Abstract
Tape spring is straight, thin-walled, elastic strip with curved cross-section, which can replace traditional hinges by allowing for folding elastically and unfolded releasing stored energy with fewer component parts. This work is devoted to the properties of the folding and deployment of simple tape spring by numerical simulation and experiment method. Firstly, the folding process of tape spring is experimentally investigated using a specially designed test rig and verified by using nonlinear finite element ABAQUS/Standard solver. Then the moment-rotation relationships for symmetric bending are studied, the effects of subtended angle of section, total tape spring length, thickness and cross section radius on the performance of tape spring are investigated. Furthermore, the optimal model of tape spring structure design is established based on the response surface methodology (RSM) and parameter’s effective analysis, which aims at maximum strain energy during the tape-spring hinge deployment and subjects to allowable stress of tape spring. And the interior point algorithm is used to solve the optimal model. The optimal results are of great importance to the design of novel deployable structures with high stability, reliability and lightweight.
1 Introduction
Tape spring is a specialized structural form of the everyday carpenter’s tape with a curved cross section, which has the key property that it can be folded elastically and unfolded by releasing stored energy automatically, that is, contains no mechanical hinges or other folding devices. The tape spring has unique mechanical properties and it is both self-powered and self-latching without additional power and lock equipment.Thus the structure has several main attractions for space application which include lower cost, lightness and friction insensitiveness. Therefore, the tape spring evokes numerous interests in the deployable structures, such as synthetic aperture radars (SARS), solar arrays.
Recently, to comprehend the folding and deploying characters of tape spring, relevant researches have been accomplished by analytical, numerical, and experimental methods. In its free configuration, a tape spring can be assimilated to a straight rod with an open and thin-walled cross-section of constant transverse curvature. When an overall bending is applied, the tape spring behaves as a classical beam firstly, but there is suddenly the creation of a partial fold, indicating snap-through buckling [1]. To simulate these buckling phenomena, the first approach consists of using a non-linear elastic shell model in the framework of large displacements and large rotations [2]. This approach can provide accurate results but lead to heavy and hard computation [3]. Seffen [4, 5] considered the tape spring in its folded configuration as an assembly of two rigid bars and a non-linear spiral spring accounting for the bending stiffness of the fold. The migration of a fold along the tape spring was investigated by using numerical simulation. What’s more, Guinot [6] came up with an intermediate approach, which considered the tape spring as a rod with highly flexible cross-sections. This approach appears to be easier to face with the complex scenarios of buckling, involving the creation, duplication, and migration of folds along the tape. As the development of the finite element method, Wang, et al. [7], studied the control of single tape spring’s bending area by numerical simulation method, and put forward the measures for controlling the bending area. Xuan, et al. [8], focused his study on the control of buckling. The empirical formula for avoiding the yielding of the single tape spring was given and confirmed by finite element analysis. Wei, et al. [9], investigated the bending process of single tape spring, and analyzed the influence of thickness and longitudinal bend angle of the tape spring on steady moment and maximum strain energy. In 2007, Soykasap, et al. [10], studied the performance of four different tape spring hinges by test apparatus design independently, and got the moment-rotation profiles of the hinges. Later, Mallikarachchi, et al. [11, 12], studied the quasi-static folding and deploying of the composite tape spring hinges by numerical and experiment methods.
Above all, most of researches with tape spring are focus on the mechanical properties, but there are few studies in the optimal design of tape spring. Yang, et al. [13, 14], investigated the folding and deployment of single-layer tape spring hinges and double-layer tape spring hinges under pure bend loading. And the multi-objective optimal design of the double-layer tape-spring hinge is performed by using modified non-dominated sorting genetic algorithm. Wang, et al. [15], investigated the deployment dynamics of large synthetic aperture radar antennas with auxiliary spring and observed the deployment synchronism, steady driving torque as well as maximum strain energy; the auxiliary spring is optimized and well agreed with the experiment. The present work aims at showing the behavior of folding and deployment of simple tape spring and the method of optimal design of tape spring is given based on experiments and numerical simulation. The influences of length, section radius, thickness and subtended angle on the mechanical properties of tape spring are investigated. The optimal model with maximum strain energy subjected to maximum stress constraints is established based on RSM(response surface methodology) in order to increase the driving ability of tape spring. Finally, the interior point algorithm is applied to solve the optimal model.
This paper is organized as follows. Section 1 gives some reviews about the tape spring in recent years; Section 2 shows the geometrical model of tape spring and explains the meanings for the geometric parameters;Section 3 compares the results from simulation and experiment; in Section 4 the analysis of parameters effects on mechanical properties of tape spring is investigated for optimal design; Section 5 introduces the strategy of the optimal design of tape spring and gives optimal algorithm to solve the mathematical optimal problem, meanwhile the program flow of optimal algorithm is charted; in Section 6 some conclusions are drawn.
2 Problem descriptions
Tape spring is straight, thin-walled, elastic strip with curved cross-section. In the bending process, the geometric parameters directly influence the mechanical properties of tape spring. The simplest and most common form of a tape spring is a cylindrical shell, as shown in Figure 1. The tape spring has an initial design with uniform thickness t = 0.1 mm and total tape spring length
Considering tape spring is an open cylindrical structure with a natural transverse curvature, the bending of tape spring about short axis (perpendicular to the length of the tape spring) is direction dependent, if the direction of external torque is opposite to the transverse curvature, the tape spring forms a opposite sense folding; if the direction is same as the curvature, the tape spring produces an equal sense folding [1]. Therefore, the analysis and discussion of the tape spring are made according to the opposite sense bending and the equal sense bending.
3 The mechanical properties analysis of tape spring
3.1 Numerical simulations of tape spring
The geometric model of tape spring is set up and analyzed through finite element software ABAQUS/Standard. The finite element model of tape spring is shown in Figure 2. The material of tape spring is spring steel 65Mn with mass density 7.85 g/cm3, Young’s modulus 200GPa, Poisson’s ratio 0.3. The boundary condition is shown in Figure 3. In order to simulate the folding process of tape spring, two reference nodes, A and B, at either end are connected to the edges of the end cross sections through kinematic constraints. All the degrees of node A are restrained except the rotation about the global z-axis. Node B is only allowed to rotate about the z-axis and translate along the global y-axis. The specified opposite and equal angular displacements with value of 90° are applied on reference nodes defined in section centroid to achieve pure bending. The complicated behavior of tape spring under pure bending is analyzed by using an improved arc-length scheme which is introduced into the nonlinear finite element procedure. The numerical results are obtained in Table 1.
Rotation(°) | The equal sense bending process | The opposite sense bending process | ||
---|---|---|---|---|
Experiment | Simulation | Experiment | Simulation | |
1 | ||||
10 | ||||
20 | ||||
30 | ||||
40 | ||||
50 | ||||
60 | ||||
70 | ||||
80 | ||||
90 |
3.2 Experiments of tape spring
In order to verify the validation of the numerical models, the properties of tape spring during folding process are experimentally investigated with a specially designed test rig, shown in Figure 4.
The test rig is equipped with a driven shaft and a driving shaft that being fixed to a rigid base. The driven shaft is the one passive driven shaft, and the driving shaft is the other active driving shaft. All the freedoms of driving shaft are limited except the rotation around itself. The driven shaft is allowed to move along the horizontal direction, which is mounted on the guide rail. Two angle sensors are connected to the computer on driving and driven shafts, which are used to monitor the rotational speed and rotation angles. As the rotation angle rises, the driving shaft rotates slowly, which driven by the motor, and the driven shaft rotates and moves along the slide way. The behavior of simple tape spring during the folding process is obtained, which is shown in Table 1.
3.3 Comparison of experiments and simulations
The properties of tape spring with initial design during folding process are investigated by means of experiment and numerical simulation. The process of equal and opposite folding is studied and the results of experiment and numerical simulation are compared in Table 1. The deformation and stress contours show that the tape spring has a large displacements and large rotations under the moment at each end. Both of the equal and opposite folding indicates that the longitudinal curvature changes from 0 to 1/R and the transverse curvature varies from 1/R to 0. During the equal process, the tape spring showed a smooth folding as the raise of rotation angle, however, in the case of opposite folding, a sudden snap through buckling occurred when the rotation angle is increasing to the critical value. The experimental results agree well with the numerical results.
Figure 5 shows that the maximum stress varies with the bending angle of folding process. The maximum stress increases to 997.1MPa during opposite folding process when the rotation angle is around 20°, and then slightly slops down due to the snap through buckling. The equal folding also has high value of maximum stress, which is 892.9MPa. The results obtained in these two cases show that the property of tape spring is including the geometric nonlinearity and material nonlinearity. Therefore, the linear buckling analysis is already unsuitable for predicting the buckling behavior of tape springs. The improved arc-length scheme is adapted to solve the nonlinear problem.
The moment rotation profiles obtained by means of simulation and experiment are drawn in Figure 6. The experiments for tape spring include two main steps, the first step is to fold the tape spring to a fully folded configuration; the second step is deployment of tape spring, starting from the completely folded state. In the picture, the starts for both deployment simulation and experiment are corresponding to the rotation of
4 Parametric effects analysis
The driving capability of tape spring plays an important role in the deployable structures, and the steady moment and maximum strain energy are treated as two important indexes to measure mechanical properties [15], which associated with the value of thickness and subtended angle as well as cross section radius and length of tape spring. Now, we investigate the parametric effects on the properties of tape spring by numerical simulation.
4.1 Thickness effects
The effects of tape spring thickness on the steady moment and maximum strain energy are investigated; meanwhile the maximum strain energy is obtained in the fully folded configuration as shown in Figures 7 and 8. It can clearly be seen that the steady moment and maximum strain energy grow rapidly as thickness rises, which indicates that the driving capability of simple tape spring get enhanced remarkably. The variations of maximum strain energy and steady moment with thickness are shown in Figure 7 and Figure 8.
When the thickness of tape spring varies from 0.05 mm to 0.3 mm while keeping other parameters using initial design, as shown in Table 2 the steady moment has a high growth rate which is more than 67.3 % during equal folding process, while the opposite gives a value of 68.2 %, see Figure 7. The values of maximum strain energy stored for deployment of tape spring increase by more than 68.8 % and 68.1 %, corresponding to equal and opposite folding, see Figure 8.
t/mm | 0.05 | 0.10 | 0.15 | 0.20 | 0.25 | 0.30 | |
---|---|---|---|---|---|---|---|
Steady moment/N.m | Equal sense | 0.004 | 0.028 | 0.084 | 0.188 | 0.349 | 0.583 |
Opposite sense | 0.007 | 0.048 | 0.151 | 0.335 | 0.639 | 1.075 | |
Strain energy/J | Equal sense | 0.015 | 0.088 | 0.266 | 0.598 | 1.130 | 1.908 |
Opposite sense | 0.024 | 0.159 | 0.494 | 1.099 | 2.098 | 3.527 |
4.2 Subtended angle effects
The variations of maximum strain energy and steady moment with the subtended angle of tape spring are obtained, see Figures 9 and 10. When the subtended angle varies from 25°to 120°with other parameters using initial design, as listed in Table 3 it is obvious that the driving capability of simple tape spring has an vast improvement as the growing of subtended angle. The steady moment has a growth percentage of 40.5 % for equal folding and the value of opposite folding is 44.1 %. For the maximum strain energy in equal and opposite bending of the tape spring, it will be a significant improvement in growth rate 48.4 % and 53.7 % as the rising of subtended angle respectively.
55 | 65 | 75 | 85 | 95 | 105 | 115 | 125 | ||
---|---|---|---|---|---|---|---|---|---|
Steady moment/N.m | Equal sense | 0.013 | 0.017 | 0.021 | 0.027 | 0.032 | 0.039 | 0.045 | 0.050 |
Opposite sense | 0.024 | 0.031 | 0.038 | 0.047 | 0.055 | 0.065 | 0.073 | 0.079 | |
Strain energy/J | Equal sense | 0.043 | 0.053 | 0.066 | 0.082 | 0.103 | 0.127 | 0.156 | 0.185 |
Opposite sense | 0.078 | 0.097 | 0.122 | 0.151 | 0.185 | 0.225 | 0.269 | 0.308 |
4.3 Length effects
For the end of tape spring is held by two rigid clamps, the actual working length is L1. Each of the rigid clamps has initial length of 25 mm, the initial design of parameters is adopted apart from L1 changing from 80 mm to 180 mm.The variation tendencies of steady moment and maximum strain energy with the length of tape spring are investigated, shown in Figures 11 and 12. Whether equal or opposite bending of the tape spring, a similar variation tendency will be obtained for the steady moment and strain energy. The two indices drop down when L1 varies from 80 mm to 160 mm with 10 mm increments, and an approximately stable state has been achieved when L1 arrived at 160 mm. It should be noted that the improvement of length is not beneficial for the driving capability of tape spring, which also can be found in Table 4.
L/mm | 80 | 90 | 100 | 110 | 120 | 130 | 140 | 150 | |
---|---|---|---|---|---|---|---|---|---|
Steady moment/N.m | Equal sense | 0.031 | 0.028 | 0.026 | 0.024 | 0.023 | 0.022 | 0.021 | 0.021 |
Opposite sense | 0.052 | 0.048 | 0.046 | 0.043 | 0.042 | 0.040 | 0.040 | 0.039 | |
Strain energy/J | Equal sense | 0.094 | 0.089 | 0.085 | 0.083 | 0.082 | 0.080 | 0.080 | 0.079 |
Opposite sense | 0.169 | 0.161 | 0.155 | 0.151 | 0.148 | 0.145 | 0.146 | 0.143 |
4.4 Cross section radius effects
The variation tendencies of driving capability with respect to cross section radius are studied and the other parameters use initial design. When the radius varies from 8 mm to 22 mm with 2 mm increments, the energy and steady moment responses are listed in Table 5, it can be seen that both of the maximum strain energy and the steady moments have a slight falling, once the radius increases to more than 12 mm, they begin to rise. The relationships between cross section radius and steady moment are obtained in Figure 1 and the variation of maximum strain energy is given in Figure 14.
L/mm | 8 | 10 | 12 | 14 | 16 | 18 | 20 | 22 | |
---|---|---|---|---|---|---|---|---|---|
Steady moment/N.m | Equal sense | 0.072 | 0.071 | 0.070 | 0.072 | 0.077 | 0.087 | 0.098 | 0.111 |
Opposite sense | 0.129 | 0.128 | 0.129 | 0.134 | 0.144 | 0.157 | 0.172 | 0.189 | |
Strain energy/J | Equal sense | 0.264 | 0.261 | 0.260 | 0.262 | 0.268 | 0.282 | 0.302 | 0.329 |
Opposite sense | 0.475 | 0.473 | 0.474 | 0.481 | 0.496 | 0.524 | 0.558 | 0.602 |
As discussed above, the steady moment and maximum strain energy are treated as two crucial indices to measure mechanical properties of simple tape spring, and both of them have close relationships with thickness, subtended angle, length and cross section radius of tape spring. From Figure 8–Figure 14, it can be found that the thickness and subtended angle of tape spring have a huge influence on the driving capability; however the length and cross section radius weaken the driving capability in a certain degree. So it is necessary to find an optimal geometry for the best driving performance.
5 Optimal design of tape spring
5.1 Establishment of optimal model
During the folding process, the stress concentration occurs at the local deformation area, and the maximum stress has already exceeded the allowable stress, as investigated in previous part. All of the four key geometric parameters have effects on the driving capability to some different degrees. The optimal design will be studied to find an optimal geometry to get the best driving capability. Therefore, it aims at maximum strain energy during the tape spring hinge folding, and subjected allowable stress of tape spring. The optimal model is established as follows:
Where
5.2 Explicit objective function and constraint function
RSM is a collection of mathematical and statistical techniques, which used for obtaining the relationship between the input and output of complex system. In this paper, RSM is introduced to solve the problems of optimal design. The basic idea is to construct a polynomial with explicit expression to represent implicit function about design variables, so as to find out the optimal response value of the input variables.
The material of tape spring is spring steel 65Mn with mass density 7.85 g/cm3, Young’s modulus 200GPa, Poisson’s ratio 0.3. x1 is the thickness of the tape spring ranging from 0.05 mm to 0.25 mm, x2 represents the subtended angle of section varying from 70° to 90°, x3 is the cross section radius changing from 14 mm to 22 mm, x4 represents the total length of tape spring ranging from 120 mm to 200 mm.
According to the design area, the central principle of expansion is used to obtain the initial center point [x1,x2,x3,x4]T=[0.15,90,18,140]T and fitting radius δ0=[0.05,10,2,10]T. Center symmetric method is adopted to design test sample points. In the range of ±μδ0(where μ = 1,2), the center symmetric design points are selected to obtain 17 test sample points, initial center point included. And then, the responses of the maximum strain energy and stress are obtained by means of simulation with finite element software ABAQUS. The results of 17 design points are listed in Table 6.
Design point | x1 (mm) | x2 (°) | x3 (mm) | x4 (mm) | Maximum strain energy (J) | Maximum stress(MPa) | ||||
---|---|---|---|---|---|---|---|---|---|---|
FEA results | RS results | Relative error(%) | FEA results | RS results | Relative error(%) | |||||
1 | 0.05 | 90 | 18 | 140 | 0.01569 | 0.01577 | 0.50988 | 738.8 | 752.1 | 1.7951 |
2 | 0.15 | 70 | 18 | 140 | 0.21467 | 0.21499 | −0.14796 | 1244 | 1257 | 1.0612 |
3 | 0.15 | 90 | 14 | 140 | 0.26192 | 0.26172 | 0.07790 | 1553 | 1529 | −1.5249 |
4 | 0.15 | 90 | 18 | 120 | 0.31350 | 0.31324 | 0.08444 | 1790 | 1791 | 0.0349 |
5 | 0.1 | 90 | 18 | 140 | 0.09323 | 0.09296 | −0.2896 | 1162 | 1127 | −2.9957 |
6 | 0.15 | 80 | 18 | 140 | 0.24508 | 0.24448 | 0.24665 | 1346 | 1330 | −1.2040 |
7 | 0.15 | 90 | 16 | 140 | 0.26787 | 0.26848 | −0.22925 | 1416 | 1475 | −4.1896 |
8 | 0.15 | 90 | 18 | 130 | 0.29488 | 0.29535 | −0.16105 | 1615 | 1605 | −0.6006 |
9 | 0.15 | 90 | 18 | 140 | 0.28221 | 0.28198 | 0.08074 | 1487 | 1471 | −1.0944 |
10 | 0.20 | 90 | 18 | 140 | 0.63300 | 0.65285 | −3.13545 | 1781 | 1783 | 0.0938 |
11 | 0.15 | 100 | 18 | 140 | 0.32678 | 0.32751 | −0.22263 | 1623 | 1680 | 3.5117 |
12 | 0.15 | 90 | 20 | 140 | 0.30200 | 0.30221 | −0.06957 | 1527 | 1516 | −0.7515 |
13 | 0.15 | 90 | 18 | 150 | 0.27381 | 0.27312 | 0.25312 | 1411 | 1387 | −1.7080 |
14 | 0.25 | 90 | 18 | 140 | 1.19553 | 1.18555 | 0.83451 | 2068 | 2063 | −0.2407 |
15 | 0.15 | 110 | 18 | 140 | 0.38140 | 0.38105 | 0.09134 | 1981 | 1958 | −1.1812 |
16 | 0.15 | 90 | 22 | 140 | 0.32917 | 0.329167 | 0.0006 | 1598 | 1610 | 0.7334 |
17 | 0.15 | 90 | 18 | 160 | 0.26844 | 0.26876 | −0.11894 | 1346 | 1354 | 0.5813 |
The fitting of response surface function with maximum difference minimization method is introduced to construct corresponding response surface model, and the complex nonlinear relationships between the objective function and design variables are approximatively expressed [16]. The objective function can be written in terms of a series basic function as follows:
Where
Thus the quadratic response polynomial function expression of objective function obtained as follows:
Where U(x1,x2,x3,x4) presents the maximum strain energy.
Then quadratic response polynomial function of constraint function is obtained as follows:
Where σ(x1,x2,x3,x4) is the maximum stress that should be less than the allowable stress σs= 1000MPa.
5.3 Precision test of response surface fitting
In order to ensure the accuracy and applicability of the response surface model, the precision of response surface fitting for objective function and constraint function should be tested. If the fitting precision could not satisfy the required one, it is necessary to add the design points and adjust the initial center point. Then setting μ=0.5, testing the boundary points of the effective range firstly, and adding the boundary points of the initial range for special point test. The added 8 sample points are shown in Table 6, and the relative error between the FEA results and RS results for the 8 added sample points are listed in Table 6. According to the definition of response surface, fitting precision is given as follows:
Where ne is the sample size for testing, yi represents the real response value, ŷi is the response value obtained by observation model,
RMSE(root mean square error) represents the difference between response surface fitting value and test value. The smaller the RSME, the higher accuracy of response surface fitting. The relative errors of maximum strain energy and maximum stress between the FEA results and RS results are shown in Table 7. The fitting error of objective function is 0.6281 %, and the fitting error of constraint function is 0.8082 %, both of them are less than 1 %, which can meet the precision demand.
Design point | x1 (mm) | x2 (°) | x3 (mm) | x4 (mm) | Maximum strain energy(J) | Maximum stress(MPa) | ||||
---|---|---|---|---|---|---|---|---|---|---|
FEA results | RS results | Relative error(%) | FEA results | RS results | Relative error(%) | |||||
18 | 0.125 | 90 | 18 | 140 | 0.17064 | 0.1672 | −2.0574 | 1348 | 1292 | −4.3344 |
19 | 0.15 | 85 | 18 | 140 | 0.26556 | 0.2622 | −1.2815 | 1415 | 1382 | −2.3878 |
20 | 0.15 | 90 | 17 | 140 | 0.27325 | 0.2744 | 0.419 | 1425 | 1456 | 2.129 |
21 | 0.15 | 90 | 18 | 135 | 0.28792 | 0.2881 | 0.062 | 1551 | 1520 | −2.0395 |
22 | 0.175 | 90 | 18 | 140 | 0.43424 | 0.4472 | 2.898 | 1653 | 1619 | −2.1001 |
23 | 0.15 | 95 | 18 | 140 | 0.30788 | 0.3037 | −1.3764 | 1570 | 1554 | −1.0296 |
24 | 0.15 | 90 | 19 | 140 | 0.29139 | 0.2912 | −0.0652 | 1507 | 1475 | −2.1695 |
25 | 0.15 | 90 | 18 | 145 | 0.27756 | 0.2770 | −0.2022 | 1437 | 1411 | −1.8427 |
Note: The fitting error of objective function
5.4 Optimal results and discussion
In order to solve the optimal model conveniently, the general nonlinear programming model is introduced as follows:
Where
The optimal model is translated into a nonlinear programming and solved by the interior point method based on MATLAB software platform. The number of the variable is reduced and the model’s scale is minified. In this paper, the convergence criterion is chosen as follows:
Where xk is the design variable of the k iteration, rk represents obstacle factor, rk>0,r1>r2> … >rk> … >0,
If rk+1<rk (rk+1=rk/c, c≥2), k=k+1, it will be back to the previous step iteration cycle, and does not jump out of the loop until convergence criteria is satisfied. Otherwise, it will directly output the final optimal results.
After 33 iterations, the optimal solution is obtained and the iteration history of objective function is shown in Figure 15.
The comparisons between original and optimized results are carried out, as depicted in Table 8. The maximum stress after optimization is 999.1MPa, which is reduced by 32.81 % before optimization. The maximum strain energy after optimization is 0.25425J, which is reduced by 1.52 % before optimization. It is obvious that the best driving capability of simple tape spring is achieved and the optimal geometry size is obtained under the condition of meeting the allowable stress.
Design variables | Original optimized variation | |||
---|---|---|---|---|
L (mm) | 160 | 181.704 | 13.5% | |
t (mm) | 0.15 | 0.136784 | −8.81% | |
R (mm) | 18 | 22 | 22.22% | |
θ (°) | 90 | 85.4716 | −5.03% | |
Objective-Maximum strain energy(J) | 0.26844 | 0.25435 | −1.52% | |
Constraint-Maximum stress (MPa) | 1487 | 999.1 | −33.2% |
Figures 16 and 17 are the stress distributions of simple tape spring when fully folded before and after optimization obtained with ABAQUS. Figure 16 shows that the maximum stress mainly locates at the edge of the central part before optimization, the maximum stress after optimization is 993.2MPa, the maximum strain energy after optimization is 0.2550J, which are almost equal with the values obtained with RSM. Whereas the optimal design has a homogeneous stress distribution, shown in Figure 17. The stress concentration of fully folded tape spring is improved remarkably and the maximum stress of tape spring is controlled within the range of allowable stress. The optimal program flowchart of simple tape spring is shown in Figure 18.
6 Conclusions
This paper investigates the folding and deployment of simple tape spring by means of simulation and experiment. A model of a particular version of this tape spring has been constructed. The whole folding process has been captured through the finite element simulation. The mechanical properties of tape spring obtained by experiment have a good agreement with that of numerical simulations, which verifies the validation of the model of tape spring.
The parametric effect on the properties of tape spring is studied. It is concluded that the thickness and subtended angle of tape spring have vastly improved the driving capability while the length and cross section radius of tape spring may weaken it. The driving capability is regarded as optimal objective with the four geometric parameters as design variables and the maximum stress of tape spring is regarded as constraints. The RSM is introduced to establish optimal model, and the interior point algorithm is applied to solve optimal model. Finally, the optimal geometry size is obtained and the best driving capability is achieved.
These results provide theoretical basis for engineering application of the novel deployable structures.
Funding statement: The project supported by the National Natural Science Foundation of China(11072009), Beijing Education Committee Development Project(SQKM201610005001) and Beijing University of Technology Basic Research Fund(001000514313003).
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