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Abstract

The dynamics of the air flow between interacting surfaces of Bernoulli–vacuum gripping device and object of manipulation is analysed. The methods of increasing lifting capacity in given devices are presented. The equation for defining pressure distribution in between interacting surfaces of gripping device and object of manipulation and equations for calculation of power characteristics is calculated. The results of theoretical researches of Bernoulli–vacuum gripping devices with different forms of active surfaces are introduced.

Keywords

Bernoulli–vacuum gripping device object of manipulation air flow radial clearance nozzle

Introduction

When solving problems of automation of machined parts handling on certain machines and transfer lines, non-contacting pneumatic grippers are becoming more widely used.¹ Their specific feature is high reliability and durability, low production price, non-contacting grip and holding the objects of manipulation (OM), blanks and parts regardless of their material, mechanical characteristics, surface layer structure and temperature.

Non-contacting pneumatic grippers of industrial robots and manipulators have a range of advantages. However, there are no detailed theoretical and experimental researches in this area, which would lead to the creation of grippers with bigger carrying capacity, reliability in work and high speed of response. The analysis of scientific papers^2
–4 shows that the issue of improving the design of non-contacting pneumatic grippers aimed at providing high performance is of a low priority. The last fact is also confirmed by the analysis of designs and characteristics of Bernoulli gripping devices (BGDs), which are produced by famous foreign corporations (Bosch Rexroth, Schmalz, SMC Pneumatics, Festo).^5

–8 The Mechatronic Systemtechnik GmbH works on the design of Bernoulli–vacuum gripping devices that combine Bernoulli principle and vacuum grippers.⁹ Also, a similar principle of work is proposed in the article.^10,11 In an earlier work,¹² the values of the optimal outer diameter for a range of supply mass flow rates were calculated. In another work,¹³ a flexible, multifunctional gripper for handling variable size, shape and weight of unpacked food products is discussed.

A study by Dini et al.¹⁴ proposes the use of contactless grippers instead of more traditional vacuum cups or fingered grippers. In particular, the main objectives of this investigation are to measure the performance of different gripper configurations whose lifting force is generated by a high-speed air flow passing between the gripper and the leather ply and to analyse the dynamics of air flow in ejector and in between interacting surfaces of Bernoulli–vacuum gripping device and OM that defines the methods of increasing lifting capacity in given devices. This work also presents mathematical models, analyses force characteristics of Bernoulli–vacuum gripping devices with different forms of active surfaces and explains the choice of the most reasonable designs.

Design and operating principle of Bernoulli–vacuum gripping device

In comparison with vacuum gripping devices, the specific features of Bernoulli devices are high reliability and durability, objects’ locating accuracy and high dynamic characteristics. The disadvantages of given devices are low force characteristics.

In comparison with Bernoulli devices of the same discharge characteristics, given Bernoulli–vacuum gripping device for flat OM (Figures 1 and 2) has 2.5 to 4 times higher carrying capacity. Besides, given device does not have any important drawbacks, which are usual for vacuum gripper devices.

Figure 1.

General view of Bernoulli–vacuum gripping device.

Figure 2.

Principal scheme of Bernoulli–vacuum gripping device.

Hard suction cup 1 with suction hole 2 and through-hole 3, where ejector body 5 is added using connector adapter 4, is used in given device. Ejector body consists of nozzle 6 and bushing 7. Created reception chamber 8 is connected to the suction hole 2 via through-hole 3. Three Bernoulli grippers 9 are installed on the periphery of hard suction cup 1. Flat butt end surfaces of the grippers 9 are on the same flat surfaces, and their axes are placed within certain radius and radial space is the same. Also, the butt end surfaces of the grippers 9 are displaced from the surfaces’ butt end of the suction cup 1 so that h ₀ − h ₁ = 0.03/0.05 mm.

The principle of this gripping device is as follows: during the supply of the compressed air from pneumatic system to the nozzle 6, negative pressure is produced in chamber 8 by means of ejection, and the air is sucked from the suction hole 2 via through-hole 3, which results in the area of low pressure. Air flows from BGD nozzle 9, which are directed to the OM 10, influence on it with viscous friction and reactive repulsion force. When reducing the space h ₁ between flat surfaces of BGD and OM to smaller than 0.5 mm, suction of air flow increases and prevails reactive force. When reducing space 11, the negative pressure increases in suction hole 2 of the suction cup. As a result, the object moved in the direction of the butt end of gripper. In case h ₀ < 0.04 mm, negative pressure in suction hole 2 reaches the maximum level, and resilient pneumatic cushion between flat surfaces of BGD and OM is created.

By keeping the difference of atmosphere pressure and absolute pressure in the suction hole 2, the OM 10 is directly connected to suction cup surface butt end 1, as it is balanced by resilience of pneumatic cushions. The OM fixing from shift in a horizontal plane is made by expense of the supports 12.

Depending on structural design (Figure 3), hard suction cup 1 provides different operational characteristics (distance of OM gripping, maximum lifting force at optimal distance between gripper and OM, etc.). The solid flat surface of hard suction cup (Figure 3(a)) provides OM gripping from long distance. The shift between surface butt ends of the suction cup for δ (Figure 3(b) and (d)) or the use of capillary tube restrictor 13 in suction cup design (Figure 3(e)) provides opportunity of OM non-contact holding, even without the use of BGD. The presence of radial groove 14 in suction cup design (Figure 3(c) to (e)) provides increasing lifting force.

Figure 3.

Constructions variants of the suction cup.

Despite the fact that restraining force of Bernoulli–vacuum gripping device is generally defined with suction cup lifting capacity, the use of Bernoulli devices in their design will improve dynamic characteristics, provide objects’ gripping from larger distance and their non-contact holding.

Defining lifting force of gripping device

In general, lifting force of Bernoulli–vacuum gripping device of flat object is as follows

F = F_{1} + 3 F_{2}

where F ₁ is the force which appears as a result of impact on OM by difference of atmospheric pressure and absolute pressure in zone opposite to suction cup 1 (0 < r < r ₃); F ₂ is the force which appears as a result of impact of one BGD.¹⁵

The lifting force which is derived from vacuum suction cup (Figure 3(e)) is as follows

F_{1} = π r_{0}^{2} (p_{a} - p_{1}) + 2 π \int_{r_{0}}^{r_{1}} (p_{a} - p_{r 1}) r d r + π (r_{2}^{2} - r_{1}^{2}) (p_{a} - p_{2}) + 2 π \int_{r_{2}}^{r_{3}} (p_{a} - p_{r 2}) r d r

where p_r ₁ and p_r ₂ are the functions of air absolute pressure distribution in radial clearance according to the zones r ₀ < r < r ₁ and r ₂ < r < r ₃; p ₁ is the absolute pressure created by ejector in the suction hole 2; p ₂ is the absolute pressure in radial groove 14; p _a is the atmospheric pressure; r ₀, r ₁, r ₂ and r ₃ are the radii of the suction cup surface butt ends.

To define absolute pressure p ₁, the equation of force impulse for nozzle outlet section 6 and ejector bushing 7 should be comprised

G_{e} V_{e} + G_{Σ} V_{oc} + p_{1} S_{eb} - (G_{e} + G_{Σ}) V_{ob} - p_{a} S_{eb} - F_{f} = 0

where G _e and V _e are mass air flow and air velocity coming out from the nozzle 6;

G_{Σ} = G_{1} + G_{2}

is the total mass air flow which is sucked by ejector from atmosphere via radial clearance in zone r ₂ ≤ r ≤ r ₃ (G ₁) and restrictor 13 (G ₂); V _oc is the gripped air flow velocity at the out of suction ejector chamber 8; V _ob is the air flow velocity at the out of suction ejector body;

S_{eb} = π d_{eb}^{2} / 4

is the area of suction ejector body; d _eb is the diameter of suction ejector body; F _f is the friction force of air flow to the walls of suction ejector chamber.

On the basis of the flow continuity equation and ideal gas law, the velocity of gripped air flow at the in of ejector chamber 8 is defined as follows

V_{oc} = \frac{4 G_{Σ} R T_{a}}{π (d_{eb}^{2} - d_{en}^{2}) p_{1}}

where R = 287.14 J/(kg·°К) is the gas constant for air; Т _a is the absolute temperature of air flow in ejector mixing chamber which is approximately equal to the environmental temperature; d _en is the diameter of ejector nozzle.

Air flow velocity at the out of suction ejector chamber is defined as follows

V_{ob} = \frac{G_{e} + G_{Σ}}{S_{eb} ρ_{a}}

where ρ _a is the air density at the out of suction ejector chamber which is equal to atmospheric one.

Friction force of air flow to the walls of suction ejector chamber¹⁶

F_{f} = π λ_{e} l_{ec} d_{eb} \frac{{(G_{e} + G_{Σ})}^{2}}{8 ρ_{a} S_{eb}^{2}}

where λ _e is the average coefficient value of viscous friction to the inner walls of ejector chamber;¹⁶ l _ec is the ejector chamber length.

Taking into consideration above-mentioned dependences, the following equation will be received

G_{e} V_{e} + \frac{4 G_{Σ}^{2} R T_{a}}{π (d_{eb}^{2} - d_{en}^{2}) p_{1}} - (p_{a} - p_{1}) S_{eb} - \frac{{(G_{e} + G_{Σ})}^{2}}{S_{eb} ρ_{a}} (1 + \frac{λ_{e} l_{ec}}{2 d_{en}}) = 0

Mass air flow and velocity of supersonic flow through the nozzle 6 are defined using Saint-Venant-Vantsel equations for supercritical outflow mode¹⁷

G_{e} = μ_{en} \frac{π d_{en}^{2}}{4} p_{0} \sqrt{\frac{2}{R T_{a}} \frac{k}{k + 1} {(\frac{2}{k + 1})}^{\frac{2}{k - 1}}}

V_{en} = ϕ_{en} \sqrt{2 R T_{a} \frac{k}{k - 1} [1 - {(\frac{p_{1}}{p_{0}})}^{\frac{k - 1}{k}}]}

where $μ_{en} = ϕ_{en} ε$ is the air flow coefficient via ejector nozzle;¹⁶ $ϕ_{en}$ is the velocity coefficient; ε is the air contraction coefficient in the nozzle; p ₀ is the absolute air pressure at the in of ejector; k = 1.4 is the adiabatic exponent of the air.

In order to define mass flow of G ₁ and G ₂ and air pressure distribution in p_r ₁ and p_r ₂ radial clearance, let’s suppose that air flow velocity in radial clearance and capillary tube restrictor 13 is small, that is why these flows are considered to be laminar flows; air volume force is smaller than the pressure and friction force; thermodynamic process of air flow in radial clearance is considered to be isothermic; flat radial air flow motion is considered to be stable.

According to the study,¹⁸ the mass air flow in radial clearance may be defined as follows

G = \frac{π h_{0}^{3}}{6 μ_{d} R T_{a}} \frac{r}{d r} p_{r} d p_{r}

where μ _d = 1.71 × 10⁻⁵ + 4.94 × 10⁻⁸ t (kg/(s×m)) is the coefficient of air dynamic viscosity.

Taking into consideration flow continuity condition G = constant in any section, the following equations will be right

\begin{array}{l} G_{1} \int_{r_{3}}^{r_{2}} \frac{d r}{r} = \frac{π {(h_{0} + δ)}^{3}}{6 μ_{d} R T_{a}} \int_{p_{a}}^{p_{2}} p_{r 2} d p_{r 2} \\ G_{Σ} \int_{r_{1}}^{r_{0}} \frac{d r}{r} = \frac{π h_{0}^{3}}{6 μ_{d} R T_{a}} \int_{p_{2}}^{p_{1}} p_{r 1} d p_{r 1} \end{array}

their solutions will be the equations for defining mass air flow

\begin{array}{l} G_{1} = \frac{π {(h_{0} + δ)}^{3} (p_{a}^{2} - p_{2}^{2})}{12 μ_{d} R T_{a} ln \frac{r_{3}}{r_{2}}} \\ G_{Σ} = \frac{π h_{0}^{3} (p_{2}^{2} - p_{1}^{2})}{12 μ_{d} R T_{a} ln \frac{r_{1}}{r_{0}}} \end{array}

When integrating equation (11) this way

G_{Σ} \int_{r_{1}}^{r} \frac{d r}{r} = \frac{π h_{0}^{3}}{6 μ_{d} R T_{a}} \int_{p_{2}}^{p_{r 1}} p_{r 1} d p_{r 1}, G_{1} \int_{r_{3}}^{r} \frac{d r}{r} = \frac{π {(h_{0} + δ)}^{3}}{6 μ_{d} R T_{a}} \int_{p_{a}}^{p_{r 2}} p_{r 2} d p_{r 2}

taking into account equation (12), pressure distribution functions in radial clearance will be received

\begin{array}{l} p_{r 1} = \sqrt{p_{2}^{2} - \frac{p_{2}^{2} - p_{1}^{2}}{ln \frac{r_{1}}{r_{0}}} ln \frac{r_{1}}{r}} \\ p_{r 2} = \sqrt{p_{a}^{2} - \frac{p_{a}^{2} - p_{2}^{2}}{ln \frac{r_{3}}{r_{2}}} ln \frac{r_{3}}{r}} . \end{array}

The mass air flow G ₂, which is sucked from the atmosphere via capillary tube restrictor 13 in radial groove 14, may be defined using the equation¹⁷

G_{2} = \frac{π d_{c}^{4} (p_{a}^{2} - p_{2}^{2})}{256 μ_{d} R T_{a} b}

where d _c and b are diameter and length of capillary tube restrictor, respectively.

Taking into consideration that $G_{Σ} = G_{1} + G_{2}$ , we’ll get

\frac{π h_{0}^{3} (p_{2}^{2} - p_{1}^{2})}{12 μ_{d} R T_{a} ln \frac{r_{1}}{r_{0}}} = \frac{π {(h_{0} + δ)}^{3} (p_{a}^{2} - p_{2}^{2})}{12 μ_{d} R T_{a} ln \frac{r_{3}}{r_{2}}} + \frac{π d_{c}^{4} (p_{a}^{2} - p_{2}^{2})}{256 μ_{d} R T_{a} b}

from which

p_{2}^{2} = \frac{p_{a}^{2} (\frac{{(h_{0} + δ)}^{3}}{3 ln (r_{3} / r_{2})} + \frac{d_{c}^{4}}{64 b}) + p_{1}^{2} \frac{h_{0}^{3}}{3 ln (r_{1} / r_{0})}}{\frac{{(h_{0} + δ)}^{3}}{3 ln (r_{3} / r_{2})} + \frac{d_{c}^{4}}{64 b} + \frac{h_{0}^{3}}{3 ln (r_{1} / r_{0})}}

G_{Σ} = \frac{π h_{0}^{3} p_{1}^{2}}{12 μ_{d} R T_{a} ln (r_{1} / r_{0})} (\frac{\frac{p_{a}^{2}}{p_{1}^{2}} (\frac{{(h_{0} + δ)}^{3}}{3 ln (r_{3} / r_{2})} + \frac{d_{c}^{4}}{64 b}) + \frac{h_{0}^{3}}{3 ln (r_{1} / r_{0})}}{\frac{{(h_{0} + δ)}^{3}}{3 ln (r_{3} / r_{2})} + \frac{d_{c}^{4}}{64 b} + \frac{h_{0}^{3}}{3 ln (r_{1} / r_{0})}} - 1)

After substituting equations (17), (8) and (9) in (7) and after transforming them, we will receive the equation from which absolute pressure p ₁ in ejector chamber will be defined using numerical methods

\begin{array}{l} 1.4229 μ_{en}^{2} d_{en}^{2} p_{0} (1 - {(\frac{p_{1}}{p_{0}})}^{0.1429}) - \frac{π d_{en}^{2}}{4} (p_{a} - p_{1}) \\ + \frac{π h_{0}^{6} p_{1}^{3}}{36 μ_{d}^{2} R T_{a} (d_{eb}^{2} - d_{en}^{2}) {(ln (r_{1} / r_{0}))}^{2}} {(\frac{\frac{p_{a}^{2}}{p_{1}^{2}} (\frac{{(h_{0} + δ)}^{3}}{3 ln (r_{3} / r_{2})} + \frac{d_{c}^{4}}{64 b}) + \frac{h_{0}^{3}}{3 ln (r_{1} / r_{0})}}{\frac{{(h_{0} + δ)}^{3}}{3 ln (r_{3} / r_{2})} + \frac{d_{c}^{4}}{64 b} + \frac{h_{0}^{3}}{3 ln (r_{1} / r_{0})}} - 1)}^{2} \\ - \frac{4 + \frac{2 λ_{e} l_{eb}}{d_{eb}}}{π ρ_{a} d_{eb}^{2}} {(\begin{array}{l} \frac{0.5378 μ_{en}^{} d_{en}^{2} p_{0}}{\sqrt{R T_{a}}} + \\ + \frac{π h_{0}^{3} p_{1}^{2}}{12 μ_{d} R T_{a} ln (r_{1} / r_{0})} (\frac{\frac{p_{a}^{2}}{p_{1}^{2}} (\frac{{(h_{0} + δ)}^{3}}{3 ln (r_{3} / r_{2})} + \frac{d_{c}^{4}}{64 b}) + \frac{h_{0}^{3}}{3 ln (r_{1} / r_{0})}}{\frac{{(h_{0} + δ)}^{3}}{3 ln (r_{3} / r_{2})} + \frac{d_{c}^{4}}{64 b} + \frac{h_{0}^{3}}{3 ln (r_{1} / r_{0})}} - 1) \end{array})}^{2} = 0 \end{array}

As a result, force F ₁ will be shown in integral

\begin{array}{l} F_{1} = π r_{0}^{2} (p_{a} - p_{1}) + π (r_{2}^{2} - r_{1}^{2}) (p_{a} - p_{2}) \\ + 2 π \int_{r_{0}}^{r_{1}} (p_{a} - \sqrt{p_{2}^{2} - \frac{p_{2}^{2} - p_{1}^{2}}{ln \frac{r_{1}}{r_{0}}} ln \frac{r_{1}}{r}}) r d r \\ + 2 π \int_{r_{2}}^{r_{3}} (p_{a} - \sqrt{p_{a}^{2} - \frac{p_{a}^{2} - p_{2}^{2}}{ln \frac{r_{3}}{r_{2}}} ln \frac{r_{3}}{r}}) r d r \end{array}

the solution of which is found using approximate approach, after previously calculating the value of p ₁ and p ₂ using dependences (18) and (16).

Justification of the gripping device surface parameters

The research of influence of power supply parameters and Bernoulli–vacuum gripping device design parameters on their operational characteristics was done using above-mentioned method. The calculations have been conducted for different values of excess pressure p _0ex = p ₀ – p _a and different types of suctions cups with the following parameters: r ₀ = 10 mm, r ₁ = 11 mm, r ₂ = 30 mm, r ₃ = 40 mm, d _en = 1.5 mm, d _eb = 3 mm, l _eb = 10 mm, μ _en = 0.92 and λ _eb = 0.035. The negative pressure distributions, which are formed by different types of suctions cups, on the OM surface are presented in Figure 4. The graphs of vacuum amount dependences p _2v = p _a – p ₂ and p _1v = p _a – p ₁, which are formed by ejector in radial groove 14 and suction hole 2, from radial clearance are given in Figures 5 and 6.

Figure 4.

Negative pressure distributions on the surface of object manipulation, which are formed by different types of suctions cups (p _0ex = 200 kPa; h ₀ = 0.04 mm).

Figure 5.

The vacuum amount dependences in the radial groove 14 of suction from radial clearance h ₀ for grippers with different suction cup design parameters (p _0ex = 300 kPa).

Figure 6.

The dependence of vacuum values formed by ejector in the suction hole 2 from radial clearance h ₀ for grippers with different suction cup design parameters (p _0ex = 300 kPa).

As it may be seen in Figure 4, the width of negative pressure zones on the OM surface and their numerical values essentially depend on design of the hard suction cup. For instance, Bernoulli–vacuum gripping devices which have radial groove 14 increase the width of negative pressure zone. Therefore, they will provide more lifting force. When using capillary tube restrictor or having a shift δ between surface butt ends (Figure 4), numerical values of negative pressure in the radial groove 14 (Figure 5) decrease. However, a possibility of OM non-contacting holding is preserved.

Amount of vacuum formed by ejector in the radial groove 14 and suction hole 2 most of all depends on the radial clearance value (Figures 5 and 6). When h ₀ < 0.01 mm, negative pressure reaches maximum values, and when h ₀ = 0.1 mm, it is 10%–20% from maximum values.

Components F ₁, F ₂ and resulting lifting force F were calculated using equations (1) and (19) and above-mentioned method.¹⁵ The graphs of dependence of these forces from the value of radial clearance h ₀ are shown in Figures 7 and 8. They were calculated with excess pressure of ejector power supply and Bernoulli devices p _0ex = 300 kPa and different types of suctions cups with the following parameters: r ₀ = 25 mm, r ₁ = 26 mm, r ₂ = 30 mm, r ₃ = 40 mm, d _en = 1 mm, d _eb = 2 mm, l _eb = 8 mm, μ _en = 0.92, λ _eb = 0.035, radius of the nozzle BGD r _n = 1 mm and radius of the butt end BGD r _ef = 12 mm.

Figure 7.

The dependence of force component F ₁ from radial clearance h ₀ for grippers with different suction cup design parameters.

Figure 8.

The dependence of resulting force F from radial clearance h ₀ for grippers with different suction cup design parameters.

Figures 7 and 8 show that the radial groove 14 in suction cup increases OM lifting force. However, if restrictor 13 is additionally used in the suction cup with a radial groove 14 or it has a shift δ between surface butt ends, it leads to the decrease in lifting force approximately for 30%. In this regard, possibility of non-contacting holding of OM even without the use of Bernoulli devices 9 is provided. In this case, optimal value of radial clearance is obtained when h ₀ = 0.02–0.04 mm (Figure 7).

The use of Bernoulli devices 9 in given device provides shock-free gripping of the objects, just like when h ₀ < 0.08 mm between surface butt ends of Bernoulli devices and the OM, and three resilient pneumatic cushions are created. Such combination provides gripping of OM from larger distance and reliable non-contacting holding in the process of manipulation. If suction cup and Bernoulli devices’ surface ends are on the same flat surfaces, the maximum suction force of parts by multiple-unit gripper is shown in spaces h ₁ = 0.04–0.06 mm.

To determine the advantages and disadvantages (Table 1) of Bernoulli–vacuum grippers with different designs of suction cup (Figure 3), the following parameters were analyzed: maximum lifting capacity, maximum distance where OM of certain weight may be gripped and working value (equal to stable value of gripped OM) of radial clearance.

Table 1.

Advantages and disadvantages of Bernoulli–vacuum gripping devices with different suction cup designs.

Suction cup design	Characteristics of Bernoulli–vacuum gripping devices (high values +/low values −)
Suction cup design	Lifting capacity	Distance of OM gripping	Working radial clearance
Figure 3(a)	−	++	+
Figure 3(b)	−	+	+
Figure 3(c)	++	+	−
Figure 3(d)	−	−	−
Figure 3(e)	+	+	+

OM: object of manipulation.

So, to provide maximum lifting capacity, according to Figure 3(c), suction cup should be used. If it is required to grip OM from larger distance, according to Figure 3(a), the suction cup should be used. Suction cup design, according to Figure 3(e), is the most satisfying one. Suction cup design, according to Figure 3(d), has the worst characteristics, that’s why it is unreasonable.

The total mass flow rate of air consumed by the Bernoulli–vacuum gripping device (Figure 9) is calculated using the equation G = G _e + 3G _bvgd, where G _bvgd is the mass flow rate of air consumed by one BGD. In accordance with equation (8), we obtain

G = π (μ_{en} \frac{d_{en}^{2}}{4} + 6 μ_{bg} r_{n} h_{1}) p_{0} \sqrt{\frac{2}{R T_{a}} \frac{k}{k + 1} {(\frac{2}{k + 1})}^{\frac{2}{k - 1}}}

Figure 9.

Dependence of the capacity flow of air on the pressure of the supply.

where μ _bg = 0.78–0.82 is the air flow rate through the nozzle of the BGD.

The total volume of air flow is brought to normal conditions Q = G/ρ _a, where ρ _a = 1293 kg/m³ is the density of air under normal conditions.

The indicator of the noise characteristics of the Bernoulli–vacuum gripping device is the level of sound that appears when the compressed air flows from the nozzle of gripper and the exhaust chamber of the ejector. At pressures of power supply of the Bernoulli–vacuum gripping device to 300 kPa, the noise does not exceed the sound level of 90 dB, which corresponds to the sanitary norms. If there is an object at the end of the Bernoulli–vacuum gripping device, the noise level is reduced. To reduce noise at the output of the ejector, silencer should be used.

The Bernoulli–vacuum gripping device is used for contactless holding of manipulation objects with a surface sensitive to damage, for example object manipulation of fragile material or objects that have different coverage.

Conclusion

Mathematical models that allow to determine the distribution of negative pressure on the surface of OM and power characteristics of Bernoulli–vacuum gripping device were proposed.

On the basis of the conducted modeling, the influence of the design parameters of the vacuum suction cup on the performance characteristics of the Bernoulli-vacuum grippers was established. The performance of characteristics of Bernoulli–vacuum gripping device was investigated.

Reasonable designs of vacuum suctions cups are presented and their parameters are explained, which will allow to increase lifting capacity of Bernoulli–vacuum grippers or to decrease compressed air flows.

Footnotes

Declaration of conflicting interests

The author(s) declared no potential conflict of interest with respect to the research, authorship and/or publication of this article.

Funding

The author(s) disclosed receipt of the following financial support for the research, authorship, and/or publication of this article: This work was supported by Slovak National Grants Req-00347-0001, VEGA 1/0065/16, APVV-16-0006 and VEGA 1/0752/17.

References

Kozyrev

. Gripping devices and industrial robots’ tools. Moscow: Knorus, 2011. (in Russian: Zakhvatnye ustroistva instrumenty promyshlennykh robotov).

Ozcelik

Erzincanli

Findik

. Evaluation of handling results of various materials using a non-contact end-effector. Ind Robot Int J 2003; 30(4): 363–369.

Ozcelik

Erzincanli

. Examination of the movement of a woven fabric in the horizontal direction using a non-contact end-effector. Int J Adv Manuf Technol 2004; 25(5–6): 527–532.

Davis

Gray

Caldwell

. An end effector based on the Bernoulli principle for handling sliced fruit and vegetables. Robot Comput Int Manuf 2008; 24(2): 249–257.

Bosch Rexroth

. The drive & control company—Bosch Rexroth AG. Boschrexroth.com, 2017. https://www.boschrexroth.com/en/xc/home/index (accessed 14 October 2017).

Vacuum Components, Floating Suction Pads SBS. Millsom.com.au, 2017. http://www.millsom.com.au/products/vacuum-components/special-grippers/sbs (accessed 14 October 2017).

SMC Products. Smcworld.com, 2017. http://www.smcworld.com/products/en/vacuum/s.do?ca_id=1036 (accessed 14 October 2017).

Festo - Support Portal - Bernoulli gripper OGGB. Festo.com, 2017. https://www.festo.com/net/sv_se/SupportPortal/default.aspx?cat=4564 (accessed 14 October 2017).

End Effectors - Mechatronic Systemtechnik GmbH. Mechatronic.at, 2017. http://www.mechatronic.at/technology/end-effectors.html (accessed 14 October 2017).

10.

Stühm

Tornow

Schmitt

. A novel gripper for battery electrodes based on the Bernoulli-principle with integrated exhaust air compensation. Procedia CIRP 2014; 23: 161–164.

11.

Shi

. Optimization of outer diameter of Bernoulli gripper. Exp Therm Fluid Sci 2016; 77: 284–294.

12.

Kagawa

. Theoretical and experimental study of factors affecting the suction force of a Bernoulli gripper. J Eng Mech 2014; 140(9): 04014066.

13.

Sam

Nefti

. A novel, flexible and multi-functional handling device based on Bernoulli principle. In: IEEE International Conference on System Engineering and Technology (ICSET), Shah Alam, 27–28 June 2011, pp. 166–171. doi: 10.1109/ICSEngT.2011.5993443.

14.

Dini

Fantoni

Failli

. Grasping leather plies by Bernoulli grippers. CIRP Annal 2009; 58(1): 21–24.

15.

Prots

Savkiv

. Gas-dynamic analysis of Bernoulli devices for flat blanks. In: Optimization of industrial processes. Sevastopol: SevGTU Editor Kopp V.Ya., Vol. 1, 1999, pp. 63–68. (in Russian: Gazodinamicheskiy analiz struinykh zakhvatov ploskikh zagotovok).

16.

Idel’chik

. Flow friction manual. Mashynostroyeniye, 1992. (in Russian: Idel’chik, I. E. (1992). Spravochnik po gidravlicheskim soprotivleniyam; pod redaktsiey MO Shteynberga, Handbook of hydraulic resistance; ed. by MO Shteynberg. Moscow, Mashinostroenie Publ.).

17.

Fedorets

Pedchenko

Strutynskyi

. Hydraulic drive and hydraulic and pneumatic control systems. Edited by Fedorets. Kyiv: Vyshchashkola, 1995. (in Ukrainian: Hidropryvody ta gidropnevmoavtomatyka).

18.