=ω˙z1-ω˙z1c=a2α+b2δzd+dω-ω˙z1c=-k2s2-q2sgn⁡s2+dω.
Substituting (18)-(19) into (15), we can get
(20)V˙=s2-k1s1-q1sgn⁡s1+ds1s1+-k2s2-q2sgn⁡s2+dωs2=-k1s12-k2s22+s1s2-q1s1+ds1s1-q2s2+dωs2≤-2k1k2s1s2+s1s2-q1s1+Δs1s1-q2s2+Δωs2=-2k1k2-1s1s2-q1-Δs1s1-q2-Δωs2.
Then, under the satisfaction of conditions in (13), we can further get that V˙≤0 always exists. Moreover, when and only when both s1=0 and s2=0 coexist, V˙=0 is tenable. As a result, s1→0 and s2→0 are both realized, which means that the actual attack angle α will tend to the desired one αd.Obviously, the derivation of Theorem3 is carried out based on the condition of δz=δzd, which reflects that the servo-loop dynamics is not considered at this time. However, when the servo-loop dynamics is considered in the design, δz is not equal to δzd anymore; that is, δz=δzd+dm. In fact, we can make dm≤Δm tenable by means of stable control system design, which will be presented in the next subsection.


## 3.2. With Consideration of Servo-Loop Dynamics

In this subsection, aiming at the three-layer design model (7), the dynamic surface attack angle control law can be designed as in the following steps.Step B1. Design the robust surface variable for the 1st-layer subsystem:
(21)s1=α-αd.Step B2. Calculate the virtual command of the 2nd-layer subsystem:
(22)ωz1d=-a1α+α˙d-k1s1-q1sgn⁡s1-fθ,k1>0,q1>0.Step B3. In order to get the differential information of ωz1d, we introduce a filter:
(23)η1ω˙z1c+ωz1c=ωz1d,ωz1c0=ωz1d0,η1>0.Step B4. Design the robust surface variable for the 2nd-layer subsystem:
(24)s2=ωz1-ωz1c.Step B5. Calculate the virtual command of the 3rd-layer subsystem:
(25)δzd=-a2α-k2s2-q2sgn⁡s2+ω˙z1cb2,k2>0,q2>0.Step B6. In order to get the differential information of δzd, we introduce another filter:
(26)η2δ˙zc+δzc=δzd,δzc0=δzd0,η2>0.Step B7. Design the robust surface variable for the 3rd-layer subsystem:
(27)s3=cδz-δzc+δ˙z-δ˙zc,c>0.Step B8. Calculate the command input of servo loop:
(28)δzd*=2ξnωn-cδ˙z+ωn2δz-k3s3m-q3sgn⁡s3+cδ˙zc+δ¨zcωn2-1,mmmmmmmmmmk3>0,q3>0.Theorem 4.
When the servo-loop dynamics is considered, by means of Steps B1–B8, the actual attack angleα will tend to the desired one αd, if the following conditions in (29) are all satisfied:
(29)k1k2>14,q1>Δα+Δfω,q2>Δω+b2Δm,q3>Δδ.Proof.
Choose a Lyapunov function as follows:(30)V=12s12+12s22+12s32.
Then, with the differential operation on (30), one can get
(31)V˙=s˙1s1+s˙2s2+s˙3s3.
According to (7), (27), and (28), one can get
(32)s˙3=cδ˙z-δ˙zc+δ¨z-δ¨zc=cδ˙z-δ˙zc-2ξnωnδ˙z-ωn2δz+ωn2δzd*+dδ-δ¨zc=-k3s3-q3sgn⁡s3+dδ.
When the fourth condition in (29) is satisfied, we can get that V˙b=s˙3s3≤0 always exists. Moreover, when and only when s3=0 exists, V˙b=0 is tenable. Subsequently, we can further get δz→δzc. Then, based on Assumption 2, we can conclude that there is δz=δzd+dm with dm≤Δm.
Subsequently, as similar with the proof process of Theorem3, we can also get the following equations:
(33)s˙1=α˙-α˙d=s2-k1s1-q1sgn⁡s1+ds1s˙2=ω˙z1-ω˙z1c=-k2s2-q2sgn⁡s2+ds2,
where ds2=dω+b2dm and ds2≤Δs2=Δω+b2Δm.
According to (33), we can further get
(34)V˙a=s˙1s1+s˙2s2=s2-k1s1-q1sgn⁡s1+ds1s1+-k2s2-q2sgn⁡s2+ds2s2=-k1s12-k2s22+s1s2-q1s1+ds1s1-q2s2+ds2s2≤-2k1k2s1s2+s1s2-q1s1+Δs1s1-q2s2+Δs2s2=-2k1k2-1s1s2-q1-Δs1s1-q2-Δs2s2.
When the first three conditions in (29) are all satisfied, we can get that V˙a≤0 always exists. Moreover, when and only when both s1=0 and s2=0 coexist, V˙a=0 is tenable. As a result, s1→0 and s2→0 are also realized, which means that the actual attack angle α will tend to the desired one αd.According to (8)–(12), we can calculate the servo-loop command δzd on the condition that the servo-loop dynamics is not considered. Meanwhile, according to (21)–(28), we can calculate new servo-loop command δzd* on the condition that the servo-loop dynamics is considered. This directly reflects the difference between the design processes without/with considering the servo-loop dynamics.


## 3.3. The Improved Control Laws

In order to avoid the high-frequency chattering at control input, which resulted from the signum term in control laws, the following saturation function will be employed to replace the signum function:(35)sat⁡s=sκ,s≤κ,sgn⁡s,s>κ,κ>0.
After introducing the saturation function (35), the final dynamic surface control laws without/with consideration of servo-loop dynamics can be, respectively and comprehensively, expressed by
(36)s1=α-αd,ωz1d=-a1α+α˙d-k1s1-q1sat⁡s1-fθ,ηω˙z1c+ωz1c=ωz1d,ωz1c0=ωz1d0,s2=ωz1-ωz1c,δzd=-a2α-k2s2-q2sat⁡s2+ω˙z1cb2,s1=α-αd,ωz1d=-a1α+α˙d-k1s1-q1sat⁡s1-fθ,η1ω˙z1c+ωz1c=ωz1d,ωz1c0=ωz1d0,s2=ωz1-ωz1c,δzd=-a2α-k2s2-q2sat⁡s2+ω˙z1cb2,η2δ˙zc+δzc=δzd,δzc0=δzd0,s3=cδz-δzc+δ˙z-δ˙zc,δzd*=2ξnωn-cδ˙z+ωn2δz-k3s3m-q3sat⁡s3+cδ˙zc+δ¨zcωn2-1.It can be proved that if the signum functions are replaced by the saturation functions, the Lyapunov asymptotic stability presented in Theorems3 and 4 will degenerate into Lyapunov bounded stability under the same conditions. Moreover, we can adjust the parameter κ to make the convergence boundary arbitrarily small.Until now, the attack angle control laws have been finished without/with considering the servo-loop dynamics. These two control schemes will be verified and compared by means of computer simulations in the next section.


## 4. Simulation Results

In this section, the simulation results of the proposed control scheme are compared with those of conventional control scheme, which is designed without considering the servo-loop dynamics.In simulation, the parameters of researched aircraft are shown as follows:V=2000m/s, m=1000kg, ρ=1.0kg/m3, S=0.45m2, L=0.70m, and Jz1=5800 kg·m2. The nominal aerodynamic parameters are shown as follows: CYα=57.26rad-1, CYδz=3.63rad-1, Cz1α=-28.02rad-1, and Cz1δz=-37.97rad-1. Note that 10% perturbation of aerodynamic parameters will be considered in the actual plant. The parameters of servo loop are shown as follows: ωn=100rad/s and ξn=0.3. Moreover, taking the practical situation into consideration, the controller output is limited between ±35 deg.In the selection process of control coefficients, the coefficients of low-pass filters and saturation functions can be first obtained. In concrete, the filter coefficients are selected based on the compromise between estimation accuracy on virtual command and suppression effect on “explosion of terms”; meanwhile the saturation function coefficients are selected based on the compromise between robust property of control system and smooth property of control output. As a result, we first selectη=η1=η2=0.001 and κ=0.1. Then, the remainder coefficients in the two control schemes are all obtained by means of trial and errors method, and they are shown as follows.When the servo-loop dynamics is not considered, the coefficients of attack angle control law are chosen as follows:k1=15, q1=3, k2=20, and q2=2.When the servo-loop dynamics is considered, the coefficients of attack angle control law are chosen as follows:k1=30, q1=6, k2=30, q2=10, c=500, k3=40, and q3=5.The step response of servo loop is illustrated in Figure1.Figure 1
Step response curve of servo loop.As seen from Figure1, the nonideal dynamic characteristics of servo loop are obviously presented, including regulation time, overshoot, and stable errors, which will affect the working performance of the whole pitching control system.With computer simulation on the whole pitching control system, the comparison curves of attack angles under the two control schemes are shown in Figure2.Figure 2
Curves of attack angles under the two control schemes.As seen from Figure2, both the two robust control schemes can guarantee good tracking performances. However, when the servo-loop dynamics is considered in the scheme design, the response speed of attack angle is faster, and the stable tacking errors are smaller.Next, the outputs of servo loops under the two control schemes are shown in Figure3.Figure 3
Output curves of servo loops under the two control schemes.As seen from Figure3, the servo-loop output is smoother under the proposed control scheme, which is beneficial to the stability of the whole control system.At this time, the control coefficients of the conventional scheme are chosen the same as with the proposed scheme; that is,k1=30, q1=6, k2=30, and q2=10, and then the tracking curve of attack angle under the conventional control scheme is shown in Figure 4.Figure 4
Tracking curve of attack angle under the conventional control scheme.As seen from Figure4, when the control parameters of the conventional scheme are increased, the bad stability is presented clearly, which reflects that the design margin can be effectively enhanced when the servo-loop dynamics is considered in the design process. Until now, the performance advantages under the proposed control scheme have been verified.


## 5. Conclusions

With consideration of second-order dynamics of electromechanical servo loop, this paper puts forward a robust attack angle control approach. By means of sliding mode control and dynamic surface control theories, the multiple subsystems of control plant are effectively connected, and the robust property of control system is also guaranteed. The stability analysis on attack angle control systems is given by using Lyapunov function method. From simulation results, we can see that the proposed scheme can guarantee that the attack angle control system possesses more satisfactory performances, compared with the conventional one which did not consider the servo-loop dynamics in design period. Moreover, the structure of the proposed control scheme is simple; therefore it is easy to be realized in engineering application. In addition, the proposed method in this paper can be extended to explore the robust whole-channel attitude control approaches, which will be carried out in future works.



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*Source: 284863-2015-01-26.xml*