TWI775411B - Soft actuator, gripping jaws, method, computer program product and computer readable recording medium for designing such - Google Patents
Soft actuator, gripping jaws, method, computer program product and computer readable recording medium for designing such Download PDFInfo
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本發明係關於一種夾持工具,尤指軟性夾爪及其設計方法、電腦程式產品、電腦可讀取紀錄媒體。 The present invention relates to a clamping tool, especially a soft clamping jaw and its design method, a computer program product, and a computer-readable recording medium.
軟性夾爪可適用外形差異較大之物件,且可降低夾持損傷物件機率,因此廣受使用。相關案件例如有本發明人曾獲准之中華民國發明專利公告第I630499號之「撓性夾爪及其設計方法、電腦程式產品、電腦可讀取紀錄媒體」。 Soft grippers are widely used because they can be applied to objects with different shapes and can reduce the probability of clamping damaged objects. Relevant cases include, for example, "Flexible Gripper and Its Design Method, Computer Program Product, and Computer-Readable Recording Media" of the Republic of China Invention Patent Publication No. I630499, which was approved by the present inventor.
在眾多不同類型的市售軟性夾爪中,以氣動軟性夾爪在產線的利用最為廣泛,主要原因為作動速度較高,可以大幅提高產線的產能。其構造主要是將多個軟性致動器以法蘭界面組成一個夾爪,而可透過對軟性致動器的氣囊充氣,以推動夾爪彎曲夾取目標物。 Among the many different types of soft grippers on the market, the pneumatic soft gripper is the most widely used in the production line, mainly due to the high actuation speed, which can greatly increase the production line capacity. The structure is mainly composed of a plurality of soft actuators with a flange interface to form a jaw, and the air bag of the soft actuator can be inflated to push the jaw to bend and clamp the target object.
惟,目前氣動夾爪的負載重量相比其他種類之軟性夾爪仍有很大的改善空間。 However, at present, the load weight of pneumatic grippers still has a lot of room for improvement compared with other types of soft grippers.
爰此,本發明人為增進軟性致動器的實用性,提出一種軟性致動器之設計方法,包含以一拓樸最佳化方法進行設計,所述拓樸最佳化方法的目標函式為交互位能(Mutual potential energy,MPE):,其 中:K為包含輸入端及輸出端連接彈簧常數之全域剛性矩陣:K=K s +;U1為僅輸入負載下之全域位移向量;U2為僅輸出負載下之全域位移向量,中的上標T為轉置矩陣之意,所述全域位移向量中的固定端位移設為0;K s 為虛擬彈簧之剛性矩陣;K e 為單一元素之剛性矩陣;Σ e 為所有元素矩陣加總之意;為經濾化後之元素密度,其下標i代表設計區間中第i個元素,其上標p為懲罰係數,x i 為濾化前之元素密度,為介於0到1之間的連續正實數。 Therefore, in order to improve the practicability of soft actuators, the present inventor proposes a design method for soft actuators, including designing with a topology optimization method, and the objective function of the topology optimization method is: Mutual potential energy (MPE): , where: K is the global stiffness matrix including the spring constants of the input and output connections: K = K s + ; U 1 is the global displacement vector under only the input load; U 2 is the global displacement vector under only the output load, The superscript T in is the meaning of the transposed matrix, and the fixed end displacement in the global displacement vector is set to 0; K s is the rigidity matrix of the virtual spring; Ke is the rigidity matrix of a single element ; Σ e is the matrix of all elements to sum up; is the element density after filtering, the subscript i represents the ith element in the design interval, the superscript p is the penalty coefficient, and x i is the element density before filtering, which is a continuous between 0 and 1 positive real number.
進一步,所述拓樸最佳化方法係以元素密度濾化演算法更新設計變數,所述元素密度濾化演算法之計算公式如下:
進一步,所述拓樸最佳化方法係以移動漸進線之變數更新方法(Method of Moving Asymptotes,MMA)進行變數更新。 Further, the topology optimization method is to update the variables with the method of moving asymptotes (Method of Moving Asymptotes, MMA).
上述軟性致動器之設計方法實施上可建構為一程式並儲存於電腦程式產品或電腦可讀取紀錄媒體。當電腦載入該程式並執行後,可完成如前述之軟性致動器之設計方法。 The design method of the above-mentioned soft actuator can be implemented as a program and stored in a computer program product or a computer-readable recording medium. After the computer loads the program and executes it, the design method of the soft actuator as described above can be completed.
本發明也是一種軟性致動器,係使用如前所述之軟性致動器之設計方法所製作,包含用於夾持物件之一夾持部,該夾持部上沿一長度方向間隔設置之複數氣囊部,且每相鄰的二個所述氣囊之間皆連接一關節部,以形成相對該夾持部之一彎曲面,該夾持部及每個所述氣囊部皆有相互連通之一充氣流道。 The present invention is also a soft actuator, which is manufactured by using the above-mentioned design method of the soft actuator, and includes a clamping portion for clamping an object, and the clamping portion is provided with spacers along a length direction. a plurality of airbag parts, and a joint part is connected between each adjacent two airbag parts to form a curved surface opposite to the clamping part, the clamping part and each airbag part are connected with each other an inflatable channel.
本發明並是一種軟性致動器,包含用於夾持物件之一夾持面、相對該夾持面之一彎曲面、及連接該夾持面與該彎曲面之二側面,該彎曲面沿一長度方向間隔設置有複數氣囊部,每相鄰的二個所述氣囊之間連接一關節部,所述關節部於中央處有一隆起部位,該隆起部位往兩側漸縮而概呈一梯形。 The present invention is also a soft actuator, comprising a clamping surface for clamping an object, a curved surface opposite to the clamping surface, and two side surfaces connecting the clamping surface and the curved surface, the curved surface along the A plurality of airbag parts are arranged at intervals in the longitudinal direction, and a joint part is connected between each two adjacent airbags. The joint part has a raised part at the center, and the raised part tapers to both sides to form a trapezoid. .
本發明亦是一種夾爪,包含複數個如前所述之軟性致動器安裝於一法蘭界面。 The present invention is also a clamping jaw comprising a plurality of the aforementioned soft actuators mounted on a flange interface.
藉由上述特徵,主要可達到如下所述的功效: With the above features, the following effects can be mainly achieved:
1.拓樸最佳化方法之目標函數採用交互位能,以避免拓樸最佳化結果產生不連續結構。 1. The objective function of the topology optimization method adopts the interactive potential energy to avoid the discontinuous structure in the topology optimization result.
2.拓樸最佳化方法採用元素密度濾化方法,以提升拓樸最佳化之收斂性。 2. The topology optimization method adopts the element density filtering method to improve the convergence of topology optimization.
3.拓樸最佳化方法的變數更新採用MMA方法,將原拓樸最佳化問題改寫為MMA之一般最佳化通式,以獲得更佳之目標函數。 3. The variable update of the topology optimization method adopts the MMA method, and rewrites the original topology optimization problem into the general optimization formula of MMA to obtain a better objective function.
4.藉上述拓樸最佳化設計之致動器,相較於市售致動器具有良好之彎曲性能,以此製作之夾爪,可有效提高負載重量。 4. The actuator designed with the above topology optimization has good bending performance compared with the commercially available actuator, and the gripper made by this can effectively increase the load weight.
(1):夾持部 (1): Clamping part
(2):氣囊部 (2): Airbag part
(3):關節部 (3): Joints
(31):隆起部位 (31): uplift part
(4):彎曲面 (4): Curved surface
(5):充氣流道 (5): Inflatable runner
(6):指尖結構 (6): Fingertip structure
(100):軟性致動器 (100): Soft Actuator
(200):法蘭界面 (200): Flange interface
(300):法蘭界面 (300): Flange interface
(400):法蘭界面 (400): Flange interface
(S01):步驟一
(S01):
(S02):步驟二
(S02):
(S03):步驟三
(S03):
(S04):步驟四
(S04):
(S05):步驟五
(S05):
圖1係本發明實施例拓樸最佳化流程圖。 FIG. 1 is a flow chart of topology optimization according to an embodiment of the present invention.
圖2係本發明實施例之設計區間示意圖。 FIG. 2 is a schematic diagram of a design interval according to an embodiment of the present invention.
圖3係本發明實施例濾化半徑示意圖。 FIG. 3 is a schematic diagram of a filtering radius according to an embodiment of the present invention.
圖4A係本發明實施例撓性機構設計區間示意圖。 4A is a schematic diagram of a design interval of a flexible mechanism according to an embodiment of the present invention.
圖4B係本發明實施例疊加原理示意圖。 FIG. 4B is a schematic diagram of a superposition principle according to an embodiment of the present invention.
圖5係本發明實施例軟性致動器之平面示意圖。 FIG. 5 is a schematic plan view of a soft actuator according to an embodiment of the present invention.
圖6A係本發明實施例中單輸出端邊界條件之示意圖。 FIG. 6A is a schematic diagram of the boundary condition of a single output terminal in an embodiment of the present invention.
圖6B係本發明實施例中雙輸出端邊界條件之示意圖。 FIG. 6B is a schematic diagram of the boundary conditions of dual output terminals in an embodiment of the present invention.
圖7係本發明實施例體積率對單位長度之末端節點平均位移量影響圖。 FIG. 7 is a graph showing the influence of volume ratio on the average displacement of end nodes per unit length according to an embodiment of the present invention.
圖8係本發明實施例氣囊設計參數示意圖。 FIG. 8 is a schematic diagram of design parameters of an airbag according to an embodiment of the present invention.
圖9係本發明實施例氣囊尺寸對末端節點平均位移量影響圖。 FIG. 9 is a graph showing the influence of the size of the airbag on the average displacement of the end node according to the embodiment of the present invention.
圖10係本發明實施例氣囊間距對單位長度之末端節點平均位移量影響圖。 FIG. 10 is a graph showing the influence of the airbag spacing on the average displacement of the end nodes per unit length according to an embodiment of the present invention.
圖11係本發明實施例氣囊厚度對單位長度之末端節點平均位移量影響圖。 11 is a graph showing the influence of the thickness of the airbag on the average displacement of the end node per unit length according to an embodiment of the present invention.
圖12係本發明實施例之軟性致動器之立體外觀示意圖。 FIG. 12 is a schematic three-dimensional appearance diagram of a soft actuator according to an embodiment of the present invention.
圖13係本發明實施例之軟性致動器之側視剖視示意圖。 FIG. 13 is a schematic side sectional view of the soft actuator according to the embodiment of the present invention.
圖14係本發明實施例之軟性致動器之局部立體剖視示意圖。 FIG. 14 is a partial three-dimensional cross-sectional schematic diagram of the soft actuator according to the embodiment of the present invention.
圖15係本發明實施例之軟性致動器之前視剖視示意圖。 FIG. 15 is a schematic cross-sectional front view of a soft actuator according to an embodiment of the present invention.
圖16係本發明實施例與市售夾爪軌跡比較圖。 FIG. 16 is a comparison diagram of the track of the gripper jaws of the embodiment of the present invention and the commercially available gripper.
圖17係本發明實施例與市售致動器彎曲曲率比較圖。 FIG. 17 is a comparison diagram of the bending curvature of an embodiment of the present invention and a commercially available actuator.
圖18係本發明實施例與市售致動器彎曲角度比較圖。 FIG. 18 is a comparison diagram of the bending angle between the embodiment of the present invention and a commercially available actuator.
圖19係本發明實施例二指式夾爪之立體外觀示意圖。 19 is a schematic three-dimensional appearance diagram of a two-finger gripper according to an embodiment of the present invention.
圖20係本發明實施例輸入壓力對二指式夾爪之最大負載關係圖。 FIG. 20 is a graph showing the relationship between the input pressure and the maximum load of the two-finger gripper according to the embodiment of the present invention.
圖21係本發明實施例三指式夾爪之立體外觀示意圖。 FIG. 21 is a schematic three-dimensional appearance diagram of a three-finger gripper according to an embodiment of the present invention.
圖22係本發明實施例輸入壓力對三指式夾爪之最大負載關係圖 Fig. 22 is a graph showing the relationship between the input pressure and the maximum load of the three-finger gripper according to the embodiment of the present invention
圖23係本發明實施例四指式夾爪之立體外觀示意圖。 FIG. 23 is a schematic three-dimensional appearance diagram of a four-finger gripper according to an embodiment of the present invention.
綜合上述技術特徵,本發明軟性夾爪及其設計方法、電腦程式產品、電腦可讀取紀錄媒體的主要功效將可於下述實施例搭配圖式清楚呈現。應注意的是,為便於理解,各圖式中,相近功能元件將採用相近或相同的元件符號。 In view of the above technical features, the main functions of the soft gripper and the design method thereof, the computer program product, and the computer-readable recording medium of the present invention can be clearly presented in the following embodiments with drawings. It should be noted that, for ease of understanding, in each figure, similar or identical reference numerals will be used for similar functional elements.
本發明實施例的軟性致動器之設計方法,實施上可建構為一程式並儲存於電腦程式產品或電腦可讀取紀錄媒體。當電腦載入該程式並執行後,可完成如前述之軟性致動器之設計方法。 The design method of the soft actuator according to the embodiment of the present invention can be implemented as a program and stored in a computer program product or a computer-readable recording medium. After the computer loads the program and executes it, the design method of the soft actuator as described above can be completed.
所述軟性致動器之設計方法包含以一拓樸最佳化方法進行設計,所述拓樸最佳化主要是以SIMP方法(Solid Isotropic Material with Penalization)為基礎,此方法具有較佳的運算速度且無網格相依性,適合用於撓性機構設計。為了避免輸入端與輸出端出現結構不連接狀況,本實施例將目標函數採用交互位能(Mutual potential energy,MPE)最大化,而設計區間拆解成僅有輸入力量及僅有輸出力量之負載條件,再依據疊加原理計算目標函數,設計變數更新則採用MMA方法〔移動漸進線之變數更新方法(Method of Moving Asymptotes,MMA)〕。 The design method of the soft actuator includes designing with a topology optimization method, and the topology optimization is mainly based on the SIMP method (Solid Isotropic Material with Penalization), which has better computing Speed and mesh-free dependence, suitable for flexible mechanism design. In order to avoid the structural disconnection between the input end and the output end, in this embodiment, the objective function is maximized by mutual potential energy (MPE), and the design interval is decomposed into loads with only input power and only output power Then, the objective function is calculated according to the superposition principle, and the MMA method is used to update the design variables [Method of Moving Asymptotes (MMA)].
以下將依序介紹三維拓樸最佳化之流程與理論,分別為設計區間、設計變數、有限元素分析、濾化演算法、MMA理論、收斂準則、目標函數及元素靈敏度。 The following will introduce the process and theory of 3D topology optimization in sequence, including design interval, design variables, finite element analysis, filtering algorithm, MMA theory, convergence criterion, objective function and element sensitivity.
請先參閱圖1,揭示本實施例所述拓樸最佳化方法的流程,係以SIMP方法為基礎,將設計區間中空洞元素之楊氏係數帶入一個趨近於0之正數,以避免計算有限元素時產生奇異之剛性矩陣,所述拓樸最佳化方法包含: Please refer to FIG. 1 first, which discloses the flow of the topology optimization method in this embodiment, which is based on the SIMP method. A singular rigid matrix is generated when computing finite elements, and the topology optimization method includes:
步驟一(S01):定義設計區間、邊界條件、設計參數及初始值。 Step 1 (S01): Define the design interval, boundary conditions, design parameters and initial values.
步驟二(S02):利用濾化演算法來更新設計變數,以更新後設計變數及邊界條件建立有限元素模型,再進行有限元素分析。 Step 2 ( S02 ): using the filtering algorithm to update the design variables, establishing a finite element model with the updated design variables and boundary conditions, and then performing finite element analysis.
步驟三(S03):以有限元素法得到之位移計算目標函數及元素靈敏度。 Step 3 (S03): Calculate the objective function and the element sensitivity with the displacement obtained by the finite element method.
步驟四(S04):以MMA方法更新設計變數。 Step 4 (S04): Update the design variables by the MMA method.
步驟五(S05):判斷是否收斂,若未達到收斂條件則回到步驟二(S02)繼續執行,若滿足收斂條件則結束拓樸最佳化。 Step 5 (S05): determine whether to converge, if the convergence condition is not met, go back to step 2 (S02) to continue execution, and if the convergence condition is met, end topology optimization.
以下將進一步詳細說明設計區間、邊界條件與有限元素分析: The design interval, boundary conditions, and finite element analysis are described in further detail below:
本實施例採用三維之拓樸最佳化方法來設計其外形結構。以長方體之設計區間為例,將設計區間離散為多個立方體元素,每個元素之長寬高皆一致,如圖2所示,設計區間中X方向之元素量為nelx,Y方向的元素量為nely,而Z方向之元素量為nelz。每一個立方體元素都有其獨立的元素密度(x i ),元素密度即為最佳化之設計變數,其下標i代表設計區間中第i個元素。元素密度代表該元素是否存在,所有元素密度都為介於0到1之間的連續正實數。當元素密度為1代表該元素為實心元素,需要被保留;當元素密度為0代表該元素為空洞元素,需要被挖除。在改良式SIMP方法中,假設每一個元素的設計變數與楊氏係數(E i )成線性關係,而楊式係數大小與剛性矩陣(k i )的值成線性關係,其關係式如下:
式(2-2):k i =E i k 0 Formula (2-2): k i = E i k 0
其中,E 0為材料之楊氏係數;E min 為一個趨近於0的正數;為經濾化後之元素密度;p為懲罰係數;k為元素剛性矩陣;k 0為楊氏係數代入1之元素剛性矩陣。懲罰係數可以使設計變數更趨近於極值,可將其數值定義為3,透過此方法可以大幅減少程式運算達到收斂的時間。當時,拓樸結果為黑色,代表該元素之楊氏係數為E 0。當時,拓樸結果為白色,代表 該元素之楊氏係數為0,在實際數值上則代入極小值E min ,以避免拓樸運算時產生奇異之剛性矩陣而使結果無法收斂。當介於0到1之間時,因其拓樸結果呈現灰色而稱之為灰階元素,此元素可提升收斂之穩定性但不具有實際上之物理意義,故使用上常以懲罰係數或投射方法使拓樸之元素密度趨向二值化。 Among them, E 0 is the Young's coefficient of the material; E min is a positive number approaching 0; is the element density after filtering; p is the penalty coefficient; k is the element rigidity matrix; k 0 is the element rigidity matrix with the Young's coefficient substituted into 1. Penalty coefficient can make the design variable more close to the extreme value, and its value can be defined as 3. Through this method, the time for the program operation to reach convergence can be greatly reduced. when When , the topological result is black, representing that the Young's coefficient of the element is E 0 . when When , the topology result is white, which means that the Young's coefficient of the element is 0, and the minimum value E min is substituted in the actual value to avoid generating a singular rigid matrix during the topology operation and the result cannot be converged. when When it is between 0 and 1, it is called a gray-scale element because its topology result is gray. This element can improve the stability of convergence but has no actual physical meaning, so it is often used with penalty coefficient or projection. The method makes the element density of topology tend to be binarized.
本實施例是採用靜態之有限元素分析,在設定之設計區間內給予邊界條件(含固定端、輸入力量及輸出力量),依照虎克定律求取各元素節點之位移,再依照位移結果計算目標函數(f)及元素靈敏度(α i ),其關係式如下:式(2-3):KU=F In this embodiment, static finite element analysis is used, and boundary conditions (including fixed end, input force and output force) are given in the set design interval, the displacement of each element node is obtained according to Hooke's law, and then the target is calculated according to the displacement result. Function ( f ) and element sensitivity ( α i ), the relationship is as follows: Formula (2-3): KU=F
其中,K為全域剛性矩陣,U為全域位移向量,F為全域力量向量。 Among them, K is the global rigidity matrix, U is the global displacement vector, and F is the global force vector.
濾化演算法:本實施例採用的元素密度濾化演算法來解決棋盤狀網格及網格相依性的問題,所述元素密度濾化演算法之計算公式如下:
元素密度濾化演算法的概念如圖3,以中心元素上黑色圓形作為為圓心,在r min 為半徑的範圍內之元素皆視為周遭元素。根據每個周遭元素與中心元素的距離來計算其線性權重,在半徑範圍內之元素距離中心元素越近權重越大,反之則權重越小,而半徑範圍外權重為0,經過加權平均後求得濾化後之元素密度。 The concept of the element density filtering algorithm is shown in Figure 3. The black circle on the central element is used as the center, and the elements within the radius of r min are regarded as surrounding elements. Calculate its linear weight according to the distance between each surrounding element and the central element. The closer the element within the radius is to the central element, the greater the weight, and vice versa, the smaller the weight, while the weight outside the radius is 0. to obtain the elemental density after filtering.
移動漸進線之變數更新方法(Method of Moving Asymptotes,MMA),以下簡稱MMA方法:MMA方法屬於一種結構最佳化之非線型規劃(Non-linear programing)方法,能應用於處理多變數及多限制條件的通用最佳化方法,本實施例利用MMA方法來進行變數更新,有助於在面對大位移變形的問題時,可以得到更好的收斂結果。其最佳化問題通式如下:
其中,f 0 為原始目標函數;f 1 ,...,f m 為限制式且f 0 ,f 1 ...,f m 為連續可微分函數;a 0 、a i 、c i 及d i 為給定的常數,須滿足a 0 、a i 0、c i 0、d i 0且c i +d i >0,當a i >0時a i c i >a 0;x j 是設計變數;y i 及z是人工變數(Artificial variable);而與為設計變數x j 的上下界限。
Among them, f 0 is the original objective function; f 1 ,..., f m is a restriction formula and f 0 , f 1 ... ,f m is a continuous differentiable function; a 0 , a i , c i and d i is a given constant, must satisfy a 0 , a i 0.
MMA方法的求解流程如下: The solution flow of the MMA method is as follows:
步驟一:設定MMA參數,給定一個初始值x (0),並假設初始疊代次數iter=0。 Step 1: Set the MMA parameters, give an initial value x (0) , and assume the initial number of iterations iter=0.
步驟二:以疊代點x iter 計算f i (x iter )及梯度值▽f i (x iter ),並藉此將函數f i 作凸函數近似轉換,產生近似函數。 Step 2: Calculate f i ( x iter ) and gradient value ▽ f i ( x iter ) with the iterative point x iter , and then convert the function f i into a convex function approximation to generate an approximate function .
步驟三:以近似函數產生一個子問題Piter取代初始最佳化問題P,並以對偶法求解子問題。 Step 3: Approximate the function with A subproblem P iter is generated to replace the initial optimization problem P, and the subproblem is solved by the dual method.
步驟四:將子問題Piter的最佳解作為下一個疊代點x (iter+1),同時令iter=iter+1。其中,MMA初始最佳化問題的子問題如式:
其中,及分別為下移動限制及上移動限制。 in, and They are the lower movement limit and the upper movement limit, respectively.
其中,式(2-8)中之近似函數如下:
其中, in,
其中, in,
上式移動限制及計算方式如下:
其中,為下漸進線(Lower asymptotes),為上漸進線(Upper asymptotes)。 in, is the lower asymptotes, For the upper asymptotes (Upper asymptotes).
當iter=1及iter=2時,
當iter3時,
其中,為移動漸進線之調整參數,
為了以MMA方法進行軟性致動器拓樸最佳化求解,本實施例將最佳化問題轉為MMA之一般問題通式如前述式(2-8)。為了使MMA通式與原式等價,依表1設定將參數代入MMA通式。除此之外,本實施例將原MMA子問題中之部分參數進行修改,修改後參數如表2所示。 In order to solve the topology optimization of the soft actuator by the MMA method, in this embodiment, the optimization problem is transformed into the general problem of MMA, and the general formula is as the aforementioned formula (2-8). In order to make the general formula of MMA equivalent to the original formula, the parameters are substituted into the general formula of MMA according to the settings in Table 1. In addition, in this embodiment, some parameters in the original MMA sub-problem are modified, and the modified parameters are shown in Table 2.
收斂準則: Convergence criterion:
一般收斂準則為當次疊代的目標值與前一次疊代的目標值的差值是否小於設定之容忍誤差,目的是當拓樸之外形結構及目標函數值趨於平緩時,結束元素不斷疊代更新之過程。本實施例在目標函數值部分採用相同準則,其計算方法如下式(2-22)所示,將當次與前一次疊代目標函數差值除以前一次目標函數值,以獲得差值百分比,藉此提高收斂穩定性。 The general convergence criterion is whether the difference between the target value of the current iteration and the target value of the previous iteration is less than the set tolerance error. Generation update process. This embodiment adopts the same criterion in the objective function value part, and its calculation method is shown in the following formula (2-22), dividing the difference between the objective function of the current iteration and the previous iteration by the objective function value of the previous iteration to obtain the percentage of difference, This improves the convergence stability.
其中,cn及cn-1為當次目標函數與前次目標函數,err為目標函數容忍誤差,而本實施例將目標函數容忍誤差err設定為0.0001。 Wherein, cn and cn -1 are the current objective function and the previous objective function, err is the objective function tolerance error, and in this embodiment, the objective function tolerance error err is set to 0.0001.
體積率部分則採用當次疊代體積率與目標體積率差值,其計算方法如下式(2-23)所示,當體積率差值滿足體積率之容忍誤差voltol時,則結束疊代更新之過程。 For the volume rate part, the difference between the current iteration volume rate and the target volume rate is used. process.
其中,為當次疊代之元素密度,為目標體積率,voltol為體積率容忍誤差,本實施例將體積率容忍誤差設定為0.001。 in, is the element density of the current iteration, is the target volume rate, and voltol is the volume rate tolerance error. In this embodiment, the volume rate tolerance error is set to 0.001.
目標函數: Objective function:
撓性機構拓樸最佳化之初始設計區間如圖4A所示,左側為具輸入力量Fin之輸入端,其力量可分為Fin,x及Fin,y兩個方向分量,在輸入端及設計區間具有一連接彈簧kin,可分為kin,x及kin,y兩個方向分量。底下為固定端,右側為具輸出力量Fout之輸出端,其力量可分為Fout,x及Fout,y兩個方向分量,在輸出端及設計區間具有一連接彈簧kout,可分為kout,x及kout,y兩個方向分量。 The initial design interval for topology optimization of the flexible mechanism is shown in Figure 4A. The left side is the input end with the input force F in , and its force can be divided into two direction components, F in, x and F in, y . The end and the design interval have a connecting spring kin , which can be divided into two directional components kin,x and kin ,y . The bottom is the fixed end, and the right side is the output end with the output force F out . The force can be divided into two directions: F out, x and F out, y . There is a connecting spring k out at the output end and the design interval, which can be divided into two directions. are two direction components of k out, x and k out, y .
本實施例採用之目標函數為交互位能(Mutual potential energy,MPE),用於描述結構受到兩個外力作用下之撓性。撓性機構常被設計來傳遞力量或位移,透過施加力量於一端,而機構產生變形進而使另一端產生力量或位移。 為了進行拓樸之分析,將施加力量一端定義為輸入端,而產生力量或位移一端定義為輸出端,而輸入及輸出力量則套用至交互位能的兩個外力,並依據疊加原理(Principle of superposition)將原設計區間拆解為僅輸入力量及僅輸出力量之兩種邊界條件,如圖4B所示。 The objective function adopted in this embodiment is mutual potential energy (MPE), which is used to describe the flexibility of the structure under the action of two external forces. Flexible mechanisms are often designed to transmit force or displacement by applying force to one end, and the mechanism deforms to cause force or displacement at the other end. In order to carry out the topological analysis, the end that exerts the force is defined as the input end, and the end that generates the force or displacement is defined as the output end, and the input and output forces are applied to the two external forces of the interaction potential energy, and according to the principle of superposition (Principle of superposition) disassembles the original design interval into two boundary conditions of only input force and only output force, as shown in Figure 4B.
因邊界條件拆解為兩種不同之設計區間,故分別對兩種邊界條件進行有限元素分析以獲得位移結果,依據虎克定律得到下列兩組靜力平衡方程式:
其中,K為包含輸入端及輸出端連接彈簧常數之全域剛性矩陣,如式(2-25)。 Among them, K is the global stiffness matrix including the spring constants of the input and output connections, as shown in Equation (2-25).
將獲得之兩種全域位移向量依式計算,可得到交互位能(MPE)目標函數如式(2-26)。 The two global displacement vectors obtained are calculated according to formula, and the objective function of interaction potential energy (MPE) can be obtained as formula (2-26).
其中,中的上標T為轉置矩陣之意。在本實施例中,以負值之交互位能最小化為目標。 in, The superscript T in it means to transpose the matrix. In this embodiment, the goal is to minimize the interaction potential energy of negative values.
元素靈敏度: Elemental Sensitivity:
元素靈敏度是作為單一元素之設計變數對於目標函數的影響程度的判斷指標,其定義為目標函數對設計變數之偏微分,其推導如下式(2-27)。 Element sensitivity is a judgment index for the degree of influence of a design variable as a single element on the objective function, which is defined as the partial differential of the objective function to the design variable, which is derived as follows (2-27).
因為K為對稱矩陣,依矩陣乘法交換律可得:,重新整理上式可得下列式(2-28)。 Because K is a symmetric matrix, according to the commutative law of matrix multiplication, we can get: , rearrange the above formula to get the following formula (2-28).
為了替換上式中全域位移向量對設計變數之偏微分,將式(2-24)對設計變數偏微分,結果如下式(2-29)所示,其中全域力量向量為常數,故偏微分後為0:
為了代入式(2-28),將式(2-29)移項整理可得式(2-30)。 In order to substitute into Equation (2-28), Equation (2-29) can be obtained by shifting the terms and finishing Equation (2-30).
將上式(2-30)代入式(2-28)可得式(2-31)。 Substitute the above formula (2-30) into the formula (2-28) to obtain the formula (2-31).
將全域元素靈敏度改寫為單一元素靈敏度:
其中,u1,j及u2,j為單一元素之位移向量,kj為單一元素上所有節點之剛性矩陣。以式(2-1)及式(2-2)來取代式(2-32)中剛性矩陣對設計變數之偏微分:
將式(2-33)代回式(2-32)以得到交互位能對設計變數之偏微分:
為將以上述拓樸最佳化方法的流程,進一步適用於致動器之邊界條件來設計軟性致動器指節,以下將依序介紹各項適用於致動器之邊界條件的設定。 In order to design the soft actuator knuckle by further applying the boundary conditions of the actuator to the flow of the above topology optimization method, the following will introduce the setting of the boundary conditions applicable to the actuator in sequence.
「矽膠材料模型」:本實施例以Smooth-on公司之Dragon skin 30矽膠作為氣動軟性夾爪製作材料,其材料硬度為30A,經拉伸測試,其抗拉強度為3.87MPa,斷裂伸長率353%。本實施例採用線彈性材料模型假設來進行拓樸最佳化設計、空負載模擬及夾持模擬,經計算工程應力與工程應變斜率間的比值,可獲得等效楊氏係數約為1.02MPa,等效密度約為1096kg/m3,蒲松比則為0.49。
"Silicone material model": In this example,
「致動器指節結構之邊界條件設定」: "Boundary condition setting of actuator knuckle structure":
本實施例將致動器定義為具氣囊之指節狀結構,透過上述拓樸最佳化方法設計具有最大彎曲能力之三氣囊指節,再將指節結構線性排列組合成一個完整致動器。為了與市售SRT公司之Meristic Adjustable Gripper-SFG-FMA2系列氣動軟性夾爪進行彎曲能力及負載重量比較,擬參考市售夾爪手指尺寸(長86×寬50×高26mm)來設計致動器,以一端為固定端,另一端為輸出端,固定端設置一氣壓輸入孔並以連通孔連接氣囊,透過氣囊充氣推動夾爪彎曲以達到夾取目標物之功能,如圖5所示。
In this embodiment, the actuator is defined as a knuckle-like structure with airbags, and three airbag knuckles with the maximum bending ability are designed through the above topology optimization method, and then the knuckle structures are linearly arranged to form a complete actuator . In order to compare the bending capacity and load weight with the commercially available Meristic Adjustable Gripper-SFG-FMA2 series pneumatic soft gripper from SRT Company, the actuator is designed with reference to the size of the gripper finger (
本實施例將設計區間由完整致動器修正為具三氣囊之指節,再將指節結構線性排列組合成一個完整致動器。指節長度由三個氣囊線性排列後決定,實際長度為16~28mm,寬度及高度則依市售SRT夾爪尺寸分別設定為50mm及26mm;氣囊以x方向等間距方式排列,y方向距離底部2mm,外層為實體非設計區間(Solid non-design domain),厚度為1~2mm,內層為空洞非設計區間(Void non-design domain)。 In this embodiment, the design interval is modified from a complete actuator to a knuckle with three airbags, and then the knuckle structures are linearly arranged and combined to form a complete actuator. The length of the knuckles is determined by the linear arrangement of the three airbags. The actual length is 16~28mm. The width and height are set to 50mm and 26mm according to the size of the commercially available SRT jaws. The airbags are arranged at equal intervals in the x direction, and the y direction is away from the bottom. 2mm, the outer layer is the solid non-design domain (Solid non-design domain), the thickness is 1~2mm, and the inner layer is the void non-design domain (Void non-design domain).
除了上述邊界條件外,因本實施例採三維拓樸最佳化方式設計致動器,相較二維拓樸最佳化設計,須再考慮z方向自由度,且夾爪實際夾取物品時夾取面不會產生z方向相對位移,故於(nelz為設計區間z方向元素量)處平面加入z方向之自由度拘束,避免拓樸最佳化結果產生不對稱結構。 In addition to the above boundary conditions, because this embodiment adopts a three-dimensional topology optimization method to design the actuator, compared with the two-dimensional topology optimization design, the degree of freedom in the z-direction must be considered again, and when the gripper actually grips the object The clamping surface will not produce relative displacement in the z direction, so the (nelz is the element quantity in the z-direction of the design interval), a degree of freedom constraint in the z-direction is added to the plane to avoid an asymmetric structure in the topology optimization result.
「邊界條件設定」可為兩種,請參閱圖6A及圖6B: There are two kinds of "boundary condition settings", please refer to Figure 6A and Figure 6B:
第一種將目標函數定義為式(3-1),僅有fin及fout兩作用力,而U1為fin作用下求得之全域位移向量,U2為fout作用下求得之全域位移向量。 The first one defines the objective function as formula (3-1), there are only two forces of f in and f out , and U 1 is the global displacement vector obtained under the action of f in , and U 2 is obtained under the action of f out the global displacement vector.
第二種將目標函數定義為式(3-3),共有fin、fout,1及fout,2三個作用力,而U1為fin作用下求得之全域位移向量,U2為fout,1與fout,2同時作用下求得之全域位移向量,兩者皆以交互位能(MPE)取代位移最大化,並以負值之交互位能最小化為目標。 The second type of objective function is defined as formula (3-3), there are three forces fin , f out,1 and f out,2 , and U 1 is the global displacement vector obtained under the action of f in , U 2 is the global displacement vector obtained under the simultaneous action of f out,1 and f out,2 , both of which are maximized by the interaction potential energy (MPE) instead of displacement, and the goal is to minimize the negative interaction potential energy.
於此,將軟性致動器彎曲能力優劣的指標定義為末端節點平均位移量及單位長度之末端節點平均位移量。前者應用於設計區間尺寸相同時之案例,後者應用於設計區間尺寸不同時之案例,當設計區間x方向長度不同時,須在除以x方向長度(nelx)。可將單輸出邊界條件下之x方向長度定義為28mm,與設計區間全長相同,位移變化則計算輸出端共51個節點之平均位移量,如圖6A所示;在雙輸出邊界條件下,將x方向長度定義為設計區間全長之一半14mm,位移變化則計算兩個輸出端共102個節點之平均位移量,如圖6B所示。 Here, the indexes of the bending ability of the soft actuator are defined as the average displacement of the end nodes and the average displacement of the end nodes per unit length. The former applies to the case where the size of the design interval is the same, and the latter applies to the case where the size of the design interval is different. When the length of the design interval in the x-direction is different, it must be divided by the length in the x-direction (nelx). The x-direction length under the single-output boundary condition can be defined as 28mm, which is the same as the full length of the design interval, and the average displacement of 51 nodes at the output end is calculated for the displacement change, as shown in Figure 6A; under the dual-output boundary condition, the The length in the x-direction is defined as half of the full length of the design interval, 14 mm, and the displacement change is calculated by calculating the average displacement of 102 nodes at the two output ends, as shown in Figure 6B.
上述兩種邊界條件之拓樸最佳化設計參數均採用相同設定,如下表3。其設計區間為長28×寬50×高26mm,由邊長1mm之正立方體網格組成;將氣囊內壁受壓面上的每個節點,給予一個大小相同且方向垂直於受壓面之輸入力量,而輸出端採相同方式,於每個節點上給予一個大小相同且方向垂直受壓面之輸出力量;輸入端及輸出端上之每個節點,給予一個彈簧常數相同且方向垂直受壓面之虛擬彈簧,其中,輸入端彈簧常數總和及輸出端彈簧常數總和皆設定為1N/m;目標體積率依表3設定,體積率容許誤差設定為±0.001。 The topology optimization design parameters of the above two boundary conditions are all set with the same settings, as shown in Table 3 below. The design interval is 28mm long x 50mm wide x 26mm high, consisting of a cube grid with a side length of 1mm; each node on the pressure surface of the inner wall of the airbag is given an input of the same size and a direction perpendicular to the pressure surface In the same way, the output end is given an output force with the same magnitude and the direction perpendicular to the pressure surface; each node on the input end and the output end is given an output force with the same spring constant and the direction perpendicular to the pressure surface The virtual spring, in which the sum of the spring constants of the input end and the sum of the spring constants of the output end are both set to 1N/m; the target volume rate is set according to Table 3, and the allowable error of the volume rate is set to ±0.001.
單輸出端及雙輸出端邊界條件之拓樸最佳化位移結果如表4所示,其輸出端位移皆隨體積率上升而下降,即位移變化量隨體積率上升而增加。如圖7所示。在體積率為0.6時,雙輸出端邊界之單位長度末端節點平均位移量為0.5mm,單輸出端邊界則為0.25mm,兩者相差100%。除了單位長度之末端節點平均位移量外,考量製造之可行性,單輸出端邊界條件因氣囊間連通結構位置並非集中於同一側,在氣囊連通氣孔及模具設計上相對較困難,故而較佳的方式是採用雙出端邊界條件之設計。 Table 4 shows the topologically optimized displacement results for the boundary conditions of the single-output terminal and the dual-output terminal. The displacement of the output terminal decreases with the increase of the volume rate, that is, the displacement change increases with the increase of the volume rate. As shown in Figure 7. When the volume ratio is 0.6, the average displacement of the end nodes per unit length of the double-output boundary is 0.5 mm, and the single-output boundary is 0.25 mm, and the difference between the two is 100%. In addition to the average displacement of the end nodes per unit length, considering the feasibility of manufacturing, the boundary conditions of the single output end are not concentrated on the same side of the communication structure between the airbags. The way is to use the design of double-outlet boundary conditions.
藉由觀察圖7可知,無論在單輸出端或雙輸出端邊界條件且體積率低於0.6時,單位長度之末端節點平均位移量會隨體積率增加而上升,當體積率 接近0.6及0.6以上時則會趨於穩定,且拓樸最佳化結構外形也會隨體積率增加而逐漸穩定,故本實施例將拓樸最佳化設計之目標體積率定義為0.6以上。 By observing Fig. 7, it can be seen that no matter in the boundary condition of single output terminal or double output terminal and the volume rate is lower than 0.6, the average displacement of the end node per unit length will increase with the increase of the volume rate. When the volume rate When it is close to 0.6 and above 0.6, it will tend to be stable, and the shape of the topology-optimized structure will gradually stabilize with the increase of the volume ratio. Therefore, in this embodiment, the target volume ratio of the topology-optimized design is defined as 0.6 or more.
「外加彈簧設計」:為了獲得較佳之目標函數及較少之拓樸最佳化疊代次數,本實施例將輸入端彈簧常數總和定義為1N/m,輸出端彈簧常數總和為1N/m。 "External spring design": In order to obtain a better objective function and fewer iterations of topology optimization, this embodiment defines the sum of the spring constants at the input end as 1N/m and the sum of the spring constants at the output end as 1N/m.
「氣囊參數設計」:將氣囊定義為拓樸最佳化之非設計區間,為探討氣囊設計對拓樸最佳化結果影響,擬透過調整氣囊之寬度(Width)、高度(Height)、厚度(Thickness)及間距(Spacing)來進行氣囊指節之拓樸最佳化設計,氣囊之設計參數如圖8所示,氣囊之設計參數設定如表5所示,拓樸最佳化參數設定如前述表3所示。 "Airbag parameter design": The airbag is defined as the non-design interval of topology optimization. Thickness) and spacing (Spacing) to optimize the topology of the airbag knuckles. The design parameters of the airbag are shown in Figure 8, and the design parameters of the airbag are set as shown in Table 5. The topology optimization parameters are set as described above. shown in Table 3.
將軟性致動器彎曲能力的比較指標定義為輸出端之末端節點平均位移量,其計算方式為輸出端總位移量除上輸出端共102個節點,拓樸最佳化得到之末端節點平均位移量繪製為圖9,末端節點平均位移量與氣囊高度及寬度皆呈正比關係,當氣囊高度增加1mm時,末端節點平均位移量會提升35.9%;當氣囊寬度增加1mm時,末端節點平均位移量會提升15.4%,故氣囊高度對位移量之影響性較高。為了達到較佳的彎曲程度同時避免產生空洞 結構,本實施例將氣囊之高度與寬度定義為24mm及50mm,並以此設定進行氣囊間距之分析。 The comparison index of the bending capacity of the soft actuator is defined as the average displacement of the end nodes at the output end. Figure 9 shows that the average displacement of the end nodes is proportional to the height and width of the airbag. When the airbag height increases by 1mm, the average displacement of the end nodes increases by 35.9%; when the airbag width increases by 1mm, the average displacement of the end nodes increases by 35.9%. will increase by 15.4%, so the airbag height has a higher influence on the displacement. In order to achieve the best degree of bending and avoid voids Structure, in this embodiment, the height and width of the airbag are defined as 24mm and 50mm, and the airbag spacing is analyzed with these settings.
氣囊間距會改變設計區間x方向長度(nelx),故將比較指標定義為單位長度之末端節點平均位移量,結果如圖10所示,單位長度之末端節點平均位移量與氣囊間距呈負相關,氣囊間距每增加1mm時,單位長度之末端節點平均位移量會下降9.3%。 The airbag spacing will change the x-direction length (nelx) of the design interval, so the comparison index is defined as the average displacement of the end nodes per unit length. The results are shown in Figure 10. The average displacement of the end nodes per unit length is negatively correlated with the airbag spacing. When the airbag spacing increases by 1mm, the average displacement of the end nodes per unit length will decrease by 9.3%.
氣囊厚度增加時會使軟性致動器耐壓程度上升,又因氣囊之剛性增加而使彎曲能力下降。本實施例將氣囊厚度分別設定為1mm、2mm、3mm來進行拓樸最佳化設計,再依單位長度平均位移量結果及耐壓程度選出最適合之條件。 When the thickness of the airbag increases, the pressure resistance of the soft actuator will increase, and the bending ability of the soft actuator will decrease due to the increase of the rigidity of the airbag. In this embodiment, the thickness of the airbag is respectively set to 1mm, 2mm, and 3mm for topology optimization design, and then the most suitable conditions are selected according to the result of the average displacement per unit length and the degree of pressure resistance.
如圖11所示。當氣囊厚度由1mm增加至2mm時,其單位長度末端節點平均位移量由1.3mm下降至0.6mm,減少約56%;當氣囊厚度由1mm增加至3mm時,其單位長度末端節點平均位移量由1.3mm下降至0.3mm,減少約76%。為了可以使耐壓程度達到60kPa以上,且維持較高之彎曲能力,故本實施例將氣囊厚度設定為2mm。 As shown in Figure 11. When the thickness of the airbag increases from 1mm to 2mm, the average displacement of the end nodes per unit length decreases from 1.3mm to 0.6mm, a decrease of about 56%; when the thickness of the airbag increases from 1mm to 3mm, the average displacement of the end nodes per unit length decreases from 1.3mm to 0.6mm. 1.3mm dropped to 0.3mm, a reduction of about 76%. In order to make the pressure resistance level above 60kPa and maintain a high bending ability, the thickness of the airbag is set to 2mm in this embodiment.
請參閱圖12及圖13所示,以下進一步說明,依上述拓樸最佳化及條件設定所形成之本發明實施例之軟性致動器,主要包含用於夾持物件之一夾持部(1),該夾持部(1)上沿一長度方向間隔設置之複數氣囊部(2),且每相鄰的二個所述氣囊(2)之間皆連接一關節部(3),以形成相對該夾持部(1)之一彎曲面(4),其中所述氣囊部(2)在所述長度方向的最大寬度約為所述關節部(3)的兩倍。另外,該夾持部(1)及每個所述氣囊部(2)皆有相互連通之一充氣流道(5),該充氣流道(5)呈圓管狀且其管徑沿該長度方向漸縮延伸。 Please refer to FIG. 12 and FIG. 13 . Further description will be given below. The soft actuator of the embodiment of the present invention formed according to the above topology optimization and condition setting mainly includes a clamping portion ( 1), a plurality of airbag parts (2) are arranged at intervals along a length direction on the clamping part (1), and a joint part (3) is connected between every two adjacent airbags (2), so as to A curved surface (4) relative to the clamping part (1) is formed, wherein the maximum width of the airbag part (2) in the longitudinal direction is approximately twice that of the joint part (3). In addition, the clamping part (1) and each of the airbag parts (2) have an inflation flow channel (5) communicating with each other, and the inflation flow channel (5) is in the shape of a circular tube and its diameter is along the length direction Tapered extension.
詳細而言,是將上述設計之指節結構平行排列至市售氣動夾爪長度尺寸(86mm)可容許之最大氣囊數量;接著將靠近前端之指節結構向前端延 伸,形成一個三角柱狀之指尖結構(6);最後為了增加夾持時軟性致動器下部之剛性以提升負載能力,將所述夾持部(1)進行加厚設計,增加4mm實心結構。 In detail, the knuckle structures of the above design are arranged in parallel to the maximum number of airbags allowed by the length of the commercially available pneumatic gripper (86mm); then the knuckle structures near the front end are extended to the front end. stretch to form a triangular column-shaped fingertip structure (6); finally, in order to increase the rigidity of the lower part of the soft actuator during clamping to improve the load capacity, the clamping part (1) is thickened and a 4mm solid structure is added. .
續請參閱圖14及圖15,所述關節部(3)於中央處有一隆起部位(31),所述隆起部位(31),該隆起部(31)位往兩側漸縮而概呈一梯形。其中所述隆起部位(31)的高度約為所述氣囊部(2)的高度的二分之一。 14 and 15, the joint portion (3) has a raised portion (31) at the center, the raised portion (31), the raised portion (31) is tapered to both sides and is approximately a trapezoid. The height of the raised portion (31) is about half of the height of the airbag portion (2).
以下,進一步以矽膠製作所設計之軟性致動器,確認上述拓樸最佳化設計方法設計之軟性致動器之彎曲能力,並與市售SRT夾爪之性能進行比較。 In the following, the designed soft actuator is further fabricated with silicone rubber, and the bending ability of the soft actuator designed by the above topology optimization design method is confirmed and compared with the performance of the commercially available SRT gripper.
為了比較本實施例之軟性致動器與市售SRT夾爪之彎曲能力,將本實施例之軟性致動器設置測試平台上。將空壓機作為壓力輸入源,以空氣導管連接調壓閥及氣壓錶,並將氣壓導入軟性致動器中。接著將軟性致動器以固定端朝上、輸出端朝下方之方向固定,由固定端輸入氣壓,壓力由0kPa開始,每次增加10kPa,並記錄其彎曲變化量,依據實驗結果匯入ImageJ並繪製其夾取面軌跡。另將市售SRT夾爪以同樣方式測試及繪製其夾取面軌跡,兩者比較圖如圖16所示。 In order to compare the bending ability of the soft actuator of this embodiment and the commercially available SRT jaws, the soft actuator of this embodiment was set on a test platform. Use the air compressor as the pressure input source, connect the pressure regulating valve and the air pressure gauge with the air conduit, and introduce the air pressure into the soft actuator. Then fix the soft actuator with the fixed end facing up and the output end facing down, input the air pressure from the fixed end, the pressure starts from 0kPa, increases by 10kPa each time, and records the bending change, according to the experimental results into ImageJ and Draw its gripping surface track. In addition, the commercially available SRT gripper was tested in the same way and its gripping surface trajectory was drawn, and the comparison chart between the two is shown in Figure 16.
由圖16可知,本實施例之軟性致動器在壓力為20kPa時,其彎曲曲率及指尖點彎曲角度已達到市售軟性致動器在80~90kPa壓力下之表現;即使市售軟性致動器在最大容許壓力100kPa下,其彎曲幅度仍遠低於本實施例之軟性致動器在30kPa下之表現。由上述結果可說明,本實施例之軟性致動器,其彎曲能力明顯優於市售結果。 It can be seen from FIG. 16 that when the pressure of the soft actuator of this embodiment is 20 kPa, the bending curvature and the bending angle of the fingertip point have reached the performance of the commercially available soft actuator under the pressure of 80-90 kPa; Under the maximum allowable pressure of 100 kPa, the bending amplitude of the actuator is still far lower than that of the soft actuator of this embodiment under 30 kPa. From the above results, it can be shown that the bending ability of the soft actuator of the present embodiment is obviously better than that of the commercially available ones.
市售SRT致動器夾取面之平均彎曲曲率及彎曲角度如圖17及圖18所示,在壓力為0~60kPa範圍內,本實施例之軟性致動器的平均彎曲曲率優於 市售軟性致動器112%以上,而彎曲角度則優於市售軟性致動器150%以上,其成效非常明顯。 The average bending curvature and bending angle of the clamping surface of commercially available SRT actuators are shown in Figures 17 and 18. Within the pressure range of 0~60kPa, the average bending curvature of the soft actuator of this embodiment is better than The commercial soft actuator is more than 112%, and the bending angle is more than 150% better than the commercial soft actuator, and its effect is very obvious.
為了測試本實施例之軟性致動器實際夾取能力,以下將二個本實施例之軟性致動器(100)以法蘭界面(200)組成一個夾爪,如圖19所示,透過夾爪進行最大負載測試及夾取範圍測試,並與市售SRT兩指式夾爪進行比較。 In order to test the actual gripping ability of the soft actuator of this embodiment, two soft actuators (100) of this embodiment are composed of a flange interface (200) to form a clamping jaw, as shown in FIG. 19, through the clamp The jaws were tested for maximum load and range of grip and compared to commercially available SRT two-finger grippers.
實驗結果紀錄如圖20所示,輸入壓力與最大負載重量呈正相關,而在最大輸入壓力為80kPa時,夾爪之最大負載重量為2665g,相比市售SRT夾爪在相同壓力下之最大負載1590g,其最大負載重量高出67.6%,而平均負載重量則高出43.82%。 The experimental result record is shown in Figure 20. The input pressure is positively correlated with the maximum load weight. When the maximum input pressure is 80kPa, the maximum load weight of the gripper is 2665g, which is compared with the maximum load of the commercially available SRT gripper under the same pressure. 1590g, its maximum load weight is 67.6% higher, while the average load weight is 43.82% higher.
以下進一步將三個本實施例之軟性致動器(100)以法蘭界面(300)組成一個夾爪,如圖21所示。透過夾爪進行夾爪最大負載測試及夾取範圍測試,並與市售三指式夾爪進行比較。 In the following, three soft actuators (100) of the present embodiment are further composed of a clamping jaw with a flange interface (300), as shown in FIG. 21 . The gripper jaw maximum load test and gripping range test were performed through the gripper jaw and compared with the commercially available three-finger gripper.
實驗結果紀錄如圖22所示,輸入壓力與最大負載重量呈正相關,而在最大輸入壓力為80kPa時,夾爪之最大負載重量為5117g,相比市售SRT夾爪在相同壓力下之最大負載2217g,其最大負載重量高出131%,平均負載重量則高出140%。 The experimental result record is shown in Figure 22. The input pressure is positively correlated with the maximum load weight. When the maximum input pressure is 80kPa, the maximum load weight of the gripper is 5117g, which is compared with the maximum load of the commercially available SRT gripper under the same pressure. At 2217g, its maximum load weight is 131% higher and its average load weight is 140% higher.
要補充說明的是,雖上述夾爪以二個、三個軟性致動器(100)的組合作為例示,但實施上並不以此為限,如圖23所示,亦可將四個以上本實施例之軟性致動器(100)以法蘭界面(400)組成一個夾爪。 It should be added that although the above-mentioned clamping jaws take the combination of two or three soft actuators (100) as an example, the implementation is not limited to this. As shown in FIG. 23, more than four The soft actuator (100) of this embodiment forms a clamping jaw with a flange interface (400).
應注意的是,上述內容僅為本發明的較佳實施例,目的在於使所屬領域的通常知識者能夠瞭解本發明而據以實施,並非用來限定本發明的申請專利範圍;故涉及本發明所為的均等變化或修飾,均為申請專利範圍所涵蓋。 It should be noted that the above content is only a preferred embodiment of the present invention, and the purpose is to enable those with ordinary knowledge in the field to understand the present invention and implement it accordingly, and not to limit the scope of the application for patent of the present invention; therefore, it relates to the present invention All equivalent changes or modifications are covered by the scope of the patent application.
(S01):步驟一
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(S02):步驟二
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(S03):步驟三
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(S04):步驟四
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(S05):步驟五
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TW201828896A (en) * | 2016-12-02 | 2018-08-16 | 美商3M新設資產公司 | Muscle or joint support article |
CN108621179A (en) * | 2018-05-07 | 2018-10-09 | 广东顺德泽洋机电制造有限公司 | A kind of soft fixture of pneumatic type |
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