# Estimation of the friction force during the needle insertion using the disturbance observer and the recursive least square

- Yuta Fukushima
^{1}Email author and - Kiyoshi Naemura
^{1}

**1**:14

https://doi.org/10.1186/s40648-014-0014-7

© Fukushima and Naemura; licensee Springer 2014

**Received: **14 January 2014

**Accepted: **24 July 2014

**Published: **5 September 2014

## Abstract

Needle insertion can be performed with the aid of an ultrasound (US) image. Detecting the position of a needle in a US image requires considerable technical expertise. To detect whether the needle has reached the target, the physician usually relies on physically sensing the amount of force being fed back from the tip of the needle to their fingertip. The goal of our research was to develop a force visualization system to assist physicians by providing them with a visual representation of the needle tip force. In this paper, we elucidated the characteristics of the force during the needle insertion, and designed the friction force estimation method. Needle tip force is difficult to estimate directly. The total insertion force acting on the needle was defined by adding the needle tip force to the friction force of the needle surface. Therefore, we proposed a method of estimating the change in the friction force by measuring the total insertion force during needle insertion using recursive least square method and a disturbance observer. The needle tip and friction forces were modeled on the basis of the results of *in vitro* experiments used pork back ribs. The experiments performed using the coaxial needle. This needle could measure the total insertion force and the needle tip force separately in real time. The validity of the designed estimator was evaluated by using the force values obtained by using a coaxial needle. As a result, the estimated friction force and measured friction force were found to be qualitatively consistent. However, a slight error was observed.

## Keywords

## Background

Needle insertion is commonly used as a means of administering medication or anesthetics, performing biopsies, and aspirating fluids. Certain needle insertion procedures, such as percutaneous ethanol injection and radiofrequency ablation, are classified as types of minimally invasive surgery. If such procedures were performed without any image of the patient, however, human error may result in the insertion of the needle into an unintended target. Although needle insertion can be performed with the aid of an ultrasound (US) image, US images cannot be used for patients with large amounts of body fat. Furthermore, detecting the position of a needle in a US image requires considerable technical expertise. To detect whether the needle has reached the target, the physician usually relies on physically sensing the amount of force being fed back from the tip of the needle to their fingertip. Detection success thus varies according to the degree of proficiency of the individual. Thus, it would be possible to improve the insertion accuracy if a visual representation of the needle tip force could be provided to the physician. The current study focused on the regions where the needle tip force changes sharply upon reaching a target, such as the cava, blood vessels, and cancerous tumors.

The forces acting on the needle tip include those generated by cutting the tissue and the reactive force from the tissue [1]. Therefore, the needle tip force has been difficult to estimate simply by considering the total insertion force. Rather, the needle tip force should be obtained by subtracting the estimated friction force from the total insertion force.

There have been several recent studies on force visualization during needle insertion. Okamura *et al.*[1] and Simone *et al.*[2] elucidated, from an experiment using a cow liver, that the force acting on a needle can be modeled by summing the friction force, the cutting force, and the stiffness force. Kobayashi *et al.*[3] modeled the friction force based on the relative velocity between the needle and the tissue through an experiment using a hog liver. The purpose of these studies was not to detect the penetration of the needle into the tissue; rather, the estimated force was compared with the measured true value in real time. The friction force acting on the needle proved difficult to measure. Kataoka *et al.*[4] and Washio *et al.*[5] developed a coaxial needle consisting of an inner needle and outer sheath cannula. This needle could measure the total insertion force and the needle tip force separately in real time. The friction force could then be calculated by subtracting the measured needle tip force from the total insertion force.

The friction coefficient, stiffness, and damping coefficient of living tissue change in real time. Carra *et al*. [6] proposed a model in which the total insertion force was decomposed into a stiffness force, friction force, and cutting force. This model could explain the sharp decrease in the total insertion force. However, they did not perform an evaluation of the model using living tissue data. In a related study on the changes in the parameter estimates, Umeno *et al*. [7] proposed a method of estimating the air pressure in tires by using the recursive least square (RLS) method and a disturbance observer. This method was capable of estimating changing parameters in real time. RLS is an adaptive filter with a low calculation cost, and it is capable of estimating the coefficient quickly. Baurbe *et al*. [8],[9] used RLS to produce a highly accurate model of the total insertion force. They did not, however, develop a method of separating the needle tip force from the friction force. Moreover, the evaluation produced by the model did not use the needle tip force and friction force that were measured in real time.

The goal of our research was to develop a force visualization system to assist physicians by providing them with a visual representation of the needle tip force. In this paper, we elucidated the characteristics of the force during the needle insertion, and designed the friction force estimation method. Needle tip force is difficult to estimate directly. Estimation of the friction force has an important implication to estimate the needle tip force. To estimate the friction force, we proposed a method of estimating the change in the friction force by measuring the total insertion force during needle insertion using RLS and a disturbance observer. The estimated friction force using the proposed method allowed us to determine the estimation accuracy, but raised problems when compared with the measured true value obtained with a coaxial needle. The novelty of this study was to elucidate the characteristic of the force during and after needle insertion.

## Methods

### Characteristics of the needle insertion force

#### Coaxial needle

*f*

_{ needle }was defined by adding the needle tip force

*f*

_{ tip }to the friction force

*f*

_{ friction }of the needle surface [4]. The friction force changed with variations in the pressure applied to the needle by the tissue and the contact area between the needle and the tissue [10]. To measure the force acting on the needle during insertion, the coaxial needle was developed as shown in Figure 2. The coaxial needle consisted of a 19 gauge inner needle (Safelet cannula GA, Nipro Co., Japan) and a 16 gauge outer sheath cannula designed for this experiment. The force acting on the needle was measured by two force sensors. The needle tip force acting on the inner needle was measured by a load cell TL3B09-50 N, (Tec Gihan Co. Ltd., Japan), and the total insertion force was measured by another load cell (LMC-21023, Nissho electric works Co. Ltd., Japan). The rated capacity of the force sensors was 50 N, and 100 N, respectively. The friction force was obtained by subtracting the needle tip force from the total insertion force. The designed coaxial needle included the error 1 N that is derived from experiment equipment.

#### Needle insertion experimental setups

#### Experimental results

In phase I, the total insertion force increased non linearly until the needle penetrated the test piece. At that instant, the total insertion force was equivalent to the needle tip force, and the friction force was zero. Also, the test piece surface was deformed by about 5 mm by the needle.

In phase II, the total insertion force waveforms exhibited several peaks. On the other hand, the needle tip force remained constant at 0.5 N while the total insertion force increased. The total insertion force decreased with needle tip force.

### Discussion

In phase I, the total insertion force increased non linearly until the needle penetrated the tissue surface. Fung *et al.*[12] stated that the insertion force present until the instant at which the needle punctures the tissue surface was generated by the viscoelasticity of the tissue.

In phase II, the total insertion force, the friction force, and the needle tip force repeatedly increased and decreased. This can be explained by the fact that muscle tissue consists of fibers and bundles [13]. The needle insertion force increased while the muscle fibers deformed, and then fell as the muscular tissue ruptured. The needle tip force was a constant 0.5 N while the total insertion force increased.

In phase III, after the needle penetrated from the opposite side of the sample, the friction force increased slightly. This phenomenon was not observed in phase II, because the needle cut the thin tissue in the beginning of phase III. In cutting the thin tissue, the needle was deformed the tissue. After penetration of the tissue, the tissue moved to the opposite direction of the needle.

## Estimation of the friction force

### Model of the insertion force

*et al.*[14] performed experiments to determine the velocity dependence of the needle tip force by using a porcine heart. We modeled the insertion force in single layer tissue of phase II as shown below.

Here, the mass of the needle was defined as *m*, the coefficient *μ* was the dynamic friction coefficient, the pressure *P* was applied to the needle by the tissue, the diameter *d* was the diameter of the needle, the vector *ω* was the disturbance vector which acted on the system, and the coefficient of the insertion speed *s* was the coefficient that defined how the needle tip force changed with the insertion speed. Equation (1) explains is the force acting on the needle inserted to the silicone. If equation (1) applies to pork back ribs, the disturbance *ω* includes the parameter variation from preset value of the equation (1). Umeno *et al*. [7] presented the parameter variation estimation method using the RLS and disturbance observer as mentioned in introduction. In general the disturbance *ω* can estimate by the disturbance observer. The needle tip force was exhibited constant value, while the needle cut the tissue at the fixed speed as shown in chapter II. The variation value is only the friction force in equation (2) under fixed speed. Therefore, if the RLS and the disturbance observer were able to design, the friction force into pork back ribs under the constant insertion speed was able to estimate. In this paper, the disturbance observer was employed to estimate the disturbance *ω*, and the variation parameter *ΔμP* in equation (1) was obtained using the RLS.

### Design of the disturbance observer

*λ*was the total insertion force

*f*

_{ needle }.

*y*was control output vector. The state variables were set as the insertion distance

*x*and the insertion speed$\dot{x}$. The state variable matrix

*X*, the system coefficient matrix

*A*, the driven matrix

*B*, the output matrix

*C*, and the coefficient matrix

*D*of the disturbance vector

*ω*that was the determining matrix for the disturbance invasion route were defined as

Here, if the system changed, the disturbance *Dω* was included in the system noise and the fluctuation components. So, we designed the system to estimate *ω*.

*Z*, the system coefficient matrix

*M*, the driven matrix

*N*, and the output matrix

*O*were defined as

Thus, we could design an observer to estimate the unmeasured state and the disturbance *ω*.

*x*and$\dot{x}$) to the estimated state

*X*. The full order observer was designed as shown by equations (9) and (10).

Here, the matrix$\widehat{Z}$was the estimated value of state *Z*, the coefficient *L* was the observer gain, and the matrix$\widehat{Y}$was the estimated value of output equation *Y*.

### Design of parameter variation method using RLS

*et al*. [7]. The general state system was defined as shown below, including the input

*λ*, white noise

*d*, and the state variable

*X*. The matrix

*A*and

*B*were the foregoing matrixes in equation (5).

*A*and

*B*fluctuate, the system after fluctuation was given as

*Dω*was defined as

Thus, the parameter fluctuation and disturbance could be defined as being equivalent.

*Dω*could be approximated as

*B*becomes constant at zero. Thus, the matrix Δ

*A*and the state

*X*were defined, and equation (14) could be deformed as

*H*(

*n*) was covariance matrix [15]. The predictive error

*e(n)*was given by

Here, the matrix$\mathrm{\Delta}\widehat{A}$was the changing estimated value of matrix *A*, *K* was the forgetting coefficient, and *n* was the sample data number.

*A*obtained from the proposed method was the fluctuation value of the system matrix A from the initial value in equation (5). So, the presented method can concurrently estimate the values of changing parameters

*μ*,

*P*, and

*s*in equation (1). These coefficients defined the relationship between the friction force and the needle tip force. In chapter II, the needle tip force remained constant during the increase in the total insertion force. This meant that the parameter defining the relationship with the needle tip force variation could not be generated. Thus, in this study, we assumed that the parameter fluctuation related to the needle tip force was negligible, and that the fluctuating parameter could be attributed to the fluctuation of

*P*and

*μ*. Figure 7 is a block diagram of the above. The disturbance observer estimated the disturbance and the state variable. The estimated disturbance included the fluctuating parameters such as

*μ*and

*P*. The fluctuating parameters were estimated by RLS using the estimated disturbance. The initial setting parameter included a measurement error. The proposed method compensated for this measurement error.

### Simulation conditions

*μ*was varied to one tenth of the base value 6.63. If the forgetting coefficient

*K*for RLS is set between 0.0 and1.0, the estimation system is insusceptible of the estimated pre value$\widehat{\theta}\left(n-1\right)$, and is susceptible by noise. So, the forgetting coefficient

*K*was set to 0.80. The pole of equation (3) was [-1.09 -89.3 0.00]

^{T}. The observer gain

*L*should be set negative value than pole of equation (3) on the complex plane. The observer gain

*L*was set to [5.90 × 10

^{3}1.14 × 10

^{7}-1.74 × 10

^{10}]

^{T}. The pole of proposed method included observer was set to [-2.0 × 10

^{3}-2.0 × 10

^{3}-2.0 × 10

^{3}].

**Initial value for the friction force estimation method during the needle insertion**

Needle diameter | 1.60 × 10 | |

Needle mass | 2.18 × 10 | |

Dynamic friction coefficient μ | 0.663 | 6.63 |

The Pressure of tissue to the needle | 63.7 × 10 | |

The coefficient of velocity | 197 |

## Results

### Estimation results

*b*was the total number of the data, the data number was defined as

*i*, the estimation value of the friction force was defined as${\widehat{F}}_{\mathit{fi}}$, and the measurement value of the friction force by the coaxial needle was defined as

*F*

_{ fi }. The estimation error and the total insertion force were shown in Figure 9. The average error, the maximum error and the RMSE in each phase were shown in Table 2 and Table 3 respectively. Here, to obtain the RSL of each phase, the integer numbers

*b*of each phase were set 1667 (

*x*: 0.00 to 5.00 mm), 7300 (

*x*: 5.00 to 26.9 mm), and 1034 (

*x*: 26.9 to 30.0 mm), respectively. The maximum estimation error in phase II was -0.27 N. The average estimation error was -0.10 N. The estimation error increased in the negative direction immediately after the total insertion force fell sharply in phase II. The RMSE were increased in both phase II and phase III.

**The estimation error in each insertion phase**

Phase | Average value [N] | Maximum error [N] |
---|---|---|

I | -0.05 | -0.13 |

II | -0.10 | -0.27 |

III | 0.24 | 0.29 |

**The RMSE in each insertion phase**

Phase | RMSE [N] | |
---|---|---|

μ: 6.63 | μ: 6.63 × 1/10 | |

I | 0.07 | 0.07 |

II | 0.14 | 0.14 |

III | 0.24 | 0.24 |

*μ*was set to one tenth of the base value is shown in Figure 10. The result for the estimation error was completely consistent with the results for the estimation error by the base value. The RMSE which

*μ*was set to one tenth of the base value is shown in Table 3. The RMSE was also completely consistent with the result of the base value. Therefore, we found that changing the dynamic friction coefficient had no effect on the robustness of the disturbance observer.

## Discussion

### Discussion

The estimation error increased in phase I as shown in Figure 9. Phase I exhibited a characteristic in that the friction force did not act on the needle, although the proposed method could not capture the characteristic of the friction force in phase I. Thus, the larger estimation error was observed.

In phase II, the total insertion force fell sharply as the muscle bundle was cut. The estimation error increased as the muscle bundle deformed, because the proposed method did not consider the characteristics of tissue deformation.

The friction force increased as a result of tissue relaxation, the estimation error could be observed in phase III. We assumed that the estimation error increased as a result of the tissue deformation, because the estimation error increased in the negative immediately after the total insertion force decreased sharply. Thus, the estimation error increased in insertion phases II and III, especially given that these phases included tissue cutting. The RMSE, indicating the dispersion from the true value, also increased in phases II and III. This means that the RMSE increases as a result of tissue cutting.

Changing the dynamic friction coefficient had no effect on the robustness of the disturbance observer. Thus, the proposed method was robust to difference of initial parameter. This means that the velocity estimated by the disturbance observer was greater than the parameter changing velocity. If the observer gain changed, so too did the estimation accuracy.

In the future, we will enhance the proposed method by including the effect of tissue deformation and relaxation.

## Conclusion

The goal of our research was to develop a force visualization system to assist physicians by displaying the needle tip force. In this paper, the needle tip and friction forces were modeled on the basis of the results of our experiments. The validity of the designed estimator was evaluated by using the force values obtained by using a coaxial needle. As a result, both forces were found to be qualitatively consistent. However, a slight error was observed. In the future, to reduce this estimation error, we will design a system that considers the force resulting from tissue deformation and characteristics of the insertion force.

## Declarations

### Acknowledgment

The authors are grateful to Mr. H. Saito, Mr. T. Yamazaki and Mr. S. Nagatomo (UNISIS Corporation Japan) for their assistance in creating the outer sheath cannula. The authors also thank Dr. Y. Koseki of the National Institute of Advanced Industrial Science and Technology (AIST) for his advice on the coaxial needle.

## Authors’ Affiliations

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## Copyright

This article is published under license to BioMed Central Ltd. This is an Open Access article distributed under the terms of the Creative Commons Attribution License (http://creativecommons.org/licenses/by/2.0), which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly credited.