Optimization of Aerodynamic Efficiency for Morphing MAV Wing
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Transcript of Aerodynamic Optimization of a Morphing Airfoil Using
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1
Aerodynamic Optimization of a Morphing Airfoil Using
Energy as an Objective
Howoong Namgoong*, William A. Crossley† and Anastasios S. Lyrintzis‡
Purdue University, West Lafayette, Indiana, 47907-2023
Recent advances in materials science and actuation technologies have led to interest in
morphing aircraft. The research discussed in this paper focuses upon the shape design of
morphing airfoil sections. In the efforts herein, the relative strain energy needed to change
from one airfoil shape to another is presented as an additional design objective along with a
drag design objective, while constraints are enforced on lift. Solving the resulting
multiobjective problem generates a range of morphing airfoil designs that represent the best
tradeoffs between aerodynamic performance and morphing energy requirements. From the
multiobjective solutions, a designer can select a set of airfoil shapes with a low relative strain
energy that requires a small actuation cost and with improved aerodynamic performance at
the design conditions.
Nomenclature
C d = coefficient of dragC l = coefficient of lift
C m = coefficient of pitching moment
C f = coefficient of skin frictionC p = coefficient of pressure
F i = objective functions f i = shape functions M = free stream Mach number
Re = Reynolds number
x = x coordinate of airfoil
y = y coordinate of airfoilU ij = relative strain energy of airfoil i and airfoil j
ξ i = design variables
ε i = reference drag coefficient
I. Introduction
IGNIFICANT research has been conducted about how birds fly to provide inspiration for improved man-madeaircraft1. Birds can change their wing shape to attain maneuverability and maximum performance in different
flight conditions. Recently, the concept of a morphing aircraft has been introduced 2,3. A morphing aircraft might
have fully deformable airfoil sections to change shape in flight. Several efforts showed that this type of morphingleads to aerodynamic performance benefits for the aircraft4,5. The Mission Adaptive Wing (MAW) program6 of the
1980s provides an example of aerodynamic performance increase from using a variable camber wing. Despite the
aerodynamic advantages, the MAW’s variable camber design was impractical due to the increased complexity and
weight increase from the actuation system used on the demonstrator aircraft. After the MAW program, most of the
morphing aircraft related research focused on light weight actuator device development to reduce the weight penaltyfor changing the shape of the aircraft. Examples of this device development include the Smart Wing7 and
SAMPSON8 programs; however, many design strategies for morphing aircraft, such as multi-objective optimization
including aerodynamic performance and morphing cost (actuator weight), have not been investigated fully.
*Graduate Student, School of Aeronautics and Astronautics, Grissom Hall, Student Member AIAA.
† Associate Professor, School of Aeronautics and Astronautics, Grissom Hall, Associate Fellow AIAA.‡ Professor, School of Aeronautics and Astronautics, Grissom Hall, Associate Fellow AIAA.
S
44th AIAA Aerospace Sciences Meeting and Exhibit9 - 12 January 2006, Reno, Nevada
AIAA 2006-132
Copyright © 2006 by the authors. Published by the American Institute of Aeronautics and Astronautics, Inc., with permission.
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The concept of a morphing aircraft1 has generated a new design aspect that must be addressed in aerodynamic
configuration design and optimization. A diverse array of optimization techniques have been applied for traditional
aerodynamic design problems. Gradient-based algorithms such as feasible direction9,10, quasi-Newton11 and adjoint
methods12 have been widely used for airfoil optimization. Recently, stochastic optimization methods (e.g. genetic
algorithms13 and simulated annealing14) have also been applied for aerodynamic optimization 15,16.Generally, in developing the objectives for aerodynamic optimization, a multi-point problem formulation17 is
used for airfoil or wing design. A weighted sum of drag coefficients, computed at various design flight conditions,
serves as the objective, and constraints ensure that the lift coefficient matches specified values at each of the flightconditions. The resulting shape has performance that is essentially a compromise over the flight conditions. In the
case of a morphing aircraft, the wing would be able to change its shape during flight. It should be possible to adjust
the wing shape to the best possible shape for any flight condition encountered by the aircraft; this would suggest that
the morphing airfoil could be designed using a series of single-point problem formulations. However, there is anactuator effort or “cost” associated with these shape changes. Thus, the effort required to effect the morphing must
be included in the optimization process.
The contributions of this paper are the formulation of an energy-objective for morphing airfoil design and the
application of a multi-objective approach to minimize both actuator effort and aerodynamic drag. To investigateenergy as an objective for morphing airfoil shape optimization, typical aerodynamics-only design methods and two
different multi-objective design methods were applied to a morphing airfoil design. These approaches highlight how
strain energy can be included as a measure of morphing airfoil actuation effort. The results demonstrate the trade-off between the morphing energy and the aerodynamic performance.
II. Representative Problem
Some recent studies by the US Air Force Research Laboratory (AFRL) have focused upon a high-altitude, long-
endurance aircraft platform18. A notional representation of this concept appears in Figure 1. This aircraft’s designmission includes a 40+ hour loiter segment, during which
the aircraft will experience a significant weight reduction
as it consumes most of its fuel. If the aircraft is intended to
loiter at a constant altitude and constant airspeed, a fixed
geometry wing would not be operating at its most efficientconditions throughout the mission. However, if the aircraft
utilized a wing with morphing airfoil sections, it would be
possible to change airfoil shape throughout the mission inorder to improve the endurance performance of the
aircraft.Based upon systems studies from AFRL, the required
lift coefficients are known at various times during the longloiter segment. To begin the energy objective
investigations, the flight conditions at three points in time
provide the airfoil shape design conditions. These are
summarized in
Table 1. Near the start of the loiter segment, theaircraft’s weight is high, and the required design lift coefficient is also high. Because of the desire for constant
altitude, constant velocity loiter, the Reynolds number and Mach number for all three conditions are the same. Thelow Mach numbers should not require aerodynamic analyses that include wave drag.
Table 1 Airfoil design conditions.
Condition 1 Condition 2 Condition 3Design lift coefficient 1.52 1.18 0.85Mach number 0.6 0.6 0.6
Reynolds number 1.5×106 1.5×106 1.5×106
III. Aerodynamics Approach
For aerodynamic analysis, the well-known XFOIL19 code is selected as a function evaluator because it provides
rapid calculation of lift and drag coefficient. XFOIL is suitable for high Reynolds number airfoil flows. A linear-
Figure 1 Notional high-altitude, long endurance
aircraft concept.
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vorticity panel method with a Karman-Tsien compressibility correction is used for inviscid calculation. While this is
not generally considered a high-fidelity analysis tool, XFOIL is relatively fast, a requirement for design studies.
XFOIL allows for a good resolution of the airfoil shape and incorporates viscous effects.
To pose the airfoil shape optimization problem when using XFOIL, the design variables describing the airfoil
shape are needed. Several possibilities were investigated in Reference 20. The modified Hicks-Henne21,22 shapefunctions were found to represent an airfoil most accurately and are used here. The design variables are multipliers
that determine the magnitude of the shape function as it is added to the baseline airfoil shape. The y-coordinate positions of the upper and lower surface of the airfoil are then described as functions of the x-coordinate position
using the following equation:
∑ξ+= )()()( AirfoilBase x f x y x y ii(1)
where ξi are the design variables; and f i, the shape functions (i =1, 16 here). Figure 2 provides two plots that depicts
the shape functions and a baseline NACA 0012 airfoil along with the upper and lower limits of the airfoil surfaces.
The left plot shows how the eight shape functions vary as a function of the chordwise position; this plot uses values
ξi=1.0. The right plot shows the available design space using the NACA 0012 base airfoil with the modified Hicks-
Henne shape functions. If all ξi are equal to the upper bound of 0.015, the upper bound airfoil shape is described.
Similary, if all ξi are equal to the lower bound of -0.015, the lower bound shape is found. As a result, all possible
shapes for the airfoil lie between these two bounds.
IV. Strain Energy as an Objective
As mentioned previously, a morphing airfoil could theoretically provide aerodynamically optimal shapes at any
flight condition. However, morphing requires some type of mechanisms to effect shape changes. This work uses the
assumption that the energy needed to change the airfoil shape is proportional to both the actuation system weight
and the power needed by the actuation system. The purpose of this research is to account for the extra cost of morphing devices needed to acquire aerodynamic performance benefits, so an additional objective developed here is
to minimize the strain energy associated with changing the shape of the airfoil.
There are several ways to model the strain energy needed to change the airfoil shape23,24. All of these ways usethe basic idea that the strain energy in a structure is proportional to the square of the change in length of the
structure. In this paper, a simple strain energy model has been considered. Eq.(2) presents the internal linear spring
model concept suggested by Prock, et al23.
0 0.1 0.2 0.3 0.4 0.5 0.6 0.7 0.8 0.9 10
0.1
0.2
0.3
0.4
0.5
0.6
0.7
0.8
0.9
1
x
y
f1 f2 f3 f4 f5 f6 f7 f8
0 0.25 0.5 0.75 1
X
-0.1
-0.05
0
0.05
0.1
0.15
Y
NACA0012Maximum LimitMinimum Limit
Figure 2 Modified Hicks-Henne shape functions (left) and design space available using the NACA 0012 base
airfoil (right)
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∑∑==
Δ=Δ=n
i
i
i
n
i
ii L L
EA Lk U
1
2
1
2
2
1
2
1 (2)
In this equation, U is the strain energy; k i, is the spring constant, EA is the spring axial stiffness, and Δ Li is the spring
deformation. With no real actuation system envisioned as yet, the spring model strain energy objective does not need
to include the EA terms. This model assumes that springs connect the upper and lower airfoil surfaces; as the airfoil
morphs, the springs deform, which corresponds to an amount of strain energy. Figure 3 presents a simpleillustration of this model.
To formulate the objective function, relative strain energy terms, U ij, representing the strain energy associated
with changing from shape i to shape j. Currently, the objective incorporating strain energy seeks to minimize the
maximum relative strain energy value associated with the
shape changes. For the three conditions used here, theobjective appears as given in Eq.(3).
Minimize [Max(U 12, U 23, U 13)] (3)
This current strain energy model does not directlyaccount for an actuation or mechanization strategy to change
the airfoil shapes. As physically realizable actuation
strategies become available, (like those suggested in Refs. 25and 26) models of these strategies should be used to also
assess strain energy or actuation energy in the same
optimization framework as the simple spring model
presented above.
V. Optimization Algorithm
Since its first descriptions, the Genetic Algorithm (GA)
has been applied to many engineering optimization problems. A genetic algorithm is a computational representation
of natural selection observed in biological populations27. A GA has the ability to search highly multimodal,
discontinuous design spaces and also locates designs at, or near, the global optimum without requiring a good initialdesign point. Because the min-max objective formulation will have discontinuous derivatives and because airfoil
shape design problems appear to frequently have local minima, the GA provides a search method that would not be
hindered by these issues.The population size and mutation rate were selected using empirically derived guidelines 28 for GA using
tournament selection and uniform crossover. Seven bits represent each of the 16 shape function multipliers (8 for
upper surface and 8 for lower surface) in the case of a single airfoil design, for a total chromosome length of 112
bits. In this research, 95% BSA(Bit-String Affinity) stopping criteria29
is applied for all aerodynamic-only designs. Normally, obtaining 95% BSA for this problem requires about 300 GA generations.
Using a GA for design optimization can be computationally expensive. To overcome the computational time
problem, parallelization of the GA is needed. Following the approach of Ref. 30, a manager-worker type
parallelization is applied to convert a serial GA into a parallel program, and a Linux-Cluster machine is used for
computation. Because a relatively small communication time is needed for the parallel GA, the code scales well onthe 52-Processor Linux Cluster used in this effort.
VI. Investigations and Results
Two typical aerodynamics-only design problems and the suggested energy-based multiobjective design areinvestigated. The aerodynamics-only problems provide the extremes of the tradeoff between low drag and low strain
energy.
The design variables are used to describe the airfoil shape as shown in Eq.(1). For the single-point and multi- point aerodynamics-only design, 16 design variables are needed. In the cases using strain energy as an objective, a
total of 48 design variables (16 for each of the three flight conditions) are needed to describe shapes for each design
condition. The NACA0012 airfoil is selected as a base airfoil for all shapes. The same modified Hicks-Henne shape
functions and design variable bounds (ξi=± 0.015) that were described previously are used here. Thus, the same
limits on upper and lower surface shapes shown in Fig. 2 are provided.
Internal springs connecting upper and lower surface
ic L )/(Δ
ic L )/(
Springs contract (or expand) to meet new airfoil shape
Figure 3 Internal linear spring model for strain
energy.
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In optimal airfoil shape design, the angle of attack also can be, and often is, used as one of the design variables,
so that the solution contains the shape and angle of attack needed to minimize drag and meet the lift constraints.
However, in this research, the angle of attack was not a design variable, because the XFOIL has a built in trimming
subroutine to find the angle of attack that satisfies the design lift constraint. This process might reduce the
complexity of the design space and help find a global optimum design, because the number of design variables issmaller. Also, this trimming can get rid of the possibility that two different airfoil shapes at different angles of
attack have same lift coefficient.
A. Aerodynamics Only Investigation
1. Three single point airfoil designs
With no consideration of the energy needed to change themorphing airfoil’s shape, the airfoil would be able to adjust
so that its performance at any given flight conditions would match the result of a single point optimization at the flight
condition. Each problem results in a single shape that
minimizes C d at each condition. Eq.(4) shows the single-
point problem objectives correspond to each of the flightconditions.
Minimizeid C
Subject toill C C = )3,2,1( =i (4)
In Figure 4, the resulting airfoils from the three single-
point optimization runs are superimposed on each other to
demonstrate the type of shape changes that would berequired for morphing the airfoil to meet the three flight
conditions given in Table 1. These are intended to represent
the best possible aerodynamic shapes for the airfoils.
2. Multi-point optimization
The multi-point approach uses the weighted sum of dragcoefficients as the objective function shown in Eq.(5),
following a typical formulation for this problem type17. Thisapproach finds a single fixed geometry shape that
compromises between all three flight conditions. The lift
coefficient constraints are satisfied by trimming the airfoil.This aerodynamics tradeoff results in an airfoil with higher
drag at each specific flight condition compared to the
corresponding single-point optimized airfoils. Because a
single airfoil shape is acquired by this approach, the airfoil
requires no strain energy.
Minimize321
3
1
3
1
3
1d d d C C C ++
Subject toill C C = )3,2,1( =i (5)
Results of the two methods are compared in Table 2. The single-point design results have lower drag than the
multi-point design results, as expected. This is because the single-point designs have only one objective which is to
minimize drag at one flight condition, but the multi-point design solution is a compromise solution over all threeflight conditions. The multi-point solution is a minimum energy solution, because the result of the multi-point
design is a single airfoil. Thus, the relative strain energies in Table 2 are all zero for the multi-point design. The
0 0.25 0.5 0.75 1
X
-0.25
-0.2
-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0.2
0.25
Y
DesignCl=0.85
DesignCl=1.18DesignCl=1.52
Figure 4 Airfoil shapes from single-point
optimizations.
0 0.25 0.5 0.75 1
X
-0.25
-0.2
-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0.2
0.25
Y
Multi-PointOptimization
Figure 5 Airfoil shapes from multi-point
optimizations.
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relative energies for the single-point solutions shown in Table 2 are calculated following the energy model described
in Eq.(2). Therefore, the values in Table 2 indicate the range of tradeoff available for a morphing airfoil. The three
single-point shapes are the best possible aerodynamic solution, while the multi-point shape is the best possible
energy solution.
Table 2 Drag comparison of aerodynamics only design
Cd 1 Cd 2 Cd 3 U 12 U 23 U 13
single-point 0.005024 0.007015 0.010249 0.00704 0.00189 0.01241
multi-point 0.007356 0.008178 0.010649 0 0 0
B. Energy-Based Investigation
In the design approach used here, strain energy is proposed as another objective to encourage minimum actuationrequirements for morphing airfoils. Because the aerodynamic performance also needs to be included, the problem
becomes multi-objective.
For the multi-objective optimization, the objective function is a vector function whose components are individual
objectives. In a problem with more than one competing objective, there exist a number of solutions called the
Pareto-optimal set31, instead of a single best solution. This research employs two multi-objective methods (i.e.ε -
constraint and N -branch tournament Genetic Algorithm32) to address the strain energy and drag as objectives.
1. ε -constraint approach
For this problem, there is no guarantee that the multi-objective approach will find an aerodynamically better shape than the multi-point aerodynamics only design. To account for this problem, constraints on the drag
coefficient are enforced via a penalty function in the ε -constraint approach. The reference drag coefficient values
(ε i) are chosen between the values of the single-point
results and multi-point results of aerodynamics only
design. By varying the values of ε i for different runs of the
optimizer, different Pareto optimal solutions are found.
The formulation of the ε -constraint approach is described
in Eq.(6).
Minimize1F
Subject toiF ε ≤2
and, jll C C = (j=1,2,3)
Where
( )[ ]
1
1323121
,,max
C
U U U F = ,
2
31
31
31
2321
C
cccF
d d d ++= ,
C 1=C 2=0.01 (6)
Figure 6 shows the Pareto set found from the ε -
constraint approach. In Fig.6, the “energy-based” points
represent the solutions obtained by including the energyobjective function in the multiobjective problem. The single-point and multi-point results of the aerodynamic-onlydesigns are also plotted for comparison. Figure 6 shows that tradeoff morphing airfoil solutions exist between the
two extreme points represented by the multi-point and single-point solutions.
0.70
0.75
0.80
0.85
0.90
-0.2 0.3 0.8 1.3 1.8
F 1 (Energy Objective)
F 2
( D r a g O
b j e c t i v e )
energy-based
multi-pointsingle-point
Figure 6 Pareto set from ε -constraint approach.
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Figure 7 shows the set of three shapes associated with
one morphing airfoil tradeoff solution selected from the
Pareto-optimal set. Thus, this airfoil set has better
aerodynamic performance than the multi-point design and
also has smaller strain energy than the single-point design.The morphing airfoil set in Figure 7 has a drag objective of
0.765, which is lower than the multi-point drag objective
of 0.864. Also, the morphing airfoil in Figure 7 has anenergy objective of 0.260, which is lower that the set of
single-point shapes of 1.240. This airfoil set shows little
difference in the lower surface to reduce energy, but has
more variation in the upper surface to reduce drag and maintain required C l values.
2. N-Branch Tournament Genetic Algorithm
Many different versions of modified Genetic
Algorithm have been used for multi-objective
optimization. An appropriately modified Genetic
Algorithm approach can generate a large number of
designs that represent the Pareto set for a multi-objective problem with similar computational effort required to
solve a single objective problem with a genetic algorithm.
In this research, the N -Branch Tournament Genetic Algorithm33 is used as a multi-objective Genetic Algorithm. N -branch tournament differs from non-dominance ranking approaches such as Multi-Objective Genetic Algorithm
(MOGA)34 because it uses the selection operator to perform multi-objective design rather than formulation of a
single fitness function. In N -branch tournament selection, designs compete once on a fitness value associated with
each objective. Eq. (7) is the problem statement for this optimization.
Minimize
( )[ ]
( )⎪⎪⎭
⎪⎪⎬
⎫
⎪⎪⎩
⎪⎪⎨
⎧
++=
2
31
31
31
1
132312
321
,,max
C
ccc
C
U U U
F d d d
G
Subject toil lC C = (i=1,2,3)
Where C 1=C 2=0.01 (7)
Figure 8 shows the Pareto set found from one run (1,000 generations) of the N -branch tournament GA. With less
effort, many more tradeoff solutions were acquired from the N -branch tournament GA than from the ε -constraint
method. Instead of using the BSA stopping criteria like in the aerodynamics-only case, here the Pareto set is
assumed to be converged after 1,000 iterations. Few changes were observed in the Pareto set after about 800
generations.
Figure 9 is one of the tradeoff solutions selected from the Pareto set shown in Figure 8. The morphing airfoil in
Figure 9 has a drag objective of 0.765 and energy objective 0.2. The morphing airfoil shapes in Figure 7 and Figure9 and seem similar, but the energy objective of the airfoil shapes in Figure 9 is slightly less. The airfoil shapes in
Figure 9 are much closer to each other than the single-point generated airfoil shapes in Figure 4, which follows thatthe strain energy of the morphing airfoil in Figure 9 is smaller than that associated with the three single-point
shapes.
0 0.25 0.5 0.75 1
X
-0.25
-0.2
-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0.2
0.25
Y
Design Cl=0.85
Design Cl=1.18Design Cl=1.52
Figure 7 Airfoil shapes from energy based design
(ε -constraint approach)
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Figures 10-12 present airfoil shapes and C p distributions associated with the three flight conditions. The left-
hand plot shows the single-point shape designed for the given flight condition, the shape of the multi-point design
problem, a morphing airfoil shape obtained via the ε -constraint method (See Fig. 7), and the morphing airfoil shapefor the given flight condition obtained via the N -branch GA (see Fig. 9)
The airfoil shape plots show that the shapes generated using energy as an objective compromise between energy
and drag when compared with the single-point shapes and the multi-point design, because the multi-objective shapes
lie between the two aerodynamics-only designs.One noticeable trend from the airfoil and C p comparison is that, as the design C l increases, the difference of the
shapes decreases. This might be due to the fact that as the design C l increases, it is more difficult to find airfoils that
satisfy the high C l with small drag.
0.70
0.75
0.80
0.85
0.90
-0.2 0.0 0.2 0.4 0.6 0.8 1.0 1.2 1.4
F 1 (Energy Objective)
F 2
( D r a g O b j e
c t i v e )
N-branchmulti-point
single-point
Figure 8 Pareto set from N-Branch tournament GA.
0 0.25 0.5 0.75 1
X
-0.25
-0.2
-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0.2
0.25
Y
Design Cl=0.85
Design Cl=1.18Design C
l=1.52
Figure 9 Airfoil shapes from energy based design (N-
Branch tournament GA).
0 0.25 0.5 0.75 1X
-0.25
-0.2
-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0.2
0.25
Y
single-pointmulti-pointε-constraintN-branch
Design Cl=0.85
M=0.6Re=1.5E6
0 0.25 0.5 0.75 1X
-3
-2.5
-2
-1.5
-1
-0.5
0
0.5
1
1.5
C p
single-pointmulti-pointε-constraintN-branch
DesignCl=0.85
M=0.6Re=1.5E6
Figure 10 Airfoil comparison (left), C p distribution comparison (right) (Design lC =0.85)
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To see the strain energy reductions more clearly, the strain
energy (see Eq.(2)) distribution along the airfoil is plotted onthe NACA0012, which is not the actual designed airfoil shape.
For example, if the control point associated with a location on
the lower surface trailing edge has a large displacement
between two airfoil shapes, a large bar is placed at thecorresponding control point on the NACA 0012 airfoil section.
In this manner, a visual representation can be made to show
which section of the airfoil is associated with the highest strainenergy. In Fig. 15, the strain energy associated with springs at
the rear upper surface of the single-point airfoil have a
significant amount of strain energy associated with moving
from shape 1 to shape 3 as displayed by the large bars in this
area of the airfoil.The single point and energy-based designs are compared.
Figs. 14-15 show that the strain energy (U 23 , U 13) in the multi-
objective designs has been reduced significantly from that of the single point shapes.
0 0.25 0.5 0.75 1X
-0.25
-0.2
-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0.2
0.25
Y
single-pointmulti-pointε-constraintN-branch
Design Cl=1.18
M=0.6Re=1.5E6
0 0.25 0.5 0.75 1X
-3
-2.5
-2
-1.5
-1
-0.5
0
0.5
1
1.5
C p
single-pointmulti-pointε-constraintN-branch
Design Cl=1.18
M=0.6Re=1.5E6
Figure 11 Airfoil comparison (left), C p distribution comparison (right) (Design lC =1.18)
0 0.25 0.5 0.75 1
X
-0.25
-0.2
-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0.2
0.25
Y
single-pointmulti-pointε-constraintN-branch
Design Cl=1.52
M=0.6Re=1.5E6
0 0.25 0.5 0.75 1
X
-3
-2.5
-2
-1.5
-1
-0.5
0
0.5
1
1.5
C p
single-pointmulti-pointε-constraintN-branch
Design Cl=1.52
M=0.6Re=1.5E6
Figure 12 Airfoil comparison (left), C p distribution comparison (right) (Design lC =1.52)
0
0.2
0.4
0.6
0.8
1
0.10
0.10
0.10
0.1
0
1
2
3
4
5
6
7
x 10−4
X
y
E n e r g y
single−point
ε −constraint
N−branch
Figure 13 Strain energy distributions (U 12)
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VII. Transonic Morphing Airfoil
As another application of the morphing airfoil design strategy described in the previous sections, a transonic
morphing airfoil design is performed. The main difference from the sensorcraft problem is the flight speed regimeof the morphing aircraft. For this application, the speed regime varies from subsonic to transonic, and the altitude
changes from low to high. This application requires a Navier-Stokes code for flow evaluation to capture the physics
of the shock wave in the transonic regime. The importance of the energy-based optimization is increased here,
because a greater shape change is expected for the optimal shapes compared to the low speed sensorcraft problem.Also, small changes in the airfoil shape could have a large impact in the aerodynamic performance when
considering transonic flow.
A. Problem Definition
The flight conditions considered in this research reflect a notional transonic morphing UAV(Unmanned AerialVehicle). This UAV has a multi-mission capability which includes features of a high altitude reconnaissance UAV
and a high-speed combat UAV.
To reduce the computational time while keeping the aspects of morphing airfoil strategy, only two design
conditions were selected for this study. The selected mission segments are the dash and loiter missions; Table 3
presents these flight conditions. These mission conditions are expected to require large shape change for optimalaerodynamic design. The loiter mission is defined based on the Global Hawk UAV35. In addition, this problem
assumes that the aircraft can significantly reduce its wing area for the dash segment. This type of area change was
presented as a goal of the DARPA morphing aircraft structure program3.
Table 3 Transonic Morphing UAV Mission Profile
Mach Altitude ( ft ) C L Re Wing Area
Dash 0.8 5000 0.20 1.98E+07 25%
Loiter 0.6 60,000 1.00 1.77E+06 100%
B. Objective Function
The objective functions are described in Eq.(8). Only one relative strain energy is needed for the two design
conditions.
0
0.2
0.4
0.6
0.8
1
0.10
0.10
0.10
0.1
0
1
2
3
4
5
6
7
x 10−4
X
y
E n e r g y
single−point
ε −constraint
N−branch
Figure 14 Strain energy distributions (U 13)
0
0.2
0.4
0.6
0.8
1
0.10
0.10
0.10
0.1
0
1
2
3
4
5
6
7
x 10−4
X
y
E n e r g y
single−point
ε −constraint
N−branch
Figure 15 Strain energy distributions (U 23)
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minimize :
⎪⎭
⎪⎬⎫
⎪⎩
⎪⎨⎧
+=
21 2
1
2
1
12
d d C C
U
F G
Subject to: 2.01=lC , M =0.8, Re=1.98E7
0.12=lC , M =0.6, Re=1.77E6 (8)
C. Flow Solver, Design Method and Parameters
The TURNS(Transonic Unsteady Rotor Navier-Stokes)36 code is the flow solver for this problem, because it was
readily adapted to this task. The TURNS code was originally developed to research the unsteady flow around arotor blade, however this code can be used for a 2-D airfoil. In the TURNS code, the inviscid flux is calculated
based on an upwind-biased flux-difference scheme originally suggested by Roe37. To acquire higher order accuracy
the Van Leer MUSCLE(Monoton Upstream-centered scheme for the sonservative laws approach)38 is applied withflux limiters. A 129×30 grid arrangement and resolution was found to be a good compromise between accuracy and
efficiency and applied in this problem (see details in Reference 20). The convergence history of this problem
generally showed that after 1500 iterations, the difference of C l and C d between subsequent iterations was less than5
10−
. From this result, an upper limit of 1500 flow solver iterations are used for each solution here to reduce thecomputational cost without paying a great penalty for accuracy. The same parallel GA described in previously isused for this problem, and the number of design variables is 16 for each airfoil shape (for a total of 32 variables
when including energy as an objective). The RAE2822 airfoil is used as the base airfoil, because it is originally
designed to reduce wave drag in transonic flight conditions. The resolution of the GA is set to 5 bits per design
variable for this problem, which is less than the sensorcraft case (7 bits), in order to control computational cost. TheGA parameters for population size (256) and mutation rate (0.00098) are selected following the guidelines of Ref.
28.
D. Aerodynamics-only Result
As before, an aerodynamics-only optimization isconducted to identify the extremes of the tradeoff between
the drag objective and the energy objective. For thistransonic morphing airfoil problem, the best solutions after 100 GA generations are used as converged solutions. This
stopping criterion also limits computational expense. Even
with these steps to limit to compute times, this requires
76,800 function evaluations and 67 hours of computational
wall-time with 30 CPUs. The single point optimizationresults are shown in Figure 16. As expected, the
aerodynamically best airfoils show a large difference in
shape between the two flight condition, compared to the
difference in shape seen for the subsonic sensor craft problem. Figure 17 presents the resulting shape from the
multi-point design case. 0 0.25 0.5 0.75 1X
-0.25
-0.2
-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0.2
0.25
Y
Designcondition1Designcondition2
SingleP ointOptimization
Designcondition1 : M=0.6, Cl=1.0, Re=7.9E6
Designcondition2 : M=0.8, Cl=0.2, Re=2.0E7
Figure 16 Best airfoil shape (Single-point
optimization)
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E. Energy-based Design Results
For this problem, the N -branch tournament GA is
used to generate a Pareto-set. Because computational
time is high for this problem, the classical multi-
objective methods (weighted sum or ε-constraint) are not
affordable with the available computing power. The
Pareto-set found by the N -branch tournament GA after 300 generations is shown in Figure 18. Figure 18 shows
that the converged Pareto set does not have low drag,
high energy solutions and this appears to be the result of low geometric resolution of the possible airfoil sets.
One Pareto front solution point (F 1=0.199, F 2=1.202)
from Fig. 18 is selected, and the airfoils are drawn in
Figure 19. The shapes are relatively close to each other,
compared with the shapes found by the single pointaerodynamic-only design (Figure 16). Also, the scale
difference of the energy objective value in Fig. 8 and
Fig. 18 reflects that the shape change of the solutionairfoil sets is relatively larger than the subsonic airfoil
solution sets of the sensorcraft application. Because the
larger change in shape provided a broader tradeoff between aerodynamic and actuation energy, the importance of the morphing airfoil optimization strategy suggested
in this paper might be increased compared to the subsonic application and suggests that this approach can identify
shapes that could save significant actuation energy.
VIII. Conclusions
Minimization of actuation energy in designing a morphing aircraft is very important to enhance the advantagesfrom the aerodynamic superiority of a morphing aircraft. In this research, a strain energy objective was formulated
and a multi-objective optimization approach was employed to minimize both actuator energy and aerodynamic drag.
Two multi-objective optimization strategies to design an airfoil set for morphing aircraft are applied to a low-
speed, incompressible flow problem and a transonic flow problem. The relative strain energy needed to change
0 0.25 0.5 0.75 1X
-0.25
-0.2
-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0.2
0.25
Y
Multi PointOptimization
Designcondition1 : M=0.6,Cl=1.0,Re=7.9E6
Designcondition2 : M=0.8,Cl=0.2,Re=2.0E7
Figure 17 Best airfoil shape (Multi-point
optimization)
1
1.1
1.2
1.3
1.4
1.5
1.6
1.7
-0.5 0 0.5 1 1.5 2 2.5 3
F 1 (Energy Objective)
F 2
( D r a g O
b j e c t i v e )
Single-point
Multi-pointN-branch
Figure 18 Pareto-front of transonic morphing wing
case
0 0.25 0.5 0.75 1X
-0.25
-0.2
-0.15
-0.1
-0.05
0
0.05
0.1
0.15
0.2
0.25
Y
Design condition1Design condition2
EnergyBasedOptimization
Designcondition1 : M=0.6, Cl=1.0, Re=7.9E6Designcondition2 : M=0.8, C
l=0.2, Re=2.0E7
Figure 19 Airfoil shapes from energy based design
( N -Branch tournament GA)
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from on airfoil shape to another is presented as a design objective along with the drag objective. From this multi-
objective optimization strategy, we found tradeoff designs of low actuation energy and low drag that lie between the
multi-point shape and the set of single-point shapes. Through these optimization processes, engineers can seek a
solution that maximizes the benefits of the morphing technology, while minimizing the actuation cost.
Acknowledgments
The authors would like to thank Jason Bowman and Brian Sanders of the Air Force Research Laboratory for providing information about the high-altitude, long-endurance aircraft. A significant portion of this work was
supported by the Air Force Research Laboratory award number F33615-00-C-3051. The calculations were performed on a 104-node cluster acquired by a Defense University Research Instrumentation Program (DURIP)
grant.
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