Nonlinear Adaptive Flight Control of a Hyper Sonic Vehicle_2
Vehicle Systems & Control Laboratory - Nonlinear Adaptive … · 2018. 12. 5. · Objectives...
Transcript of Vehicle Systems & Control Laboratory - Nonlinear Adaptive … · 2018. 12. 5. · Objectives...
Nonlinear Adaptive Dynamic Inversion Applied to
a Generic Hypersonic Vehicle
Elizabeth Rollins and John ValasekVehicle Systems & Control Laboratory, Texas A&M University
andJonathan A. Muse and Michael A. Bolender
U.S. Air Force Research Laboratory, Wright-Patterson Air Force Base
Approved for Public Release; Distribution Unlimited. Case Number88ABW-2013-3391.
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Outline
Introduction
Nonlinear Adaptive Dynamic Inversion Control Architecture
Analysis of the Nonlinear Adaptive Dynamic Inversion ControlArchitecture During Inlet Unstarts
Conclusions
Extensions
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Outline
IntroductionMotivationLiterature SurveyResearch IssuesObjectives
Nonlinear Adaptive Dynamic Inversion Control Architecture
Analysis of the Nonlinear Adaptive Dynamic Inversion ControlArchitecture During Inlet Unstarts
Conclusions
Extensions
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Motivation
Control of Hypersonic Vehicles
• Wide range of flight conditions
• Highly integrated elastic vehicle
• Uncertainties
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Motivation
Inlet Unstart
• Safety concern in hypersonic flight
• Three main causes of inlet unstarts:
1 A flow to the inlet that is slower than the required operatingMach number for the engine,
2 An altered flow that no longer passes through the throat of theengine, and
3 An increase in the back pressure in the engine that causes theshock wave to move ahead of the throat [1].
• Example - Boeing X-51A Waverider
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Literature Survey
• Use of linearized models of hypersonic vehicles to designcontrollers:
- Annaswamy, A. M., Jang, J., and Lavretsky, E. ”AdaptiveGain-Scheduled Controller in the Presence of ActuatorAnomalies.” 2008. [2]
- Gibson, T. E. and Annaswamy, A. M. ”Adaptive Control ofHypersonic Vehicles in the Presence of Thrust and ActuatorUncertainties.” 2008. [3]
- Groves, K. P., et al. ”Reference Command Tracking for aLinearized Model of an Air-breathing Hypersonic Vehicle.”2005. [4]
- Bolender, M. A., Staines, J. T., and Dolvin, D. J. ”HIFiRE 6:An Adaptive Flight Control Experiment.” 2012. [5]
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Literature Survey
• Use of nonlinear models of hypersonic vehicles to designcontrollers:
- Johnson, E. N., et al. ”Adaptive Guidance and Control forAutonomous Hypersonic Vehicles.” 2006. [6]
- Fiorentini, L., et al. ”Nonlinear Robust Adaptive Control ofFlexible Air-breathing Hypersonic Vehicles.” 2009. [7]
- Parker, J. T., et al. ”Approximate Feedback Linearization ofan Air-breathing Hypersonic Vehicle.” 2006. [8]
- Brocanelli, M., et al. ”Robust Control for Unstart Recovery inHypersonic Vehicles.” 2012. [9]
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Research Issues
• Control of hypersonic flight vehicles modeled as couplednonlinear equations with significant parametric uncertainty inthe aerodynamics
• Preventing inlet unstart due to exceeding limits on states
• Preventing inlet unstart due to control surface failures
• Maintaining reasonable tracking following an inlet unstart
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Objectives
Develop a nonlinear adaptive dynamic inversion controlarchitecture that:
1 Uses the complete coupled nonlinear dynamic equations for aninelastic, rigid body model of a hypersonic vehicle
2 Can enforce state constraints to prevent inlet unstarts thatoccur because of changes in angle-of-attack (α) and sideslipangle (β)
3 Is capable of preventing the loss of the vehicle following aninlet unstart
4 Is easily extensible to fault tolerant control methods
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Scope
Plant: The Generic Hypersonic Vehicle (GHV)
• Academic hypersonic vehicle model created at AFRL.
• Nonlinear, 6-DOF, inelastic, no rotors, CFD aero fromshock-expansion viscous corrected. [10]
• Four control surfaces - Two elevons, two ruddervators.
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Outline
Introduction
Nonlinear Adaptive Dynamic Inversion Control ArchitectureGeneral Adaptive Dynamic Inversion EquationsSimulation ResultsRobustness Analysis
Analysis of the Nonlinear Adaptive Dynamic Inversion ControlArchitecture During Inlet Unstarts
Conclusions
Extensions
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Nonlinear Adaptive Dynamic Inversion Control
Architecture for the GHV
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Case 1: Equal Number of Controls and Controlled
Variables
Given a general nonlinear equation of a system in the form
x = f(x) + g(x)u (1)
the dynamic equations for α, β, and µ can be written in the sameform as Equation (1) as
βαµ
=
1
mVT
(
(Ys + FTy)Cβ + mgSµCγ − FTx
CαSβ − FTzSαSβ
)
1
mVTCβ
(
−Ls + mgCµCγ − FTxSα + FTz
Cα)
1
mVT
(
Ls(Tβ + TγSµ) + (Ys + FTy)TγCµCβ − mgCγCµTβ
+ (FTxSα − FTz
Cα)(TγSµ + Tβ) − (FTxCα + FTz
Sα)TγCµSβ
)
+
Sα 0 −Cα
−TβCα 1 −TβSα
Cα/Cβ 0 Sα/Cβ
pqr
.
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Case 1: Equal Number of Controls and Controlled
Variables
Suppose that a desired reference model for the system is chosen tobe
xm = Axm +Br. (2)
The equation for the error between the reference model and theactual system is
e = xm − x. (3)
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Case 1: Equal Number of Controls and Controlled
Variables
Taking the time derivative of Equation (3) results in
e = xm − x = xm − f(x)− g(x)u. (4)
The control u is chosen to be
u = [g(x)]−1[xm − f(x) +Ke− ν]. (5)
Substituting Equation (5) into Equation (4) and defining∆ = f(x)− f(x) produces the error dynamics
e = −Ke+∆+ ν. (6)
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Case 1: Equal Number of Controls and Controlled
Variables
Assume that ∆ can be represented in the form ∆ = W Tβ(x; d),where d is a vector of bounded continuous exogenous inputs.Choose ν to be ν = −W Tβ(x; d). Then, Equation (6) can bewritten as
e = −Ke− W Tβ(x; d) (7)
where W = W −W , which is the weight estimation error.
Finally, the adaptive law to ensure Lyapunov stability is defined as
˙W = ΓW Proj(W , β(x; d)eT ) (8)
where Proj represents the projection operator [11], which is usedto maintain specified bounds on the weights
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Case 2: Number of Controls > Number of Controlled
Variables
Given a general nonlinear equation of a system in the form
x = f(x) + g(x)Λu (9)
the dynamic equations for p, q, and r can be written in the sameform as
ω = I−1(ω × Iω) + I−1(MT +MA(δ = 0))︸ ︷︷ ︸f(x)
+ I−1Mδδ︸ ︷︷ ︸g(x)Λu
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Case 2: Number of Controls > Number of Controlled
Variables
ω = I−1(ω × Iω) + I−1(MT +MA(δ = 0))︸ ︷︷ ︸f(x)
+ I−1Mδδ︸ ︷︷ ︸g(x)Λu
where(ω × Iω) = −
−Jxzpq + (Jz − Jy)qr
(Jx − Jz)pr + Jxz(p2− r2)
Jxzqr + (Jy − Jx)pq
MA(δ = 0) =
qSb
(
C`,baseline + b2VT
(C`pp)
)
qSc
(
Cm,baseline +c
2VT
(Cmq q + Cmαα) + 2Cmδf,r
(δf,r = 0) + 2Cmδt,r(δt,r = 0)
)
− 2CNδf,r(δf,r = 0)qSxcg − 2CNδt,r
(δt,r = 0)qSxcg
qSb
(
Cr,baseline + b2VT
(Cnr r)
)
− 2CYδf,r(δf,r = 0)qSxcg − 2CYδt,r
(δt,r = 0)qSxcg
Mδ =
b∂C`∂δf,r
b∂C`∂δf,l
b∂C`∂δt,r
b∂C`∂δt,l
(
c ∂Cm∂δf,r
− xcg∂CN∂δf,r
) (
c ∂Cm∂δf,l
− xcg∂CN∂δf,l
) (
c ∂Cm∂δt,r
− xcg∂CN∂δt,r
) (
c ∂Cm∂δt,l
− xcg∂CN∂δt,l
)
(
b ∂Cn∂δf,r
− xcg∂CY∂δf,r
) (
b ∂Cn∂δf,l
− xcg∂CY∂δf,l
) (
b ∂Cn∂δt,r
− xcg∂CY∂δt,r
) (
b ∂Cn∂δt,l
− xcg∂CY∂δt,l
)
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Case 2: Number of Controls > Number of Controlled
Variables
Suppose that the desired dynamics of the closed loop system aregiven by
xm = Axm +Br. (10)
The equation for the error between the reference model and theactual system is
e = xm − x. (11)
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Case 2: Number of Controls > Number of Controlled
Variables
Taking the time derivative of Equation (11) results in
e = xm − x = xm − f(x)− g(x)Λu. (12)
The desired final form for e is
e = −Ke− W Tβ(x; d) + g(x)Λu (13)
which is the same as the final form for e in Case 1, except for thefinal term g(x)Λu.
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Case 2: Number of Controls > Number of Controlled
Variables
In order to express e in the final desired form of Equation (13), theterm g(x)Λu is added and subtracted from Equation (12) toproduce
e = xm − f(x)− g(x)Λu+ g(x)Λu. (14)
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Case 2: Number of Controls > Number of Controlled
Variables
In order to determine a specific control law for the system, aconstrained optimization problem is solved in which the costfunction
J = uTQu (15)
where Q = QT > 0, will be minimized, subject to the constraintg(x)Λu = `, which must be satisfied at all times. The term ` isbased on the control from Case 1 and is expressed as
` = xm − f(x) +Ke− ν. (16)
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Case 2: Number of Controls > Number of Controlled
Variables
To derive the control law, first the constraint must be included inthe cost function to form the augmented cost function
J = uTQu+ λT (g(x)Λu− `) (17)
where λ ∈ Rn is a Lagrange multiplier. The first order necessary
conditions for minimizing J are given by
∂J
∂λ= g(x)Λu− ` = 0 (18)
∂J
∂u= 2Qu+ ΛT gT (x)λ = 0. (19)
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Case 2: Number of Controls > Number of Controlled
Variables
From the first order necessary conditions, the control law isdetermined to be
u = Q−1ΛT gT (x)(g(x)ΛQ−1ΛT gT (x))−1`. (20)
where` = xm − f(x) +Ke− ν (21)
Note that for the case where n = m, Equation (20) simplifies tothe control law in Case 1, which is
u = [g(x)]−1[xm − f(x) +Ke− ν]. (22)
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Case 2: Number of Controls > Number of Controlled
Variables
Continuing with the derivation of e, let ∆ = f(x)− f(x).Substituting Equation (20) and Equation (16) into Equation (14)produces the equation
e = −Ke+∆+ ν + g(x)Λu. (23)
Again, assume that ∆ can be represented in the form∆ = W Tβ(x; d), and choose ν to be ν = −W Tβ(x; d), where d isa vector of bounded continuous exogenous inputs. Then, Equation(23) can be written as
e = −Ke− W Tβ(x; d) + g(x)Λu (24)
where W = W −W , which is the weight estimation error.
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Case 2: Number of Controls > Number of Controlled
Variables
Finally, the adaptive laws to ensure Lyapunov stability are definedas
˙W = ΓW Proj(W , β(x; d)eT ) (25)
˙Λ = ΓΛ Proj(Λ,−ueT g(x)) (26)
where Proj represents the projection operator, which is used to
maintain specified bounds on W and Λ.
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Simulation Results
Objective: Evaluate tracking of a specified reference trajectory,6/80K.
Commands to α, β, and µ are given as ramp signals from 0degrees to a desired angle in a fixed amount of time.
Current simulation includes:
• Velocity PID Controller
• Second-order actuator dynamics with ζ = 0.7 and ωn = 25 Hz
• Time delay of 0.03 s (Note: time delays of 0.04 s can betolerated as well)
α, β, µ inversion controller: β(x; d) =[c α β µ M
]T, where
c is a constant bias term.
P, Q, R inversion controller: β(x; d) =[c p q r α β M
]T,
where c is a constant bias term.
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Simulation Results
For α = ±2 deg, β = 0 deg, and µ = 70 deg,
0 5 10 15 20 25 30−10
0
10
20
30
40
time (s)
angu
lar
rate
(de
g/s)
P, Q, R
p
q
rp
c
qc
rc
0 5 10 15 20 25 30
−2
−1
0
1
2
time (s)
angl
e (d
eg)
Angle−of−Attack and Sideslip Angle
αβα
c
βc
0 5 10 15 20 25 30−20
0
20
40
60
80
time (s)
angl
e (d
eg)
Bank Angle
µµ
c
0 5 10 15 20 25 30−1000
0
1000
2000
3000
4000
5000
6000
7000
time (s)
velo
city
(ft/
s)
U, V, W
u
v
w
0 5 10 15 20 25 30
5865.3
5865.4
5865.5
5865.6
5865.7
5865.8
5865.9
5866
5866.1
5866.2
time (s)
tota
l vel
ocity
(ft/
s)
Total Velocity
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Simulation Results
For α = ±2 deg, β = 0 deg, and µ = 70 deg,
0 5 10 15 20 25 30−0.2
−0.1
0
0.1
0.2
time (s)
adap
tive
wei
ght
Adaptive Weights forP, Q, R Inversion
0 5 10 15 20 25 30−2
−1
0
1
2
time (s)
adap
tive
Λ w
eigh
t
Adaptive Λ Weightsfor P, Q, R Inversion
0 5 10 15 20 25 30−1
−0.5
0
0.5
1x 10
−3
time (s)
adap
tive
wei
ght
Adaptive Weights forα, β, µ Inversion
0 5 10 15 20 25 300
0.2
0.4
0.6
0.8
1
time (s)
equi
vale
nce
ratio
Equivalence Ratio
0 5 10 15 20 25 30−30
−20
−10
0
10
20
30
time (s)
cont
rol s
urfa
ce d
efle
ctio
n (d
eg)
Control Surfaces
δf,r
δf,l
δt,r
δt,l
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Robustness Analysis
Uncertainties in the plant examined in the analysis include theadditive uncertainties ∆Cmα , ∆Cnβ
, and ∆Cm and multiplicativegains D on the control surface deflections, given in terms ofequations as
Cm = Cmbaseline+∆Cmαα (27)
Cn = Cnbaseline+∆Cnβ
β (28)
Cm = Cmbaseline+∆Cm (29)
Cδ = DCδo . (30)
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Robustness Analysis
Table 1: Additive uncertainty ∆Cmαover a 30 s period with 0.03 s time
delay.
α (deg) β (deg) µ (deg) max ∆Cmα min ∆Cmα
(deg−1) (deg−1)
5 0 0 0.0005 -0.0013
5 1 20 0.0003 -0.0011
Table 2: Additive uncertainty ∆Cnβover a 30 s period with 0.03 s time
delay.
α (deg) β (deg) µ (deg) max ∆Cnβmin ∆Cnβ
(deg−1) (deg−1)
0 1 0 0.007 -0.003
5 0 20 0.01 -0.004
5 1 20 0.006 -0.003
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Robustness Analysis
Table 3: Additive uncertainty ∆Cm over a 30 s period with 0.03 s timedelay.
α (deg) β (deg) µ (deg) max ∆Cm min ∆Cm
5 0 0 0.0005 -0.003
5 1 20 0.0005 -0.002
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Robustness Analysis
Table 4: Multiplicative gains D on control surface deflection terms over a30 s period with 0.03 s time delay.
α (deg) β (deg) µ (deg) Dδf,r Dδf,l Dδt,r Dδt,l
5 0 0 1 0.14 1 1
5 0 0 1 1 1 0.01
5 0 0 0.15 0.15 1 1
5 0 0 1 1 0.15 0.15
5 0 20 1 0.31 1 1
5 0 20 1 1 1 0.01
5 0 20 0.21 0.21 1 1
5 0 20 1 1 0.30 0.30
5 1 20 1 0.42 1 1
5 1 20 1 1 1 0.05
5 1 20 0.38 0.38 1 1
5 1 20 1 1 0.38 0.38
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Outline
Introduction
Nonlinear Adaptive Dynamic Inversion Control Architecture
Analysis of the Nonlinear Adaptive Dynamic Inversion ControlArchitecture During Inlet Unstarts
Modeling an Inlet UnstartFlight Path Angle Reference Trajectory GenerationSimulation Results
Conclusions
Extensions
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Modeling an Inlet Unstart
For this simplified model, an inlet unstart is triggered at a specifiedtime, and the following changes occur in the GHV plant:
• Instantaneous loss of thrust,
• Slight increase in the coefficient of the axial force (CA),
• Slight decrease in the coefficient of the normal force (CN ),and
• Inclusion of additive variations in Cmα and Cnβthrough the
equationsCm = Cmbaseline
+∆Cmαα (31)
Cn = Cnbaseline+∆Cnβ
β. (32)
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Flight Path Angle Reference Trajectory Generation
To allow the GHV simulation to track a flight path angle trajectorygenerated using a nonzero setpoint (NZSP) controller, a methodfrom Reference [12] was applied in which the equation for h, whereh represents the altitude of the aircraft, is written in the form
h =[b0V + b1β + b2α
]+
[a0 a1 a2
]p
q
r
(33)
wherea0 = b4
a1 = b3Cφ + b4SφTθ
a2 = b4CφTθ − b3Sφ
andb0 = CβCαSθ − SβSφCθ − CβSαCφCθ
b1 = V (−SβCαSθ − CβSφCθ + SβSαCφCθ)
b2 = V (−CβSαSθ − CβCαCφCθ)
b3 = V (CβCαCθ + SβSφSθ + CβSαCφSθ)
b4 = V (−SβCφCθ + CβSαSφCθ) .36 / 50
Flight Path Angle Reference Trajectory Generation
The original reference trajectory that is generated for γ using theNZSP controller can be converted to h using the relation fromaircraft kinematics that h = V Sγ . The h, β, µ inversion controllerreplaces the original α, β, µ inversion controller in the GHVsimulation, and now desired trajectories for γ can be tracked.
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Simulation Results
Track flight path angle trajectory during inlet unstart at 10 seconds,6/80K.
0 10 20 30 40 50 60−5
0
5
time (s)
angu
lar
rate
(de
g/s)
P, Q, R
p
q
rp
c
qc
rc
0 10 20 30 40 50 60
−200
0
200
400
600
time (s)
altit
ude
rate
(ft/
s)
Altitude Rate
h
h c
0 10 20 30 40 50 60−1
−0.5
0
0.5
1
time (s)
angl
e (d
eg)
Bank Angle and Sideslip Angle
µβµ
c
βc
0 10 20 30 40 50 60−1
0
1
2
3
4
5
6
time (s)
angl
e (d
eg)
Flight Path Angle
γγp
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Simulation Results
For the generated flight path angle trajectory during an inlet unstart at10 seconds
0 10 20 30 40 50 60−0.5
0
0.5
time (s)
adap
tive
wei
ght
Adaptive Weights forP, Q, R Inversion
0 10 20 30 40 50 60−2
−1
0
1
2
time (s)
adap
tive
Λ w
eigh
t
Adaptive Λ Weightsfor P, Q, R Inversion
0 10 20 30 40 50 60−5
0
5
time (s)
adap
tive
wei
ght
Adaptive Weights forα, β, µ Inversion
0 10 20 30 40 50 600
0.2
0.4
0.6
0.8
1
time (s)
equi
vale
nce
ratio
Equivalence Ratio
0 10 20 30 40 50 60−30
−20
−10
0
10
20
30
time (s)
cont
rol s
urfa
ce d
efle
ctio
n (d
eg)
Control Surfaces
δf,r
δf,l
δt,r
δt,l
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Outline
Introduction
Nonlinear Adaptive Dynamic Inversion Control Architecture
Analysis of the Nonlinear Adaptive Dynamic Inversion ControlArchitecture During Inlet Unstarts
Conclusions
Extensions
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Conclusions
• The approach of nonlinear adaptive dynamic inversion controlworks well as a candidate control architecture for hypersonicvehicles because
- the control architecture is able to maintain trackingperformance without excessive control effort while beingrobust to
• decreases in control surface effectiveness,• changes in system parameters, and• time delays of 0.04 seconds or less, and
- the control architecture can tolerate an inlet unstart andmaintain nominal tracking of a specified flight path angletrajectory.
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Conclusions
• The nonlinear adaptive dynamic inversion control architecturecan maintain reference trajectory tracking with only a slightdegradation in tracking performance following an inlet unstart.
- Through a robustness analysis on the GHV, it wasdetermined that the maximum additive variations inCmα and Cnβ
that the control architecture could toleratewere ∆Cmα = 0.001 deg−1 and ∆Cnβ
= −0.001 deg−1.
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Outline
Introduction
Nonlinear Adaptive Dynamic Inversion Control Architecture
Analysis of the Nonlinear Adaptive Dynamic Inversion ControlArchitecture During Inlet Unstarts
Conclusions
Extensions
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Extensions
• Enforcing state constraints with a projection operator, andincluding the projection operator in the control laws.
• Combine controllers that can enforce state constraints withfault-tolerant controllers.
• Development of control logic associated with the inlet unstartenvelope for a hypersonic vehicle to determine the appropriatecourse of action to ensure its preservation.
• Development and testing of controllers using an elastic modelof a hypersonic vehicle.
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Questions?
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References I
[1] Heiser, W. H. and Pratt, D. T., Hypersonic Airbreathing
Propulsion, AIAA Education Series, American Institute ofAeronautics and Astronautics, Washington D. C., 1994.
[2] Annaswamy, A. M., Jang, J., and Lavretsky, E., “Adaptivegain-scheduled controller in the presence of actuatoranomalies,” AIAA Guidance, Navigation and Control
Conference and Exhibit, Honolulu, Hawaii, August 2008.
[3] Gibson, T. E. and Annaswamy, A. M., “Adaptive Control ofHypersonic Vehicles in the Presence of Thrust and ActuatorUncertainties,” AIAA Guidance, Navigation and Control
Conference and Exhibit, Honolulu, Hawaii, August 2008.
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References II
[4] Groves, K. P., Sigthorsson, D. O., Serrani, A., Yurkovich, S.,Bolender, M. A., and Doman, D. B., “Reference CommandTracking for a Linearized Model of an Air-breathingHypersonic Vehicle,” AIAA Guidance, Navigation and Control
Conference and Exhibit, San Francisco, California, August2005.
[5] Bolender, M. A., Staines, J. T., and Dolvin, D. J., “HIFiRE 6:An Adaptive Flight Control Experiment,” 50th AIAA
Aerospace Sciences Meeting including the New Horizons
Forum and Aerospace Exposition, Nashville, TN, January2012.
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References III
[6] Johnson, E. N., Calise, A. J., Curry, M. D., Mease, K. D., andCorban, J. E., “Adaptive Guidance and Control forAutonomous Hypersonic Vehicles,” Journal of Guidance,
Control, and Dynamics, Vol. 29, No. 3, May - June 2006,pp. 725–737.
[7] Fiorentini, L., Serrani, A., Bolender, M. A., and Doman,D. B., “Nonlinear Robust Adaptive Control of FlexibleAir-breathing Hypersonic Vehicles,” Journal of Guidance,
Control, and Dynamics, Vol. 32, No. 2, Mar.-Apr. 2009,pp. 401–416.
[8] Parker, J. T., Serrani, A., Yurkovich, S., Bolender, M. A., andDoman, D. B., “Approximate Feedback Linearization of anAir-breathing Hypersonic Vehicle,” AIAA Guidance,
Navigation and Control Conference and Exhibit, Keystone,Colorado, August 2006.
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References IV
[9] Brocanelli, M., Gunbatar, Y., Serrani, A., and Bolender,M. A., “Robust Control for Unstart Recovery in HypersonicVehicles,” AIAA Guidance, Navigation and Control
Conference, Minneapolis, Minnesota, August 2012.
[10] Vick, T. J., “Documentation for Generic Hypersonic VehicleModel,” Tech. rep., U.S. Air Force Research Laboratory,Wright-Patterson AFB.
[11] Pomet, J.-B. and Praly, L., “Adaptive Nonlinear Regulation:Estimation from the Lyapunov Equation,” IEEE Transactions
on Automatic Control , Vol. 37, No. 6, June 1992,pp. 729–740.
[12] Menon, P., Badgett, M., Walker, R., and Duke, E.,“Nonlinear Flight Test Trajectory Controllers for Aircraft,”Journal of Guidance, Control, and Dynamics, Vol. 10, No. 1,Jan.-Feb. 1987, pp. 67–72.
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References V
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