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A Linear Least-Squares Solution to Elastic Shape-from-Template

Abed Malti1 Adrien Bartoli2 Richard Hartley31 Fluminance/INRIA, Rennes, France

2 ALCoV/ISIT, UMR 6284 CNRS/Universite dAuvergne, Clermont-Ferrand, France3Australian National University and NICTA, Canberra, Australia

Abstract

We cast SfT (Shape-from-Template) as the search of avector field (X, X), composed of the pose X and the dis-placement X that produces the deformation. We proposethe first fully linear least-squares SfT method modeling elas-tic deformations. It relies on a set of Solid Boundary Con-straints (SBC) to position the template at X in the deformedframe. The displacement is mapped by the stiffness matrixto minimize the amount of force responsible for the defor-mation. This linear minimization is subjected to the Repro-jection Boundary Constraints (RBC) of the deformed shapeX + X on the deformed image. Compared to state-of-the-art methods, this new formulation allows us to obtainaccurate results at a low computation cost.

1. IntroductionThe SfT problem is to reconstruct a 3D deformed surface

from its image and a 3D shape template. Most SfT methodsrely on point correspondences between the template and theimage, defining Reprojection Boundary Constraints (RBC).These constrain 3D points to lie on the sightlines from theimage, leaving an infinite number of possible 3D deforma-tions. Physics-based or statistics-based priors are then usedas additional constraints. In physics-based priors, the ge-ometric and mechanical priors are the most used. Whilegeometric priors tend to use invariant measures betweendeformations, mechanical priors represent the physics thatrules the deformation. In parallel to an extensive study ofisometry-based priors [3, 5, 17, 15, 18, 19], mechanical pri-ors [1, 2, 10, 7] have recently become a line of investigationin SfT. They have potential for real applications since theyaddress a wider class of deformable objects such as organs,tissues and other elastic objects. In comparison, isometricSfT is limited to paper and some types of clothes.

Current geometric/mechanical SfT methods suffer froma certain number of caveats that are summarized in table1. First, the types of deformations: geometric approaches[3, 9] may not behave well when the prior is not fulfilled bythe deformation, while mechanical methods [10, 1] cover alarger range of deformations (such as linear elasticity). Sec-ond, the tradeoff between accuracy and speed of estimation.

Analytical solutions [3] are fast but with lower accuracy.Non-linear optimization methods [9, 10] are more accuratebut at a higher computation cost. Moreover, their accuracydepends on the initialization and on some hyper-parameters.Methods based on Kalman filtering [1] also require an ini-tialization step besides the fact that errors may accumulateover the considered time frame. In summary, physics-basedapproaches lack a method which is (i) able to exploit themechanical constraints to cover a large deformation range,(ii) robust to noise, and (iii) both accurate and fast. Devel-oping such a method is the main goal of this work. Theanswer we propose is to use mechanical constraints into alinear least-squares estimation framework.

We use finite elements (FEM) to represent the surfaceand the deformation. This is particularly adapted to SfT andfits the problem we want to solve. Indeed, only the finitediscrete set of point correspondences has a natural bound-ary condition through the RBC. Any other point of the sur-face is free from boundary conditions and is only subject tothe physical prior. Thus, we use the finite set of correspon-dences as nodes of the elements (triangles). Each elementis subject to the mechanical laws that rule the deformation.We use a weak formulation of these laws to derive a linearrelation (via the stiffness matrix) between the displacementof the nodes and the external deforming forces. The assem-bly of all elementary matrices reconstruct the global stiff-ness matrix that links the global external deforming forceto the global deformation X. Minimizing this force sub-ject to the RBC is a linear least-squares problem that can besolved very efficiently.

2. State-of-the-ArtStatistical constraints usually represent the deformation

as a linear combination of basis vectors, which can belearned online either for face reconstruction [12] or forgeneric shapes [17, 15, 19]. Non-linear learning methodswere applied in human tracking [16] and then extended tomore generic surfaces [18].

Physical constraints include spatial and temporal sur-face priors. The isometry constraint [5] requires that anygeodesic distance is preserved by the deformation. Thisapproach has proven its accuracy for paper-like surfacesand was extended to conformal deformations [9, 3]. [3]

1

Method Deformation Time Acc Noise Init/params

Isometric Conformal Elastic

analytic-GbM-[3] + + + +iterative-GbM-[9] + + + +

iterative-MbM-[10] + + + + + sequential-MbM-[1] + + + + +

linear-MbM-Proposed + + + + + + +

Table 1. Strong (+) and weak (-) points of state-of-the-art physics-based SfT methods. GbM stands for geometric-based methodand MbM for mechanics-based methods. Time is the computa-tion cost. Acc is the accuracy of the method to recover the de-formed shape. Noise is the sensitivity of the method to imagenoise. Init/params tells if the method requires an initial shape orhyper-parameters (-) or not (+). Isometric SfT methods are limitedto isometric deformations and are not mentioned.

X

known

reprojection

unknown non-rigid

mapping

rigid mapping

computed

from state-of-the-art

template

known

2D-3D warp

solid boundary

unknown

rigid positioning

of template

Figure 1. New formalization of the physics-based SfT. The dis-placement field at the solid boundary point is the zero 3-vector.

studied the well-posedness of both the isometric and con-formal cases. The first SLAM (Simultaneous LocalizationAnd Mapping) method for elastic surfaces was attemptedwith fixed boundary conditions [1] and later extended tofree boundary conditions [2]. This approach relies on theNavier-Stokes fluid-flow equation. It makes use of FEM tomodel the surface and approximates the deformation forceswith Gaussians. Both the surface and the forces are es-timated using an EKF (Extended Kalman Filter). It hasto be noticed that SLAM and SfTare conceptually differ-ent. In the former a time sequential smoother is embed-ded in a Bayesian a-posteriori estimator. At the initializa-tion the scene has to be static. Recently [10] proposed anSfTmethod with mechanical priors. The approach relies onstretching energy minimization under reprojection bound-ary conditions. [7] tested a similar approach with differentmechanical models and orthographic projection. Thoughthis has proven effective, it has the drawbacks of non-lineariterative methods: the need for an initialization (that is dif-ficult to find) and for hyper-parameter setting to obtain anoptimal accuracy.

FEM techniques with mechanical priors have been ex-tensively used in medical imaging to solve organ segmen-tation from 3D volume scanning modalities [13, 20]. How-ever these methods do not address the registration problemas is usually done in SfT.

3. Mathematical FormulationLet n be the number of point correspondences. We pro-

pose to formalize SfT as follows: find the 3D displacementfield (X, X) R3n R3n, where: (i) X minimizes thenorm of the applied forces for the deformation, (ii) X + Xsatisfies the RBC, and (iii) X is a rigid positioning of thetemplate shape in the deformed frame thanks to the SBC.See figure 1 for an illustration. Formally speaking, finding(X, X) involves two main steps:

1. Find X from X0 with a PnP method applied to thesolid boundary points of SBC. X0 is the template posein the world coordinate frame.

2. Find X such that:

minXR3n

1

2 K X 2 s.t.

{P X = b RBCS X = 0 SBC

(1)

Matrix K is the stiffness matrix of size 3n3n. Note thatf = K X is thus the vector of external forces to be mini-mized. P is an n-block diagonal matrix of dimension 2 3per block. P and b enforce the fact that the n points mustlie on the sightlines that pass through the n correspondingpoints in the deformed image. S is an m 3n sparse ma-trix. It adds m depth displacement constraints which to-gether with the corresponding 2m, among 2n, equations ofRBC set the m solid boundary points. The constructionof matrix P and vector b are straightforward. Considera point X + X on the deformed shape and its reprojec-tion =

(x y

)>in the image. The RBC for this point

provides two non-homogeneous equations in the unknownpoint displacement X =

(u v w

)>. We use perspec-

tive projection and assume that the effect of the intrinsicparameters were undone on the image coordinates, whichgives:

U + u = x(W + w)

V + v = y(W + w)(2)

or in matrix form as:(1 0 x0 1 y

)

P

uvw

= (xW UyW V

)

b

, (3)

whereX =(U V W

)>. The global matrix P is written

as:

P =

P 1 0 00 P i 00 0 Pn

(4)and b is written as:

b =(b1 bi bn

)>(5)

The next sections are dedicated to the construction of matrixK with the related assumptions of deformation modeling.

2

xyv

ux y plane y z plane

@yw

y

yz

x z planex

@xw

z

y

x

mid-surface

h

z

x

y

deforming

Figure 2. Local in-plane and out-of-plane deformations. To sim-plify the representation, we do not consider transverse shear in thisexample.

4. Mechanical ModelingWe adapt the plate theory [4] to surfaces which we as-

sume have locally planar properties (2-manifolds). Theequations of plate theory are written in local coordinates(tangent vectors and normal). Consider first a small flat sur-face, called the plate reference surface or simply the mid-surface . We put a local coordinate system xyz on themid-surface, x and y being the in-plane axes and z the out-of-plane axis. Extending h/2 above and h/2 below the zaxis gives the whole surface with thickness h. The onein the +z direction is by convention called the top surface(seen by the camera) whereas the one in the z direction isthe bottom surface (z = 0 being the mid-surface). Such athree dimensional body is called a plate if the thickness his everywhere small, but not too small, compared to a char-acteristic length L of the local plate mid-surface. The termsmall is to be interpreted in the engineering sense and not inthe mathematical sense. For example, h/L is typically 1/5to 1/100 for most plate structures.

Figure 2 illustrates the different variables of deform-ing an elementary plate. The local displacement X =(u v w

)>represents the deformation shift from an ini-

tial pose X . The mechanical laws applied to a deforminglocal plane relates this shift to the deforming forces. In whatfollows, we make explicit the physical relation betweenthese variables and the deforming forces. In plane stresstheory, both anisotropic scaling and shearing are taken intoaccount. The equations of equilibrium relates the stress (in-ternal body forces) to the external forces:

xx

+xyy

+xzz

+ fx = 0

xyx

+yy

+yzz

+ fy = 0

xzx

+yzy

+ fz = 0

(6)

where(fx fy fz

)>are the components of the exter-

nal body forces per unit volume. x, y are the in-plane

axial stress component. xy , yz and xz are the shearstress components. For a thin material, the transverse ax-ial stress z is neglected since we assume that the thicknessbarely changes after deformation. These equations repre-sent the combined bending and transverse shear deforma-tion on thin materials. The bending stress components are(x y xy

)>and the transverse shear stress compo-

nents are(xz yz

)>. The bending behaviour is asso-

ciated with in-plane deformations and the transverse shearbehaviour is associated with the rotation of surface normalsafter deformation.

The constitutive equation provides the relationship be-tween the stresses and strains. For a homogeneous andisotropic material, the in-plane stress-strain relation is: xy

xy

= E1 2

1 0 1 00 0 12

Db

xyxy

, (7)

where x, y are the in-plane axial strain and xy is the in-plane shear strain. E is Youngs modulus and is Poissonsratio. The transverse shear stress-strain relation is:(

xzyz

)=

(E

2(1+) 0

0 E2(1+)

)

Ds

(xzyz

)(8)

where xz and yz are the rotation angles about respectivelythe y and x axes of the local mid-surface caused by thetransverse deformation. The in-plane strains are related tothe displacement by what is called the in-plane kinematicequation: xy

xy

= uxvyuy +

vx

(9)The transverse shear strains are related to the displacementby what is called the out-of-plane kinematic equation:(

xzyz

)=

(uz +

wx

vz +

wy

)(10)

Combining all these mechanical equations results in asecond order Partial Differential Equation (PDE) in the dis-placement vector. This PDE requires the displacement tobe twice continuously differentiable. Moreover, using FEMwith such an order is not as stable as for a first order sincethe computation would require second order derivations.For this reason, we derive a weak formulation at first or-der. This new obtained PDE requires the displacement tobe continuously differentiable and can be easily handled byFEM.

5. Weak FormulationThe weak formulation method derives from distribution

theory. First, it uses scalar products of the PDE with so

3

called test functions. Second, thanks to integration by parts,the derivatives on the unknowns are transported to test func-tions and boundary conditions are exhibited. Finally, aftersome appropriate manipulations, we end up with a first or-der PDE that can be represented easily with FEM.

5.1. Scalar Product with Test FunctionsMultiplying equation (6) by the test functions(

)>

, we obtain:

h2

h2

>xx +

xyy +

xzz

xyx +

yy +

yzz

xzx +

yzy

d dz+ h

2

h2

>fxfyfz

d dz = 0,(11)

which is valid for any(

) R3 that fits the SBC.

Here, we denote d = dx dy. Splitting up the parts relatedto the bending and transverse shear deformations gives: h

2

h2

(

)>(xx +

xyy

xyx +

yy

)d dz+

h2

h2

>

xzzyzz

xzx +

yzy

d dz+ h

2

h2

>fxfyfz

d dz = 0.(12)

5.2. Integration by PartsTo remove the derivation on the bending stress and the

transverse shear stress in equation (12), we use integrationby parts:

h2

h2

xy

y +

x

> xy

xy

d dz+ h

2

h2

(z +

x

z +

y

)>(xzyz

)d dz+

h2

h2

>fxfyfz

d dz h

2

h2

(

)>(NxNy

)d dz

h2

h2

(+

+

)>(xznzyznz

)d dz = 0,

(13)

where z is the boundary of z. Nx = xnx+xynyandNy = xynx+yny are the in-plane stress componentsat the boundaries.

(xznz yznz

)are the transverse shear

components related to the displacement at the boundariesand

(nx ny nz

)>is the surface normal at the bound-

ary points. Substituting the constitutive equation (7) in (13)gives:

h2

h2

xy

y +

x

>

Db

xyxy

d dz+ h

2

h2

(z +

x

z +

y

)>Ds

(xzyz

)d dz+

h2

h2

>fxfyfz

d dz h

2

h2

(

)>(NxNy

)d dz

h2

h2

(+

+

)>(xznzyznz

)d dz = 0.

(14)

One more substitution of the kinematic equation (9) into(14) gives:

h2

h2

xy

y +

x

>

Db

uxvyuy +

vx

d dz+ h

2

h2

(z +

x

z +

y

)>Ds

(xzyz

)d dz =

h

2

h2

>fxfyfz

d dz+ h

2

h2

(

)>(NxNy

)d dz+

h2

h2

(+

+

)>(xznzyznz

)d dz.

(15)

Note that replacing(

)by(u v w

)leads to a

quadratic internal energy term on the left-hand side and anexternal energy term at the right-hand side. This equalitystates that the external energy spent on the deformation isfully transferred to the material.

5.3. Change of Variables: from local in-plane dis-placements to angles of rotation of the patchnormal

Substituting the second kinematic equation (10) into (15)involves derivatives with respect to z. For thin plates,

4

computing such derivative can be very unstable. To over-come this, we propose a change of variable that willavoid computing these derivatives. The local displacements(u v w

)>can be expressed with respect to the rotation

of the patch normal. When the transverse shear is consid-ered, the classic Kirchoff laws [4] can be extended to thefollowing formulas:

u = z x(x, y),v = z y(x, y),

w = w(x, y),

(16)

where x and y are local rotations about the tangent vectorsy and x. For shear deformable plate, the relation betweenthese angles and the normal displacement w is:

x =w

x xz,

y =w

y yz.

(17)

Equations (16) and (17) illustrate the fact that a change oforientation of the patch normal is caused by both bendingand transverse shear. In the case of only in-plane deforma-tion (e.g. planar stretching), only the transverse shear maybe responsible of the change in normal orientation. Thetest function being any function, the changes of variable on(u v w

)>can be similarly applied to the test functions

so that we obtain similar terms on the left and right handsides of Db and Ds. Let us denote

(

)>the new

test functions obtained from the former test functions withsimilar changes of variable (16) and (17). Using these twochanges of variables into (15) yields:

h2

h2

zx

z yz(y +

x )

>

Db

zxx

z yyz(xy +

yx )

d dz+ h

2

h2

(x y

)>Ds

(wx xwy y

)d dz =

h

2

h2

zz

>fxfyfz

d dz+ h

2

h2

(zz

)>(NxNy

)d dz+

h2

h2

(z+ z +

)>(xznzyznz

)d dz.

(18)

Equation (18) constrains the solution(x y w

)>to

be continuously differentiable. This condition is weaker interm of regularity than the original equation (6) that imposes

(u v w

)>to be twice continuously differentiable. This

weaker regularity has also the advantage to let the surfacefold sharply if required.

6. Iso-Parametric FEMWe approximate the whole surface with a mesh of tri-

angle patches j , 1 j e, where e is the number of patchelements. In order to use the FEM approach, we parameter-ize surface points and the corresponding displacements withshape functions [6]. We use iso-parametric shape functionsto interpolate the surface points, the displacements and thetest functions. If we consider a triangle patch, then the in-terpolation scheme is written as:

Q(1, 2) =

ni=1

Si(1, 2)Qi, 1 i n, (19)

where (1, 2) R2 is a global parameterization. Q is amute variable that can be replaced by the surface point X ,the displacement w, x, y and the test functions , , .{Si(1, 2)}1in, are real valued differentiable functionscalled shape functions. The support of Si is the union ofpatches that contains node i. The shape functions must sumto one for all 1, 2. i =

(ix

iy w

i)>

is the displace-

ment of node i. i =(i i i

)>are the values of the

test functions at node i.First we focus on the left-hand side of equation (18) that

we denote El. The right-hand side is denoted Er and will beaddressed right after. We replace the displacement and testfunction parameterization of equation (19) into El to obtaina global equation that uses the global bending stiffness Kband the global transverse shear stiffness Ks matrices:

El = T>(Kb + Ks

) = T>K, (20)

where =(1 n

)>is the global displacement

3n-vector and T is the global nodal test function 3n-vector.K is the global stiffness matrix. Kb and Ks are the globalbending and transverse shear stiffness matrices (the tildesymbol represents matrices related to the new variable ).They are assembled from bending and transverse shear stiff-ness matrices of each element patch:

kb =

( h2

h2

z2 B>b Db Bb d dz

)

ks =

( h2

h2

B>s Db Bs d dz

),

(21)

with the formula:

Kb(I, J) =

ek=1

(I,J)k

kb(iI , jJ),

Ks(I, J) =

ek=1

(I,J)k

ks(iI , jJ),

(22)

5

where 1 < I, J < 3n is the global indexing of node dis-placements and 1 iI , jJ 3 3 is the correspondinglocal element indexing. The expressions of Bb, Bs are eas-ily obtained from the Jacobian matrices of shape functionswhen applied to and test functions [6]. Applying the samereasoning to the right-hand side of equation (18), we can de-duce a similar formula involving the external nodal force f :

Er = T> f . (23)

Thus, the approximation of equation (18) with FEM is:

T>K = T> f , for all T R3n (24)

For this equation to hold for any T, we have obviously:

K = f (25)

In order to recover the initial global displacement vectorX, we apply the inverse variable change, which gives:

K H X = K X = f . (26)

where H is a 3n block diagonal matrix with blocks H =diag

(2/h, 2/h, 1

). Recall h is the material thick-

ness and z = h/2 corresponds to the top surface of thematerial. Now we have seen the construction of matrix Kand previously the construction of matrices P and S. Wecan thus study the feasibility and uniqueness of solution forour SfT formulation (1).

7. Feasibility and Solution UniquenessBy construction K is not always full rank especially if

the elements are not regular. However, with sufficientm, Kbecomes full rank after adding the m SBCs as follows:

K(3i, 3j) = 1, if i = jK(3i, 3j) = 0, otherwise,

(27)

with i running only for SBC nodes and 1 j n. Practi-cally, we can add sufficient SBCs to make K full rank. Toexhibit the feasibility and uniqueness of problem (1), wecompute its Lagrangian:

L(X, , ) = 12X>K>K X +> (PX b)+>SX,

(28)where is a 2n-vector and is anm-vector. The optimalityconditions are written as:

LX

= K>K X + C(> >

)>= 0, (29)

L(, )

= C X =(b> 0

)>, (30)

with C =(P> S>

)>a matrix of rank 2n + m by con-

struction. The set of feasible solutions X is written as

X = X + d, (31)

where X is any vector that satisfies (30) and d Ker{C}(the null space of C). Substituting in (28) we find:

K>K d = K>K XC(

)(32)

This equation has a unique solution if and only if the restric-tion of K>K to Ker{C} is invertible. This is the case sinceK is full rank by construction and by equation (27).

8. Experimental Results8.1. Compared Methods

To have a representative evaluation with related state-of-the-art methods, we compare our method LM (linearmechanics-based) to four other methods that have been pre-sented previously in section 2 and table 1: (1) NLM [10],a non-linear iterative method that minimizes stretching en-ergy. (2) KFM [1], a sequential method that uses mechan-ical priors embedded in a Kalman Filtering process. (3)NLG [9], a non-linear iterative method that minimizes alocal isotropy penalty. (4) AG [3], an analytic geometricmethod that uses local isotropy as prior.

These methods were evaluated using MATLAB R2014Aon a MAC desktop (OS X 10.9.5) with QUAD-CORE IN-TEL XEON running at 22.66 GHz. Our evaluation is basedon three criteria: (i) accuracy, (ii) computation time and(iii) robustness to image noise for the synthetic experiments.The amount of extensibility is expressed as a percentageof the relative variation of the stretching energy with respectto the ground-truth template [10].

8.2. Simulated DataThe synthetic deformations are obtained using 3D Stu-

dio Max [11]. This provides plausible deformations accord-ing to the mechanical properties of the considered material.We simulate a material with Poissons ratio = 0.49 andYoungs modulus E = 106 Pa (Pa stands for Pascals tomeasure force per unit area). Such a material deforms likea toy balloon for 15%. We use a planar template ofsize 150 150 mm2. We subdivide it in a regular gridof N = 30 30 nodes and 1682 triangular faces. Thelargest length of each triangle being 5

2 mm, we choose

a thickness h = 0.8 mm such that it fits the local plate as-sumption (c.f . section 4). The points at the boundary of thematerial are taken as being part of the SBC. The deformingforces are applied at the nodes of the grid. Their magni-tude follows a gaussian distribution of standard deviationof 20 Newton and their orientations vary from node to nodewith a uniform distribution. To obtain the deformed images,the nodes on the simulated deformed surfaces are projectedwith a calibrated perspective camera located 800 mm fromthe surface. We run two sets of test; (i) Robustness to noise:centred Gaussian noise N with varying standard deviation = 1 : 1 : 5 pixels was added to the image points. Forthis set the amount of deformation was set to = 15%. (ii)Robustness to amount of deformation: deformations in therange = {2%, 5%, 7%, 10%, 12%, 15%} are tested

6

1 2 3 4 5

5

10

15

20

STD Gaussian Noise [pixel]

Me

an

3D

err

or

[mm

]

NLM

KFM

NLG

AG

LM

1 2 3 4 50

1

2

3

4

STD Gaussian Noise [pixel]S

TD

3D

err

or

[mm

]

NLMKFMNLGAGLM

(a) Robustness to noise

0 5 10 15

2

4

6

8

10

12

14

16

Extensibility [%]

Mean

3D

err

or

[mm

]

NLM

KFM

NLG

AG

LM

0 5 10 150

0.5

1

1.5

2

2.5

3

3.5

4

Extensibility [%]

ST

D 3

D e

rro

r [m

m]

NLM

KFM

NLG

AG

LM

(b) Robustness to extensibility

0 0.5 1 1.5 2 2.5 3 3.5 4 4.5 5

[mm]

(c) 3D Reconstructions with error display ( = 15%, = 1). From left to right: AG, NLG, KFM, NLM, LM and ground-truth.

Figure 3. Results on simulated deformations. Large error results are not displayed to fit the error scale of the most accurate methods.

with image noise N1. We measure the reconstruction ac-curacy as being the 3D residual error in mm between theground-truth and the reconstructed 3D points. For each ex-tensibility ratio and noise N , we compute the mean andthe standard deviation (std) of the 3D residual error over100 samples.

The results are shown in figure 3: figures 3-a and 3-bshow the error curves while 3-c shows some example ofreconstructions. Globally, the error increases when noiseor extensibility increase. Also we can notice that methodswith mechanical priors outperform methods with geometricpriors. Some error values of the latter methods are not dis-played in cases where there is at least an order of magnitudedifference when compared to the former methods. NLMand KFM have similar orders of magnitude errors whencompared to our proposed method LM. However, LM ismore accurate and more stable than the two other mechani-cal based methods. NLM requires an initial deformed roughshape and an optimal hyper-parameter setting to provide thebest possible result. KFM is particularly sensitive to noisesince it is sequentially integrated from deformation to de-formation in the Kalman filter. Moreover, it is worth not-ing that for such methods, any mismatch defeats the wholeprocedure that needs to be re-initialized. LM is concep-tually free from these drawbacks; no hyper-parameter, noinitialization and frame independence since it requires anindependent single view at each time. These specificitiesmake the LM method more appropriate for substantial noiseor extensibility. Regarding the computation time, table 2reports the execution time that we obtained on our plat-form. The analytic method is with no doubt the fastest. Thenon-linear iterative methods are the slowest. The proposedmethod is in the same order of speed as KFM. The speed of

Method NLM KFM NLG AG LM

Time [sec] 10.6 1.4 10.4 0.5 1.1Table 2. Execution time for the compared methods. The men-tioned values do not take into account the matching process.

execution of the LM method can be significantly improvedif we would take into account the block-wise structure ofK.

8.3. Real DataFor validation with real data, we used four sets of data

with ground-truth that was obtained with stereo calibratedcameras [10]. The two cameras have a resolution of 640 480 pixels. A set of 10 deformed shapes was used foreach dataset. (1) A stretchable redchecker pattern clothesmade of polyester ( = 0.3, E = 105 Pa) with thicknessh = 2 mm and square size 400 400 mm2. (2) A dottedblack/white pattern spandex ( = 0.5, E = 104 Pa) withthickness h = 1.5 mm and square size 400 400 mm2. (3)A balloon pattern fabric made of rubber ( = 0.5, E = 103Pa) with h = 0.7 mm and bounding box 150 150 100mm3. (4) a cap made of quasi-inextensible polyester mate-rial ( = 0.001, E = 107 Pa) with h = 2 mm and boundingbox 220 220 150 mm3. The redchecker and spandexmaterials are clipped on the edge of a box to fixed boundaryfor the SBC. The balloon is clipped to a cup-ring in order tofix its boundaries. The cap was deformed only in the top ofthe cap so that its surroundings are kept rigid. The boundarypoints were estimated by a PnP method [14]1. Features are

1 http://cvlab.epfl.ch/software/EPnP/index.php

7

http://cvlab.epfl.ch/software/EPnP/index.php

(a) Redchecker dataset

(a.1) KFM

(a.2) NLM

(a.3) AG

(a.4) NLG

(a.5) Grd truth

(a.6) LM (b) Spandex dataset

(b.1) KFM

(b.2) NLM

(b.3) AG

(b.4) NLG

(b.5) Grd truth

(b.6) LM

(a.1) Balloon

(a.2) KFM

(a.3) NLM

(a.4) Grd truth

(a.5) LM (b.1) Cap

(b.2) KFM

(b.3) NLM

(b.4) Grd truth

(b.5) LM

0 0.5 1 1.5 2 2.5 3 3.5 4 4.5 5

[mm]

Figure 4. 3D reconstructions of real datasets. The ground-truth of the cap data is shown in red for better display.

obtained semi-automatically with SIFT [8]. For the red-checker pattern, its corner points were used for manual-driven point selection. A total of 100 feature points and 36fixed boundary points were used for this dataset. For thespandex, features are found by manual selection with ini-tial matches from SIFT. A total of 212 feature points and45 fixed boundary points were used for this dataset. Forthe balloon a total of 95 feature points and 30 fixed bound-ary points were used for this dataset. A set of 40 boundarypoints and a 130 point correspondences were used for thecap. These feature points are used as nodes of the mesh.The extensibility ranges from 0% to 15% for the wholedataset except for the cap for which it was negligible. Themean 3D error was measured at about 1 mm for LM, 1.3mm for NLM method, 1.7 mm for KFM, 5.3 mm for NLGand 6.9 mm for AG. Table 3 gives more details about themean and std of 3D errors.

9. ConclusionWe formulated SfT as finding the deformation field

through linear least-squares using mechanical priors. Toobtain this result we minimized the norm of the deform-ing forces subject to reprojection boundary conditions andsome solid boundary points. We showed experimentallythat this method is more accurate than state-of-the-art meth-

Method NLG AG NLM KFM LM

redchecker 4.5/3.5 5.7/3.6 1.2/1.0 1.3/1.2 0.9/0.8spandex 5.0/3.6 6.2/4.1 1.4/1.1 1.4/1.3 1.1/0.9balloon 7.5/5.9 8.7/5.5 1.8/1.5 2.0/1.5 1.2/1.0

cap 3.0/2.5 3.7/2.9 1.4/1.0 1.3/1.2 0.9/0.6Table 3. Average and standard deviation of 3D error (in mm) forthe real datasets.

ods, computationally efficient and has the fundamental ad-vantage of being convex. It opens perspectives for real timeSfT in critical applications in the medical field for instance.We think that image matching under elastic deformations isan interesting area of future research.

AcknowledgementsThis research has received funding from the EUs

FP7 through the ERC research grant 307483 FLEX-ABLE.

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