1111 lines
65 KiB
TeX
1111 lines
65 KiB
TeX
% Created 2025-04-02 Wed 10:56
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% Intended LaTeX compiler: pdflatex
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\documentclass[a4paper, 10pt, DIV=12, parskip=full, bibliography=totoc]{scrreprt}
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\input{preamble.tex}
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\input{preamble_extra.tex}
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\bibliography{nass-geometry.bib}
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\author{Dehaeze Thomas}
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\date{\today}
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\title{Nano Hexapod - Optimal Geometry}
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\hypersetup{
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pdfauthor={Dehaeze Thomas},
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pdftitle={Nano Hexapod - Optimal Geometry},
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pdfkeywords={},
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pdfsubject={},
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pdfcreator={Emacs 29.4 (Org mode 9.6)},
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pdflang={English}}
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\usepackage{biblatex}
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\begin{document}
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\maketitle
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\tableofcontents
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\clearpage
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\begin{itemize}
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\item In the conceptual design phase, the geometry of the Stewart platform was chosen arbitrarily and not optimized
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\item In the detail design phase, we want to see if the geometry can be optimized to improve the overall performances
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\item Optimization criteria: mobility, stiffness, decoupling between the struts for decentralized control, dynamical decoupling in the cartesian frame
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\end{itemize}
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Outline:
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\begin{itemize}
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\item Review of Stewart platform (Section \ref{sec:detail_kinematics_stewart_review})
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Geometry, Actuators, Sensors, Joints
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\item Effect of geometry on the Stewart platform characteristics (Section \ref{sec:detail_kinematics_geometry})
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\item Cubic configuration: special architecture that received many attention in the literature. We want to see the special properties of this architecture and if this can be applied for the nano hexapod (Section \ref{sec:detail_kinematics_cubic})
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\item Presentation of the obtained geometry for the nano hexapod (Section \ref{sec:detail_kinematics_nano_hexapod})
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\end{itemize}
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\chapter{Review of Stewart platforms}
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\label{sec:detail_kinematics_stewart_review}
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\begin{itemize}
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\item As was explained in the conceptual phase, Stewart platform have the following key elements:
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\begin{itemize}
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\item Two plates connected by six struts
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\item Each strut is composed of:
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\begin{itemize}
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\item a flexible joint at each end
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\item an actuator
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\item one or several sensors
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\end{itemize}
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\end{itemize}
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\item The exact geometry (i.e. position of joints and orientation of the struts) can be chosen freely depending on the application.
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\item This results in many different designs found in the literature.
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\item The focus is here made on Stewart platforms for nano-positioning and vibration control.
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Long stroke stewart platforms are not considered here as their design impose other challenges.
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Some Stewart platforms found in the literature are listed in Table \ref{tab:detail_kinematics_stewart_review}
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\item All presented Stewart platforms are using flexible joints, as it is a prerequisites for nano-positioning capabilities.
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\item Most of stewart platforms are using voice coil actuators or piezoelectric actuators.
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The actuators used for the Stewart platform will be chosen in the next section.
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\item Depending on the application, various sensors are integrated in the struts or on the plates such as force sensors, inertial sensors or relative displacement sensors.
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The choice of sensor for the nano-hexapod will be described in the next section.
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\item Flexible joints can also have various implementations. This will be discussed in the next section.
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\item There are two main categories of Stewart platform geometry:
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\begin{itemize}
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\item Cubic architecture (Figure \ref{fig:detail_kinematics_stewart_examples_cubic}).
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Struts are positioned along 6 sides of a cubic (and are therefore orthogonal to each other).
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Such specific architecture has some special properties that will be studied in Section \ref{sec:detail_kinematics_cubic}.
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\item Non-cubic architecture (Figure \ref{fig:detail_kinematics_stewart_examples_non_cubic})
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The orientation of the struts and position of the joints are chosen based on performances criteria.
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Some of which are presented in Section \ref{sec:detail_kinematics_geometry}
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\end{itemize}
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\end{itemize}
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\begin{figure}[htbp]
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\begin{subfigure}{0.48\textwidth}
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\begin{center}
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\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_jpl.jpg}
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\end{center}
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\subcaption{\label{fig:detail_kinematics_jpl}California Institute of Technology - USA}
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\end{subfigure}
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\begin{subfigure}{0.48\textwidth}
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\begin{center}
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\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_uw_gsp.jpg}
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\end{center}
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\subcaption{\label{fig:detail_kinematics_uw_gsp}University of Wyoming - USA}
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\end{subfigure}
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\bigskip
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\begin{subfigure}{0.53\textwidth}
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\begin{center}
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\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_ulb_pz.jpg}
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\end{center}
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\subcaption{\label{fig:detail_kinematics_ulb_pz}ULB - Belgium}
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\end{subfigure}
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\begin{subfigure}{0.43\textwidth}
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\begin{center}
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\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_uqp.jpg}
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\end{center}
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\subcaption{\label{fig:detail_kinematics_uqp}Naval Postgraduate School - USA}
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\end{subfigure}
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\caption{\label{fig:detail_kinematics_stewart_examples_cubic}Some examples of developped Stewart platform with Cubic geometry. (\subref{fig:detail_kinematics_jpl}), (\subref{fig:detail_kinematics_uw_gsp}), (\subref{fig:detail_kinematics_ulb_pz}), (\subref{fig:detail_kinematics_uqp})}
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\end{figure}
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\begin{figure}[htbp]
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\begin{subfigure}{0.48\textwidth}
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\begin{center}
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\includegraphics[scale=1,height=5cm]{figs/detail_kinematics_pph.jpg}
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\end{center}
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\subcaption{\label{fig:detail_kinematics_pph}Naval Postgraduate School - USA}
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\end{subfigure}
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\begin{subfigure}{0.48\textwidth}
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\begin{center}
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\includegraphics[scale=1,height=5cm]{figs/detail_kinematics_zhang11.jpg}
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\end{center}
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\subcaption{\label{fig:detail_kinematics_zhang11}Beihang University - China}
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\end{subfigure}
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\bigskip
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\begin{subfigure}{0.43\textwidth}
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\begin{center}
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\includegraphics[scale=1,height=5cm]{figs/detail_kinematics_yang19.jpg}
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\end{center}
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\subcaption{\label{fig:detail_kinematics_yang19}Nanjing University - China}
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\end{subfigure}
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\begin{subfigure}{0.53\textwidth}
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\begin{center}
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\includegraphics[scale=1,height=5cm]{figs/detail_kinematics_naves.jpg}
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\end{center}
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\subcaption{\label{fig:detail_kinematics_naves}University of Twente - Netherlands}
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\end{subfigure}
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\caption{\label{fig:detail_kinematics_stewart_examples_non_cubic}Some examples of developped Stewart platform with non-cubic geometry. (\subref{fig:detail_kinematics_pph}), (\subref{fig:detail_kinematics_zhang11}), (\subref{fig:detail_kinematics_yang19}), (\subref{fig:detail_kinematics_naves})}
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\end{figure}
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\begin{table}[htbp]
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\caption{\label{tab:detail_kinematics_stewart_review}Examples of Stewart platform developed. When not specifically indicated, sensors are included in the struts. All presented Stewart platforms are using flexible joints. The table is ordered by appearance in the literature}
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\centering
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\scriptsize
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\begin{tabularx}{\linewidth}{llllX}
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\toprule
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& \textbf{Geometry} & \textbf{Actuators} & \textbf{Sensors} & \textbf{Reference}\\
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\midrule
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& Cubic & Magnetostrictive & Force, Accelerometers & \cite{geng93_six_degree_of_freed_activ,geng94_six_degree_of_freed_activ,geng95_intel_contr_system_multip_degree}\\
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Figure \ref{fig:detail_kinematics_jpl} & Cubic & Voice Coil (0.5 mm) & Force & \cite{spanos95_soft_activ_vibrat_isolat,rahman98_multiax}\\
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& Cubic & Voice Coil (10 mm) & Force, LVDT, Geophones & \cite{thayer98_stewar,thayer02_six_axis_vibrat_isolat_system,hauge04_sensor_contr_space_based_six}\\
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Figure \ref{fig:detail_kinematics_uw_gsp} & Cubic & Voice Coil & Force & \cite{mcinroy99_dynam,mcinroy99_precis_fault_toler_point_using_stewar_platf,mcinroy00_desig_contr_flexur_joint_hexap,li01_simul_vibrat_isolat_point_contr,jafari03_orthog_gough_stewar_platf_microm}\\
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& Cubic & Piezoelectric (\(25\,\mu m\)) & Force & \cite{defendini00_techn}\\
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Figure \ref{fig:detail_kinematics_ulb_pz} & Cubic & APA (\(50\,\mu m\)) & Force & \cite{abu02_stiff_soft_stewar_platf_activ}\\
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Figure \ref{fig:detail_kinematics_pph} & Non-Cubic & Voice Coil & Accelerometers & \cite{chen03_payload_point_activ_vibrat_isolat}\\
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& Cubic & Voice Coil & Force & \cite{hanieh03_activ_stewar,preumont07_six_axis_singl_stage_activ}\\
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Figure \ref{fig:detail_kinematics_uqp} & Cubic & Piezoelectric (\(50\,\mu m\)) & Geophone & \cite{agrawal04_algor_activ_vibrat_isolat_spacec}\\
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& Non-Cubic & Piezoelectric (\(16\,\mu m\)) & Eddy Current & \cite{furutani04_nanom_cuttin_machin_using_stewar}\\
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& Cubic & Piezoelectric (\(120\,\mu m\)) & (External) Capacitive & \cite{ting06_desig_stewar_nanos_platf,ting13_compos_contr_desig_stewar_nanos_platf}\\
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& Non-Cubic & Piezoelectric (\(160\,\mu m\)) & (External) Capacitive & \cite{ting07_measur_calib_stewar_microm_system}\\
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Figure \ref{fig:detail_kinematics_zhang11} & Non-cubic & Magnetostrictive & Accelerometer & \cite{zhang11_six_dof}\\
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& Non-Cubic & Piezoelectric & Strain Gauge & \cite{du14_piezo_actuat_high_precis_flexib}\\
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& Cubic & Voice Coil & Accelerometer & \cite{chi15_desig_exper_study_vcm_based,tang18_decen_vibrat_contr_voice_coil,jiao18_dynam_model_exper_analy_stewar}\\
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& Cubic & Piezoelectric & Force & \cite{wang16_inves_activ_vibrat_isolat_stewar}\\
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& Almost cubic & Voice Coil & Force, Accelerometer & \cite{beijen18_self_tunin_mimo_distur_feedf,tjepkema12_activ_ph}\\
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Figure \ref{fig:detail_kinematics_yang19} & Almost cubic & Piezoelectric & Force, Strain gauge & \cite{yang19_dynam_model_decoup_contr_flexib}\\
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Figure \ref{fig:detail_kinematics_naves} & Non-Cubic & 3-phase rotary motor & Rotary Encoder & \cite{naves20_desig,naves20_t_flex}\\
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\bottomrule
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\end{tabularx}
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\end{table}
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Conclusion:
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\begin{itemize}
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\item Various Stewart platform designs:
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\begin{itemize}
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\item geometry, sizes, orientation of struts
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\item Lot's have a ``cubic'' architecture that will be discussed in Section \ref{sec:detail_kinematics_cubic}
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\item actuator types
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\item various sensors
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\item flexible joints
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\end{itemize}
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\item The effect of geometry on the properties of the Stewart platform is studied in section \ref{sec:detail_kinematics_geometry}
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\item It is determined what is the optimal geometry for the NASS
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\end{itemize}
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\chapter{Effect of geometry on Stewart platform properties}
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\label{sec:detail_kinematics_geometry}
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\begin{itemize}
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\item As was shown during the conceptual phase, the geometry of the Stewart platform influences:
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\begin{itemize}
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\item the stiffness and compliance properties
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\item the mobility or workspace
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\item the force authority
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\item the dynamics of the manipulator
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\end{itemize}
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\item It is therefore important to understand how the geometry impact these properties, and to be able to optimize the geometry for a specific application.
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\end{itemize}
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One important tool to study this is the Jacobian matrix which depends on the \(\bm{b}_i\) (join position w.r.t top platform) and \(\hat{\bm{s}}_i\) (orientation of struts).
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The choice of frames (\(\{A\}\) and \(\{B\}\)), independently of the physical Stewart platform geometry, impacts the obtained kinematics and stiffness matrix, as it is defined for forces and motion evaluated at the chosen frame.
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\section{Platform Mobility / Workspace}
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The mobility of the Stewart platform (or any manipulator) is here defined as the range of motion that it can perform.
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It corresponds to the set of possible pose (i.e. combined translation and rotation) of frame \{B\} with respect to frame \{A\}.
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It is therefore a six dimensional property which is difficult to represent.
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Depending on the applications, only the translation mobility (i.e. fixed orientation workspace) or the rotation mobility may be represented.
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This is equivalent as to project the six dimensional value into a 3 dimensional space, easier to represent.
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Mobility of parallel manipulators are inherently difficult to study as the translational and orientation workspace are coupled \cite{merlet02_still}.
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Things are getting much more simpler when considering small motions as the Jacobian matrix can be considered constant and the equations are linear.
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As was shown during the conceptual phase, for small displacements, the Jacobian matrix can be used to link the strut motion to the motion of frame B with respect to A through equation \eqref{eq:detail_kinematics_jacobian}.
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\begin{equation}\label{eq:detail_kinematics_jacobian}
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\begin{bmatrix} \delta l_1 \\ \delta l_2 \\ \delta l_3 \\ \delta l_4 \\ \delta l_5 \\ \delta l_6 \end{bmatrix} = \begin{bmatrix}
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{{}^A\hat{\bm{s}}_1}^T & ({}^A\bm{b}_1 \times {}^A\hat{\bm{s}}_1)^T \\
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{{}^A\hat{\bm{s}}_2}^T & ({}^A\bm{b}_2 \times {}^A\hat{\bm{s}}_2)^T \\
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{{}^A\hat{\bm{s}}_3}^T & ({}^A\bm{b}_3 \times {}^A\hat{\bm{s}}_3)^T \\
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{{}^A\hat{\bm{s}}_4}^T & ({}^A\bm{b}_4 \times {}^A\hat{\bm{s}}_4)^T \\
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{{}^A\hat{\bm{s}}_5}^T & ({}^A\bm{b}_5 \times {}^A\hat{\bm{s}}_5)^T \\
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{{}^A\hat{\bm{s}}_6}^T & ({}^A\bm{b}_6 \times {}^A\hat{\bm{s}}_6)^T
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\end{bmatrix} \begin{bmatrix} \delta x \\ \delta y \\ \delta z \\ \delta \theta_x \\ \delta \theta_y \\ \delta \theta_z \end{bmatrix}
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\end{equation}
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Therefore, the mobility of the Stewart platform (set of \([\delta x\ \delta y\ \delta z\ \delta \theta_x\ \delta \theta_y\ \delta \theta_z]\)) depends on:
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\begin{itemize}
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\item the stroke of each strut
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\item the geometry of the Stewart platform (embodied in the Jacobian matrix)
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\end{itemize}
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More specifically:
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\begin{itemize}
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\item the XYZ mobility only depends on the si (orientation of struts)
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\item the mobility in rotation depends on bi (position of top joints)
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\end{itemize}
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\paragraph{Mobility in translation}
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Here, for simplicity, only translations are first considered (i.e. fixed orientation of the Stewart platform):
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\begin{itemize}
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\item Let's consider a general Stewart platform geometry shown in Figure \ref{fig:detail_kinematics_mobility_trans_arch}.
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\item In the general case: the translational mobility can be represented by a 3D shape with 12 faces (each actuator limits the stroke along its orientation in positive and negative directions).
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The faces are therefore perpendicular to the strut direction.
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The obtained mobility for the considered stewart platform geometry is shown in Figure \ref{fig:detail_kinematics_mobility_trans_result}.
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In reality, the workspace boundaries are portion of spheres, but they are well approximated by flat surfaces for short stroke hexapods
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\item Considering an actuator stroke of \(\pm d\), the mobile platform can be translated in any direction with a stroke of \(d\)
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This means that a sphere with radius \(d\) is contained in the general shape as illustrated in Figure \ref{fig:detail_kinematics_mobility_trans_result}.
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The sphere will touch the shape along six lines defined by the strut axes.
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\end{itemize}
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\begin{figure}[htbp]
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\begin{subfigure}{0.48\textwidth}
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\begin{center}
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\includegraphics[scale=1,scale=1]{figs/detail_kinematics_mobility_trans_arch.png}
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\end{center}
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\subcaption{\label{fig:detail_kinematics_mobility_trans_arch}Stewart platform geometry}
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\end{subfigure}
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\begin{subfigure}{0.48\textwidth}
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\begin{center}
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\includegraphics[scale=1,scale=1]{figs/detail_kinematics_mobility_trans_result.png}
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\end{center}
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\subcaption{\label{fig:detail_kinematics_mobility_trans_result}Translational mobility}
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\end{subfigure}
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\caption{\label{fig:detail_kinematics_mobility_trans}Example of one Stewart platform (\subref{fig:detail_kinematics_mobility_trans_arch}) and associated translational mobility (\subref{fig:detail_kinematics_mobility_trans_result})}
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\end{figure}
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To better understand how the geometry of the Stewart platform impacts the translational mobility, two configurations are compared:
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\begin{itemize}
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\item Struts oriented horizontally (Figure \ref{fig:detail_kinematics_stewart_mobility_vert_struts}).
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This leads to having more stroke in the horizontal direction and less stroke in the vertical direction (Figure \ref{fig:detail_kinematics_mobility_translation_strut_orientation}).
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\item Struts oriented vertically (Figure \ref{fig:detail_kinematics_stewart_mobility_hori_struts}).
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More stroke in vertical direction
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\end{itemize}
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It can be counter intuitive to have less stroke in the direction of the struts.
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This is because the struts are forming a lever mechanism that amplifies the motion.
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The amplification factor increases when the struts have an high angle with the direction and motion and is equal to one when it is aligned with the direction of motion.
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\begin{figure}[htbp]
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\begin{subfigure}{0.25\textwidth}
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\begin{center}
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\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_stewart_mobility_vert_struts.png}
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\end{center}
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\subcaption{\label{fig:detail_kinematics_stewart_mobility_vert_struts}Vertical struts}
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\end{subfigure}
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\begin{subfigure}{0.25\textwidth}
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\begin{center}
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\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_stewart_mobility_hori_struts.png}
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\end{center}
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\subcaption{\label{fig:detail_kinematics_stewart_mobility_hori_struts}Horizontal struts}
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\end{subfigure}
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\begin{subfigure}{0.46\textwidth}
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\begin{center}
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\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_mobility_translation_strut_orientation.png}
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\end{center}
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\subcaption{\label{fig:detail_kinematics_mobility_translation_strut_orientation}Translational mobility}
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\end{subfigure}
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\caption{\label{fig:detail_kinematics_stewart_mobility_examples}Effect of strut orientation on the obtained mobility in translation. Two Stewart platform geometry are considered: struts oriented vertically (\subref{fig:detail_kinematics_stewart_mobility_vert_struts}) and struts oriented vertically (\subref{fig:detail_kinematics_stewart_mobility_hori_struts}). Obtained mobility for both geometry are shown in (\subref{fig:detail_kinematics_mobility_translation_strut_orientation}).}
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\end{figure}
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\paragraph{Mobility in rotation}
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As shown by equation \eqref{eq:detail_kinematics_jacobian}, the rotational mobility depends both on the orientation of the struts and on the location of the top joints.
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Similarly to the translational case, to increase the rotational mobility in one direction, it is advantageous to have the struts more perpendicular to the rotational direction.
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For instance, having the struts more vertical (Figure \ref{fig:detail_kinematics_stewart_mobility_vert_struts}) gives less rotational stroke along the vertical direction than having the struts oriented more horizontally (Figure \ref{fig:detail_kinematics_stewart_mobility_hori_struts}).
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Two cases are considered with same strut orientation but with different top joints positions:
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\begin{itemize}
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\item struts close to each other (Figure \ref{fig:detail_kinematics_stewart_mobility_close_struts})
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\item struts further apart (Figure \ref{fig:detail_kinematics_stewart_mobility_space_struts})
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\end{itemize}
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The mobility for pure rotations are compared in Figure \ref{fig:detail_kinematics_mobility_angle_strut_distance}.
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Note that the same strut stroke are considered in both cases to evaluate the mobility.
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Having struts further apart decreases the ``level arm'' and therefore the rotational mobility is reduced.
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For rotations and translations, having more mobility also means increasing the effect of actuator noise on the considering degree of freedom.
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Somehow, the level arm is increased, so any strut vibration gets amplified.
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Therefore, the designed Stewart platform should just have the necessary mobility.
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\begin{figure}[htbp]
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\begin{subfigure}{0.25\textwidth}
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\begin{center}
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\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_stewart_mobility_close_struts.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_stewart_mobility_close_struts}Struts close together}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.25\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_stewart_mobility_space_struts.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_stewart_mobility_space_struts}Struts far apart}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.46\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_mobility_angle_strut_distance.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_mobility_angle_strut_distance}Rotational mobility}
|
|
\end{subfigure}
|
|
\caption{\label{fig:detail_kinematics_stewart_mobility_examples}Effect of strut position on the obtained mobility in rotation. Two Stewart platform geometry are considered: struts close to each other (\subref{fig:detail_kinematics_stewart_mobility_close_struts}) and struts further appart (\subref{fig:detail_kinematics_stewart_mobility_space_struts}). Obtained mobility for both geometry are shown in (\subref{fig:detail_kinematics_mobility_angle_strut_distance}).}
|
|
\end{figure}
|
|
|
|
\paragraph{Combined translations and rotations}
|
|
|
|
It is possible to consider combined translations and rotations.
|
|
Displaying such mobility is more complex.
|
|
It will be used for the nano-hexapod to verify that the obtained design has the necessary mobility.
|
|
|
|
For a fixed geometry and a wanted mobility (combined translations and rotations), it is possible to estimate the required minimum actuator stroke.
|
|
It will be done in Section \ref{sec:detail_kinematics_nano_hexapod} to estimate the required actuator stroke for the nano-hexapod geometry.
|
|
|
|
\section{Stiffness}
|
|
Stiffness matrix:
|
|
\begin{itemize}
|
|
\item defines how the nano-hexapod deforms (frame \(\{B\}\) with respect to frame \(\{A\}\)) due to static forces/torques applied on \(\{B\}\).
|
|
\item It depends on the Jacobian matrix (i.e. the geometry) and the strut axial stiffness \eqref{eq:detail_kinematics_stiffness_matrix}
|
|
\item The contribution of joints stiffness is here not considered \cite{mcinroy00_desig_contr_flexur_joint_hexap,mcinroy02_model_desig_flexur_joint_stewar}
|
|
\end{itemize}
|
|
|
|
\begin{equation}\label{eq:detail_kinematics_stiffness_matrix}
|
|
\bm{K} = \bm{J}^T \bm{\mathcal{K}} \bm{J}
|
|
\end{equation}
|
|
|
|
It is assumed that the stiffness of all strut is the same: \(\bm{\mathcal{K}} = k \cdot \mathbf{I}_6\).
|
|
Obtained stiffness matrix linearly depends on the strut stiffness \(k\), and is structured as shown in \eqref{eq:detail_kinematics_stiffness_matrix_simplified}.
|
|
|
|
\begin{equation}\label{eq:detail_kinematics_stiffness_matrix_simplified}
|
|
\bm{K} = k \bm{J}^T \bm{J} =
|
|
k \left[
|
|
\begin{array}{c|c}
|
|
\Sigma_{i = 0}^{6} \hat{\bm{s}}_i \cdot \hat{\bm{s}}_i^T & \Sigma_{i = 0}^{6} \bm{\hat{s}}_i \cdot ({}^A\bm{b}_i \times {}^A\hat{\bm{s}}_i)^T \\
|
|
\hline
|
|
\Sigma_{i = 0}^{6} ({}^A\bm{b}_i \times {}^A\hat{\bm{s}}_i) \cdot \hat{\bm{s}}_i^T & \Sigma_{i = 0}^{6} ({}^A\bm{b}_i \times {}^A\hat{\bm{s}}_i) \cdot ({}^A\bm{b}_i \times {}^A\hat{\bm{s}}_i)^T\\
|
|
\end{array}
|
|
\right]
|
|
\end{equation}
|
|
|
|
\paragraph{Translation Stiffness}
|
|
|
|
As shown by \eqref{eq:detail_kinematics_stiffness_matrix_simplified}, the translation stiffnesses (the 3x3 top left terms of the stiffness matrix):
|
|
\begin{itemize}
|
|
\item Only depends on the orientation of the struts and not their location: \(\hat{\bm{s}}_i \cdot \hat{\bm{s}}_i^T\)
|
|
\item Extreme case: all struts are vertical \(s_i = [0,\ 0,\ 1]\) => vertical stiffness of \(6 k\), but null stiffness in X and Y directions
|
|
\item If two struts along X, two struts along Y, and two struts along Z => \(\hat{\bm{s}}_i \cdot \hat{\bm{s}}_i^T = 2 \bm{I}_3\)
|
|
Stiffness is well distributed along directions.
|
|
This corresponds to the cubic architecture presented in Section \ref{sec:detail_kinematics_cubic}.
|
|
\end{itemize}
|
|
|
|
If struts more vertical (Figure \ref{fig:detail_kinematics_stewart_mobility_vert_struts}):
|
|
\begin{itemize}
|
|
\item increase vertical stiffness
|
|
\item decrease horizontal stiffness
|
|
\item increase Rx,Ry stiffness
|
|
\item decrease Rz stiffness
|
|
\end{itemize}
|
|
|
|
Opposite conclusions if struts are not horizontal (Figure \ref{fig:detail_kinematics_stewart_mobility_hori_struts}).
|
|
|
|
\paragraph{Rotational Stiffness}
|
|
|
|
The rotational stiffnesses depends both on the orientation of the struts and on the location of the top joints (with respect to the considered center of rotation, i.e. the location of frame B).
|
|
|
|
Same orientation but increased distances (bi) by a factor 2 => rotational stiffness increased by factor 4.
|
|
Compact stewart platform of Figure \ref{fig:detail_kinematics_stewart_mobility_close_struts} as therefore less rotational stiffness than the Stewart platform of Figure \ref{fig:detail_kinematics_stewart_mobility_space_struts}.
|
|
|
|
\paragraph{Diagonal Stiffness Matrix}
|
|
|
|
Having the stiffness matrix \(\bm{K}\) diagonal can be beneficial for control purposes as it would make the plant in the cartesian frame decoupled at low frequency.
|
|
This depends on the geometry and on the chosen \{B\} frame.
|
|
For specific geometry and chose of B frame, it is possible to have a diagonal K matrix.
|
|
|
|
This will be discussed in Section \ref{ssec:detail_kinematics_cubic_static}.
|
|
|
|
\section{Dynamical properties}
|
|
\paragraph{In the Cartesian Frame}
|
|
|
|
Dynamical equations (both in the cartesian frame and in the frame of the struts) for the Stewart platform were derived during the conceptual phase with simplifying assumptions (massless struts and perfect joints).
|
|
The dynamics depends both on the geometry (Jacobian matrix) but also on the payload being placed on top of the platform.
|
|
|
|
Under very specific conditions, the equations of motion in the Cartesian frame \eqref{eq:nhexa_transfer_function_cart} can be decoupled.
|
|
These are studied in Section \ref{ssec:detail_kinematics_cubic_dynamic}.
|
|
|
|
\begin{equation}\label{eq:nhexa_transfer_function_cart}
|
|
\frac{{\mathcal{X}}}{\bm{\mathcal{F}}}(s) = ( \bm{M} s^2 + \bm{J}^{T} \bm{\mathcal{C}} \bm{J} s + \bm{J}^{T} \bm{\mathcal{K}} \bm{J} )^{-1}
|
|
\end{equation}
|
|
|
|
\paragraph{In the frame of the Struts}
|
|
|
|
In the frame of the struts, the equations of motion \eqref{eq:nhexa_transfer_function_struts} are well decoupled at low frequency.
|
|
This is why most of Stewart platforms are controlled in the frame of the struts: bellow the resonance frequency, the system is decoupled and SISO control may be applied for each strut, independently of the payload being used.
|
|
|
|
\begin{equation}\label{eq:nhexa_transfer_function_struts}
|
|
\frac{\bm{\mathcal{L}}}{\bm{f}}(s) = ( \bm{J}^{-T} \bm{M} \bm{J}^{-1} s^2 + \bm{\mathcal{C}} + \bm{\mathcal{K}} )^{-1}
|
|
\end{equation}
|
|
|
|
Coupling between sensors (force sensors, relative position sensor, inertial sensors) in different struts may also be important for decentralized control.
|
|
In section \ref{ssec:detail_kinematics_decentralized_control}, it will be study if the Stewart platform geometry can be optimized to have lower coupling between the struts.
|
|
|
|
\section*{Conclusion}
|
|
The effects of two changes in the manipulator's geometry, namely the position and orientation of the legs, are summarized in Table \ref{tab:detail_kinematics_geometry}.
|
|
These results could have been easily deduced based on some mechanical principles, but thanks to the kinematic analysis, they can be quantified.
|
|
|
|
These trade-offs give some guidelines when choosing the Stewart platform geometry.
|
|
|
|
\begin{table}[htbp]
|
|
\caption{\label{tab:detail_kinematics_geometry}Effect of a change in geometry on the manipulator's stiffness, force authority and stroke}
|
|
\centering
|
|
\small
|
|
\begin{tabularx}{0.9\linewidth}{Xcc}
|
|
\toprule
|
|
\textbf{Struts} & \textbf{Vertically Oriented} & \textbf{Increased separation}\\
|
|
\midrule
|
|
Vertical stiffness & \(\nearrow\) & \(=\)\\
|
|
Horizontal stiffness & \(\searrow\) & \(=\)\\
|
|
Vertical rotation stiffness & \(\searrow\) & \(\nearrow\)\\
|
|
Horizontal rotation stiffness & \(\nearrow\) & \(\nearrow\)\\
|
|
\midrule
|
|
Vertical stroke & \(\searrow\) & \(=\)\\
|
|
Horizontal stroke & \(\nearrow\) & \(=\)\\
|
|
Vertical rotation stroke & \(\nearrow\) & \(\searrow\)\\
|
|
Horizontal rotation stroke & \(\searrow\) & \(\searrow\)\\
|
|
\bottomrule
|
|
\end{tabularx}
|
|
\end{table}
|
|
|
|
\chapter{The Cubic Architecture}
|
|
\label{sec:detail_kinematics_cubic}
|
|
The Cubic configuration for the Stewart platform was first proposed in \cite{geng94_six_degree_of_freed_activ}.
|
|
This configuration is quite specific in the sense that the active struts are arranged in a mutually orthogonal configuration connecting the corners of a cube, as shown in Figure \ref{fig:detail_kinematics_cubic_architecture_examples}.
|
|
|
|
Typically, the struts have similar size than the cube's edge, as shown in Figure \ref{fig:detail_kinematics_cubic_architecture_example}.
|
|
Practical implementations of such configuration are shown in Figures \ref{fig:detail_kinematics_jpl}, \ref{fig:detail_kinematics_uw_gsp} and \ref{fig:detail_kinematics_uqp}.
|
|
|
|
It is also possible to have the struts length smaller than the cube's edge (Figure \ref{fig:detail_kinematics_cubic_architecture_example_small}).
|
|
An example of such Stewart platform is shown in Figure \ref{fig:detail_kinematics_ulb_pz}.
|
|
|
|
\begin{figure}[htbp]
|
|
\begin{subfigure}{0.49\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,scale=1]{figs/detail_kinematics_cubic_architecture_example.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_architecture_example}sub caption a}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.49\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,scale=1]{figs/detail_kinematics_cubic_architecture_example_small.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_architecture_example_small}sub caption b}
|
|
\end{subfigure}
|
|
\caption{\label{fig:detail_kinematics_cubic_architecture_examples}Typical Stewart platform cubic architectures. (\subref{fig:detail_kinematics_cubic_architecture_example}) (\subref{fig:detail_kinematics_cubic_architecture_example_small})}
|
|
\end{figure}
|
|
|
|
|
|
A number of properties are attributed to the cubic configuration, which have made this configuration widely popular (\cite{geng94_six_degree_of_freed_activ,preumont07_six_axis_singl_stage_activ,jafari03_orthog_gough_stewar_platf_microm}):
|
|
\begin{itemize}
|
|
\item Simple kinematics relationships and dynamical analysis \cite{geng94_six_degree_of_freed_activ}
|
|
\item Uniform stiffness in all directions \cite{hanieh03_activ_stewar}
|
|
\item Uniform mobility \cite[, chapt.8.5.2]{preumont18_vibrat_contr_activ_struc_fourt_edition}
|
|
\item Minimization of the cross coupling between actuators and sensors in other struts \cite{preumont07_six_axis_singl_stage_activ}.
|
|
This is attributed to the fact that the struts are orthogonal to each other.
|
|
This is said to facilitate collocated sensor-actuator control system design, i.e. the implementation of decentralized control \cite{geng94_six_degree_of_freed_activ,thayer02_six_axis_vibrat_isolat_system}.
|
|
\end{itemize}
|
|
|
|
|
|
Such properties are studied to see if they are useful for the nano-hexapod and the associated conditions:
|
|
\begin{itemize}
|
|
\item The mobility and stiffness properties of the cubic configuration are studied in Section \ref{ssec:detail_kinematics_cubic_static}.
|
|
\item Dynamical decoupling is studied in Section \ref{ssec:detail_kinematics_cubic_dynamic}
|
|
\item Decentralized control, important for the NASS, is studied in Section \ref{ssec:detail_kinematics_decentralized_control}
|
|
\end{itemize}
|
|
|
|
As the cubic architecture has some restrictions on the geometry, alternative designs are proposed in Section \ref{ssec:detail_kinematics_cubic_design}.
|
|
|
|
The goal is to determine if the cubic architecture is interesting for the nano-hexapod.
|
|
\section{Static Properties}
|
|
\label{ssec:detail_kinematics_cubic_static}
|
|
\paragraph{Stiffness matrix for the Cubic architecture}
|
|
Consider the cubic architecture shown in Figure \ref{fig:detail_kinematics_cubic_schematic_full}.
|
|
The unit vectors corresponding to the edges of the cube are described by \eqref{eq:detail_kinematics_cubic_s}.
|
|
|
|
\begin{equation}\label{eq:detail_kinematics_cubic_s}
|
|
\hat{\bm{s}}_1 = \begin{bmatrix} \sqrt{2}/\sqrt{3} \\ 0 \\ 1/\sqrt{3} \end{bmatrix} \quad
|
|
\hat{\bm{s}}_2 = \begin{bmatrix} -1/\sqrt{6} \\ -1/\sqrt{2} \\ 1/\sqrt{3} \end{bmatrix} \quad
|
|
\hat{\bm{s}}_3 = \begin{bmatrix} -1/\sqrt{6} \\ 1/\sqrt{2} \\ 1/\sqrt{3} \end{bmatrix} \quad
|
|
\hat{\bm{s}}_4 = \begin{bmatrix} \sqrt{2}/\sqrt{3} \\ 0 \\ 1/\sqrt{3} \end{bmatrix} \quad
|
|
\hat{\bm{s}}_5 = \begin{bmatrix} -1/\sqrt{6} \\ -1/\sqrt{2} \\ 1/\sqrt{3} \end{bmatrix} \quad
|
|
\hat{\bm{s}}_6 = \begin{bmatrix} -1/\sqrt{6} \\ 1/\sqrt{2} \\ 1/\sqrt{3} \end{bmatrix}
|
|
\end{equation}
|
|
|
|
Coordinates of the cube's vertices relevant for the top joints, expressed with respect to the cube's center \eqref{eq:detail_kinematics_cubic_vertices}.
|
|
|
|
\begin{equation}\label{eq:detail_kinematics_cubic_vertices}
|
|
\tilde{\bm{b}}_1 = \tilde{\bm{b}}_2 = H_c \begin{bmatrix} \frac{1}{\sqrt{2}} \\ \frac{-\sqrt{3}}{\sqrt{2}} \\ \frac{1}{2} \end{bmatrix}, \quad
|
|
\tilde{\bm{b}}_3 = \tilde{\bm{b}}_4 = H_c \begin{bmatrix} \frac{1}{\sqrt{2}} \\ \frac{ \sqrt{3}}{\sqrt{2}} \\ \frac{1}{2} \end{bmatrix}, \quad
|
|
\tilde{\bm{b}}_5 = \tilde{\bm{b}}_6 = H_c \begin{bmatrix} \frac{-2}{\sqrt{2}} \\ 0 \\ \frac{1}{2} \end{bmatrix}
|
|
\end{equation}
|
|
|
|
\begin{figure}[htbp]
|
|
\begin{subfigure}{0.48\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,scale=0.9]{figs/detail_kinematics_cubic_schematic_full.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_schematic_full}Full cube}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.48\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,scale=0.9]{figs/detail_kinematics_cubic_schematic.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_schematic}Cube's portion}
|
|
\end{subfigure}
|
|
\caption{\label{fig:detail_kinematics_cubic_schematic_cases}Cubic architecture. Struts are represented un blue. The cube's center by a black dot. The Struts can match the cube's edges (\subref{fig:detail_kinematics_cubic_schematic_full}) or just take a portion of the edge (\subref{fig:detail_kinematics_cubic_schematic})}
|
|
\end{figure}
|
|
|
|
In that case (top joints at the cube's vertices), a diagonal stiffness matrix is obtained \eqref{eq:detail_kinematics_cubic_stiffness}.
|
|
Translation stiffness is twice the stiffness of the struts, and rotational stiffness is proportional to the square of the cube's size \(H_c\).
|
|
|
|
\begin{equation}\label{eq:detail_kinematics_cubic_stiffness}
|
|
\bm{K}_{\{B\} = \{C\}} = k \begin{bmatrix}
|
|
2 & 0 & 0 & 0 & 0 & 0 \\
|
|
0 & 2 & 0 & 0 & 0 & 0 \\
|
|
0 & 0 & 2 & 0 & 0 & 0 \\
|
|
0 & 0 & 0 & \frac{3}{2} H_c^2 & 0 & 0 \\
|
|
0 & 0 & 0 & 0 & \frac{3}{2} H_c^2 & 0 \\
|
|
0 & 0 & 0 & 0 & 0 & 6 H_c^2 \\
|
|
\end{bmatrix}
|
|
\end{equation}
|
|
|
|
But typically, the top joints are not placed at the cube's vertices but anywhere along the cube's edges (Figure \ref{fig:detail_kinematics_cubic_schematic}).
|
|
In that case, the location of the top joints can be expressed by \eqref{eq:detail_kinematics_cubic_edges}.
|
|
But the computed stiffness matrix is the same \eqref{eq:detail_kinematics_cubic_stiffness}.
|
|
|
|
\begin{equation}\label{eq:detail_kinematics_cubic_edges}
|
|
\bm{b}_i = \tilde{\bm{b}}_i + \alpha \hat{\bm{s}}_i
|
|
\end{equation}
|
|
|
|
The Stiffness matrix is therefore diagonal when the considered \{B\} frame is located at the center of the cube.
|
|
This corresponds to forces and torques applied on the top platform, but expressed at the center of the cube, and for translations and rotations of the top platform expressed with respect to the cube's center.
|
|
We may call this specific location (where the Stiffness matrix is diagonal) the ``Center of Stiffness'' (in analogy with the ``Center of Mass'' where the mass matrix is diagonal).
|
|
|
|
\paragraph{Effect of having frame \(\{B\}\) off-centered}
|
|
|
|
However, as soon as the location of the A and B frames are shifted from the cube's center, off diagonal elements in the stiffness matrix appear.
|
|
|
|
Let's consider here a vertical shift as shown in Figure \ref{fig:detail_kinematics_cubic_schematic}.
|
|
In that case, the stiffness matrix is \eqref{eq:detail_kinematics_cubic_stiffness_off_centered}.
|
|
Off diagonal elements are increasing with the height difference between the cube's center and the considered B frame.
|
|
|
|
\begin{equation}\label{eq:detail_kinematics_cubic_stiffness_off_centered}
|
|
\bm{K}_{\{B\} \neq \{C\}} = k \begin{bmatrix}
|
|
2 & 0 & 0 & 0 & -2 H & 0 \\
|
|
0 & 2 & 0 & 2 H & 0 & 0 \\
|
|
0 & 0 & 2 & 0 & 0 & 0 \\
|
|
0 & 2 H & 0 & \frac{3}{2} H_c^2 + 2 H^2 & 0 & 0 \\
|
|
-2 H & 0 & 0 & 0 & \frac{3}{2} H_c^2 + 2 H^2 & 0 \\
|
|
0 & 0 & 0 & 0 & 0 & 6 H_c^2 \\
|
|
\end{bmatrix}
|
|
\end{equation}
|
|
|
|
|
|
Such structure of the stiffness matrix is very typical with Stewart platform that have some symmetry, but not necessary only for cubic architectures.
|
|
|
|
Therefore, the stiffness of the cubic architecture is special only when considering a frame located at the center of the cube.
|
|
This is not very convenient, as in the vast majority of cases, the interesting frame (where motion are relevant and forces are applied) is located about the top platform.
|
|
|
|
Note that the cube's center needs not to be at the ``center'' of the Stewart platform.
|
|
This can lead to interesting architectures shown in Section \ref{ssec:detail_kinematics_cubic_design}.
|
|
|
|
\paragraph{Uniform Mobility}
|
|
|
|
The mobility in translation of the Stewart platform is studied with constant orientation.
|
|
Considering limited actuator stroke (i.e. elongation of each strut), the maximum XYZ position that can be reached can be estimated.
|
|
The obtained mobility in X,Y,Z directions for the Cubic architecture is shown in Figure \ref{fig:detail_kinematics_cubic_mobility_translations}.
|
|
\begin{itemize}
|
|
\item It corresponds to a cube, whose axis are aligned with the struts, and the length of the cube's edge is equal to the strut axial stroke.
|
|
\item We can say that the mobility in not uniform in the XYZ directions, but is uniform in the directions aligned with the cube's edges.
|
|
Claims of the cubic architecture having the property of having a translational mobility of a sphere is wrong \cite{mcinroy00_desig_contr_flexur_joint_hexap}.
|
|
\item Nevertheless, it can be said that the obtained mobility is somehow more uniform than other architecture, as the ones shown in Figure \ref{fig:detail_kinematics_mobility_trans}.
|
|
\item Note that the mobility in translation does not depend on the cube's size.
|
|
\end{itemize}
|
|
|
|
Also show mobility in Rx,Ry,Rz (Figure \ref{fig:detail_kinematics_cubic_mobility_rotations}):
|
|
\begin{itemize}
|
|
\item More mobility in Rx and Ry than in Rz
|
|
\item Mobility decreases with the size of the cube
|
|
\end{itemize}
|
|
|
|
\begin{figure}[htbp]
|
|
\begin{subfigure}{0.48\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,scale=1]{figs/detail_kinematics_cubic_mobility_translations.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_mobility_translations}Mobility in translation}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.48\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,scale=1]{figs/detail_kinematics_cubic_mobility_rotations.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_mobility_rotations}Mobility in rotation}
|
|
\end{subfigure}
|
|
\caption{\label{fig:detail_kinematics_cubic_mobility}Mobility of a Stewart platform with Cubic architecture. Both for translations (\subref{fig:detail_kinematics_cubic_mobility_translations}) and rotations (\subref{fig:detail_kinematics_cubic_mobility_rotations})}
|
|
\end{figure}
|
|
|
|
\section{Dynamical Decoupling}
|
|
\label{ssec:detail_kinematics_cubic_dynamic}
|
|
In this section, the dynamics of the platform in the cartesian frame is studied.
|
|
This corresponds to the transfer function from forces and torques \(\bm{\mathcal{F}}\) to translations and rotations \(\bm{\mathcal{X}}\) of the top platform.
|
|
If relative motion sensor are located in each strut (\(\bm{\mathcal{L}}\) is measured), the pose \(\bm{\mathcal{X}}\) is computed using the Jacobian matrix as shown in Figure \ref{fig:detail_kinematics_centralized_control}.
|
|
|
|
\begin{figure}[htbp]
|
|
\centering
|
|
\includegraphics[scale=1]{figs/detail_kinematics_centralized_control.png}
|
|
\caption{\label{fig:detail_kinematics_centralized_control}From Strut coordinate to Cartesian coordinate using the Jacobian matrix}
|
|
\end{figure}
|
|
|
|
We want to see if the Stewart platform has some special properties for control in the cartesian frame.
|
|
\paragraph{Low frequency and High frequency coupling}
|
|
|
|
As was derived during the conceptual design phase, the dynamics from \(\bm{\mathcal{F}}\) to \(\bm{\mathcal{X}}\) is described by \eqref{eq:detail_kinematics_transfer_function_cart}
|
|
|
|
\begin{equation}\label{eq:detail_kinematics_transfer_function_cart}
|
|
\frac{{\mathcal{X}}}{\bm{\mathcal{F}}}(s) = ( \bm{M} s^2 + \bm{J}^{T} \bm{\mathcal{C}} \bm{J} s + \bm{J}^{T} \bm{\mathcal{K}} \bm{J} )^{-1}
|
|
\end{equation}
|
|
|
|
|
|
At low frequency: the static behavior of the platform depends on the stiffness matrix \eqref{eq:detail_kinematics_transfer_function_cart_low_freq}.
|
|
In section \ref{ssec:detail_kinematics_cubic_static}, it was shown that for the cubic configuration, the stiffness matrix is diagonal if frame \(\{B\}\) is taken at the cube's center.
|
|
In that case, the ``cartesian'' plant is decoupled at low frequency.
|
|
|
|
\begin{equation}\label{eq:detail_kinematics_transfer_function_cart_low_freq}
|
|
\frac{{\mathcal{X}}}{\bm{\mathcal{F}}}(j \omega) \xrightarrow[\omega \to 0]{} \bm{K}^{-1}
|
|
\end{equation}
|
|
|
|
|
|
At high frequency, the behavior depends on the mass matrix (evaluated at frame B) \eqref{eq:detail_kinematics_transfer_function_high_freq}.
|
|
To have the mass matrix diagonal, the center of mass of the mobile parts needs to coincide with the B frame and the principal axes of inertia of the body also needs to coincide with the axis of the B frame.
|
|
|
|
\begin{equation}\label{eq:detail_kinematics_transfer_function_high_freq}
|
|
\frac{{\mathcal{X}}}{\bm{\mathcal{F}}}(j \omega) \xrightarrow[\omega \to \infty]{} - \omega^2 \bm{M}^{-1}
|
|
\end{equation}
|
|
|
|
To verify that,
|
|
\begin{itemize}
|
|
\item A cubic stewart platform is used with a cylindrical payload on top (Figure \ref{fig:detail_kinematics_cubic_payload})
|
|
\item The transfer functions from F to X are computed for two specific locations of the B frames:
|
|
\begin{itemize}
|
|
\item center of mass: coupled at low frequency due to non diagonal stiffness matrix (Figure \ref{fig:detail_kinematics_cubic_cart_coupling_com})
|
|
\item center of stiffness: coupled at high frequency due to non diagonal mass matrix (Figure \ref{fig:detail_kinematics_cubic_cart_coupling_cok})
|
|
\end{itemize}
|
|
\item In both cases, similar dynamics for a non-cubic stewart platform would be obtained and the cubic architecture does not show any clear advantage.
|
|
\end{itemize}
|
|
|
|
\begin{figure}[htbp]
|
|
\centering
|
|
\includegraphics[scale=1,width=0.6\linewidth]{figs/detail_kinematics_cubic_payload.png}
|
|
\caption{\label{fig:detail_kinematics_cubic_payload}Cubic stewart platform with top cylindrical payload}
|
|
\end{figure}
|
|
|
|
\begin{figure}[htbp]
|
|
\begin{subfigure}{0.48\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_cubic_cart_coupling_com.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_cart_coupling_com}$\{B\}$ at the center of mass}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.48\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_cubic_cart_coupling_cok.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_cart_coupling_cok}$\{B\}$ at the cube's center}
|
|
\end{subfigure}
|
|
\caption{\label{fig:detail_kinematics_cubic_cart_coupling}Transfer functions for a Cubic Stewart platform expressed in the Cartesian frame. Two locations of the \(\{B\}\) frame are considered: at the cube's center (\subref{fig:detail_kinematics_cubic_cart_coupling_cok}) and at the center of mass of the moving body (\subref{fig:detail_kinematics_cubic_cart_coupling_com}).}
|
|
\end{figure}
|
|
|
|
\paragraph{Payload's CoM at the cube's center}
|
|
|
|
It is natural to try to have the cube's center (center of stiffness) and the center of mass of the moving part coincide at the same location \cite{li01_simul_fault_vibrat_isolat_point}.
|
|
To do so, the payload is located below the top platform, such that the center of mass of the moving body is at the cube's center (Figure \ref{fig:detail_kinematics_cubic_centered_payload}).
|
|
|
|
This is what is physically done in \cite{mcinroy99_dynam,mcinroy99_precis_fault_toler_point_using_stewar_platf,mcinroy00_desig_contr_flexur_joint_hexap,li01_simul_vibrat_isolat_point_contr,jafari03_orthog_gough_stewar_platf_microm} (Figure \ref{fig:detail_kinematics_uw_gsp}).
|
|
|
|
The obtained dynamics is indeed well decoupled, thanks to the diagonal stiffness matrix and mass matrix at the same time.
|
|
|
|
The main issue with this is that usually we want the payload to be located above the top platform, as it is the case for the nano-hexapod.
|
|
Indeed, if a similar design than the one shown in Figure \ref{fig:detail_kinematics_cubic_centered_payload} was used, the x-ray beam will hit the different struts during the rotation of the spindle.
|
|
|
|
\begin{figure}[htbp]
|
|
\begin{subfigure}{0.49\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_cubic_centered_payload.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_centered_payload}Payload at the cube's center}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.49\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_cubic_cart_coupling_com_cok.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_cart_coupling_com_cok}Fully decoupled cartesian plant}
|
|
\end{subfigure}
|
|
\caption{\label{fig:detail_kinematics_cubic_com_cok}Cubic Stewart platform with payload at the cube's center (\subref{fig:detail_kinematics_cubic_centered_payload}). Obtained cartesian plant is fully decoupled (\subref{fig:detail_kinematics_cubic_cart_coupling_com_cok})}
|
|
\end{figure}
|
|
|
|
\paragraph{Conclusion}
|
|
|
|
Some conclusions can be drawn from the above analysis:
|
|
\begin{itemize}
|
|
\item Static Decoupling <=> Diagonal Stiffness matrix <=> \{A\} and \{B\} at the cube's center
|
|
Can also have static decoupling with non-cubic architecture, if there is some symmetry between the struts.
|
|
\item Dynamic Decoupling <=> Static Decoupling + CoM of mobile platform coincident with \{A\} and \{B\}.
|
|
This is very powerful, but requires to have the payload at the cube's center which is very restrictive and often not possible.
|
|
This is also not specific to the cubic architecture.
|
|
\item Same stiffness in XYZ, which can be interesting for some applications.
|
|
\end{itemize}
|
|
|
|
\section{Decentralized Control}
|
|
\label{ssec:detail_kinematics_decentralized_control}
|
|
This is reasonable to think that as the struts are orthogonal to each other for the cubic architecture, the coupling between the struts should be minimized and it should therefore be especially interesting for decentralized control.
|
|
|
|
In this section, we wish to see if the cubic architecture has indeed some interesting properties related to decentralized control in the frame of the struts.
|
|
|
|
Here two sensors integrated in the struts are considered: a displacement sensor and a force sensor.
|
|
The control architecture is shown in Figure \ref{fig:detail_kinematics_decentralized_control} where \(\bm{K}_{\mathcal{L}}\) is a diagonal transfer function matrix.
|
|
|
|
\begin{figure}[htbp]
|
|
\centering
|
|
\includegraphics[scale=1]{figs/detail_kinematics_decentralized_control.png}
|
|
\caption{\label{fig:detail_kinematics_decentralized_control}From Strut coordinate to Cartesian coordinate using the Jacobian matrix}
|
|
\end{figure}
|
|
|
|
The ``strut plant'' are compared for two Stewart platforms:
|
|
\begin{itemize}
|
|
\item with cubic architecture shown in Figure \ref{fig:detail_kinematics_cubic_payload} (page \pageref{fig:detail_kinematics_cubic_payload})
|
|
\item with a Stewart platform shown in Figure \ref{fig:detail_kinematics_non_cubic_payload}. It has the same payload and strut dynamics than for the cubic architecture.
|
|
The struts are oriented more vertically to be far away from the cubic architecture
|
|
\end{itemize}
|
|
|
|
\begin{figure}[htbp]
|
|
\centering
|
|
\includegraphics[scale=1,width=0.6\linewidth]{figs/detail_kinematics_non_cubic_payload.png}
|
|
\caption{\label{fig:detail_kinematics_non_cubic_payload}Stewart platform with non-cubic architecture}
|
|
\end{figure}
|
|
\paragraph{Relative Displacement Sensors}
|
|
|
|
The transfer functions from actuator force included in each strut to the relative motion of the struts are shown in Figure \ref{fig:detail_kinematics_decentralized_dL}.
|
|
As expected from the equations of motion from \(\bm{f}\) to \(\bm{\mathcal{L}}\) \eqref{eq:nhexa_transfer_function_struts}, the \(6 \times 6\) plants are decoupled at low frequency.
|
|
|
|
At high frequency, the plant is coupled as the mass matrix projected in the frame of the struts is not diagonal.
|
|
|
|
No clear advantage can be seen for the cubic architecture (figure \ref{fig:detail_kinematics_cubic_decentralized_dL}) as compared to the non-cubic architecture (Figure \ref{fig:detail_kinematics_non_cubic_decentralized_dL}).
|
|
|
|
Note that the resonance frequencies are not the same in both cases as having the struts oriented more vertically changed the stiffness properties of the Stewart platform and hence the frequency of different modes.
|
|
|
|
\begin{figure}[htbp]
|
|
\begin{subfigure}{0.48\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_non_cubic_decentralized_dL.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_non_cubic_decentralized_dL}Non cubic architecture}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.48\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_cubic_decentralized_dL.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_decentralized_dL}Cubic architecture}
|
|
\end{subfigure}
|
|
\caption{\label{fig:detail_kinematics_decentralized_dL}Bode plot of the transfer functions from actuator force to relative displacement sensor in each strut. Both for a non-cubic architecture (\subref{fig:detail_kinematics_non_cubic_decentralized_dL}) and for a cubic architecture (\subref{fig:detail_kinematics_cubic_decentralized_dL})}
|
|
\end{figure}
|
|
|
|
\paragraph{Force Sensors}
|
|
|
|
Similarly, the transfer functions from actuator force to force sensors included in each strut are extracted both for the cubic and non-cubic Stewart platforms.
|
|
The results are shown in Figure \ref{fig:detail_kinematics_decentralized_fn}.
|
|
|
|
The system is well decoupled at high frequency in both cases.
|
|
There are no evidence of an advantage of the cubic architecture.
|
|
|
|
\begin{figure}[htbp]
|
|
\begin{subfigure}{0.48\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_non_cubic_decentralized_fn.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_non_cubic_decentralized_fn}Non cubic architecture}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.48\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.95\linewidth]{figs/detail_kinematics_cubic_decentralized_fn.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_decentralized_fn}Cubic architecture}
|
|
\end{subfigure}
|
|
\caption{\label{fig:detail_kinematics_decentralized_fn}Bode plot of the transfer functions from actuator force to force sensor in each strut. Both for a non-cubic architecture (\subref{fig:detail_kinematics_non_cubic_decentralized_fn}) and for a cubic architecture (\subref{fig:detail_kinematics_cubic_decentralized_fn})}
|
|
\end{figure}
|
|
|
|
\paragraph{Conclusion}
|
|
|
|
The Cubic architecture seems to not have any significant effect on the coupling between actuator and sensors of each strut and thus provides no advantages for decentralized control.
|
|
No evidence of specific advantages of the cubic architecture for decentralized control has been found in the literature, despite many claims.
|
|
|
|
\section{Cubic architecture with Cube's center above the top platform}
|
|
\label{ssec:detail_kinematics_cubic_design}
|
|
As was shown in Section \ref{ssec:detail_kinematics_cubic_dynamic}, the cubic architecture can have very interesting dynamical properties when the center of mass of the moving body is at the cube's center.
|
|
|
|
This is because, both the mass and stiffness matrices are diagonal.
|
|
As shown in in section \ref{ssec:detail_kinematics_cubic_static}, the stiffness matrix is diagonal when the considered B frame is located at the cube's center.
|
|
|
|
Or, typically the \(\{B\}\) frame is taken above the top platform where forces are applied and where displacements are expressed.
|
|
|
|
In this section, modifications of the Cubic architectures are proposed in order to be able to have the payload above the top platform while still benefiting from interesting dynamical properties of the cubic architecture.
|
|
|
|
There are three key parameters for the geometry of the Cubic Stewart platform:
|
|
\begin{itemize}
|
|
\item \(H\) height of the Stewart platform (distance from fix base to mobile platform)
|
|
\item \(H_c\) height of the cube, as shown in Figure \ref{fig:detail_kinematics_cubic_schematic_full}
|
|
\item \(H_{CoM}\) height of the center of mass with respect to the mobile platform. It is also the cube's center.
|
|
\end{itemize}
|
|
|
|
Depending on the considered cube's size \(H_c\) compared to \(H\) and \(H_{CoM}\), different designs are obtained.
|
|
|
|
In the three examples shows bellow, \(H = 100\,mm\) and \(H_{CoM} = 20\,mm\).
|
|
\paragraph{Small cube}
|
|
|
|
When the considered cube size \(H_c\) is smaller than twice the height of the CoM \(H_{CoM}\), the obtained design looks like Figure \ref{fig:detail_kinematics_cubic_above_small}.
|
|
|
|
\begin{equation}\label{eq:detail_kinematics_cube_small}
|
|
H_c < 2 H_{CoM}
|
|
\end{equation}
|
|
|
|
This is similar to \cite{furutani04_nanom_cuttin_machin_using_stewar}, even though it is not mentioned that the system has a cubic configuration.
|
|
Adjacent struts are parallel to each other, which is quite different from the typical architecture in which parallel struts are opposite to each other.
|
|
|
|
This lead to a compact architecture, but as the cube's size is small, the rotational stiffness may be too low.
|
|
|
|
\begin{figure}[htbp]
|
|
\begin{subfigure}{0.36\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.9\linewidth]{figs/detail_kinematics_cubic_above_small_iso.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_above_small_iso}Isometric view}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.30\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.9\linewidth]{figs/detail_kinematics_cubic_above_small_side.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_above_small_side}Side view}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.30\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.9\linewidth]{figs/detail_kinematics_cubic_above_small_top.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_above_small_top}Top view}
|
|
\end{subfigure}
|
|
\caption{\label{fig:detail_kinematics_cubic_above_small}Cubic architecture with cube's center above the top platform. A cube height of 40mm is used.}
|
|
\end{figure}
|
|
|
|
\paragraph{Medium sized cube}
|
|
|
|
Increasing the cube size with an height close to the stewart platform height leads to an architecture in which the struts are crossing.
|
|
|
|
\begin{equation}\label{eq:detail_kinematics_cube_medium}
|
|
2 H_{CoM} < H_c < 2 (H_{CoM} + H)
|
|
\end{equation}
|
|
|
|
This is similar to \cite{yang19_dynam_model_decoup_contr_flexib} (Figure \ref{fig:detail_kinematics_yang19} in page \pageref{fig:detail_kinematics_yang19}), even though it is not cubic (but the struts are crossing).
|
|
|
|
\begin{figure}[htbp]
|
|
\begin{subfigure}{0.36\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.9\linewidth]{figs/detail_kinematics_cubic_above_medium_iso.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_above_medium_iso}Isometric view}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.30\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.9\linewidth]{figs/detail_kinematics_cubic_above_medium_side.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_above_medium_side}Side view}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.30\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.9\linewidth]{figs/detail_kinematics_cubic_above_medium_top.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_above_medium_top}Top view}
|
|
\end{subfigure}
|
|
\caption{\label{fig:detail_kinematics_cubic_above_medium}Cubic architecture with cube's center above the top platform. A cube height of 140mm is used.}
|
|
\end{figure}
|
|
|
|
\paragraph{Large cube}
|
|
|
|
When the cube's height is more than twice the platform height added to the CoM height, the architecture shown in Figure \ref{fig:detail_kinematics_cubic_above_large} is obtained.
|
|
|
|
\begin{equation}\label{eq:detail_kinematics_cube_large}
|
|
2 (H_{CoM} + H) < H_c
|
|
\end{equation}
|
|
|
|
\begin{figure}[htbp]
|
|
\begin{subfigure}{0.36\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.9\linewidth]{figs/detail_kinematics_cubic_above_large_iso.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_above_large_iso}Isometric view}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.30\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.9\linewidth]{figs/detail_kinematics_cubic_above_large_side.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_above_large_side}Side view}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.30\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,width=0.9\linewidth]{figs/detail_kinematics_cubic_above_large_top.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_cubic_above_large_top}Top view}
|
|
\end{subfigure}
|
|
\caption{\label{fig:detail_kinematics_cubic_above_large}Cubic architecture with cube's center above the top platform. A cube height of 240mm is used.}
|
|
\end{figure}
|
|
|
|
\paragraph{Platform size}
|
|
|
|
The top joints \(\bm{b}_i\) are located on a circle with radius \(R_{b_i}\) \eqref{eq:detail_kinematics_cube_top_joints}.
|
|
The bottom joints \(\bm{a}_i\) are located on a circle with radius \(R_{a_i}\) \eqref{eq:detail_kinematics_cube_bot_joints}.
|
|
|
|
\begin{subequations}\label{eq:detail_kinematics_cube_joints}
|
|
\begin{align}
|
|
R_{b_i} &= \sqrt{\frac{3}{2} H_c^2 + 2 H_{CoM}^2} \label{eq:detail_kinematics_cube_top_joints} \\
|
|
R_{a_i} &= \sqrt{\frac{3}{2} H_c^2 + 2 (H_{CoM} + H)^2} \label{eq:detail_kinematics_cube_bot_joints}
|
|
\end{align}
|
|
\end{subequations}
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The size of the platforms increase with the cube's size and the height of the location of the center of mass (also coincident with the cube's center).
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The size of the bottom platform also increases with the height of the Stewart platform.
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As the rotational stiffness for the cubic architecture is scaled as the square of the cube's height \eqref{eq:detail_kinematics_cubic_stiffness}, the cube's size can be determined from the requirements in terms of rotational stiffness.
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Then, using \eqref{eq:detail_kinematics_cube_joints}, the size of the top and bottom platforms can be determined.
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\paragraph{Conclusion}
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For each of the proposed configuration, the Stiffness matrix is diagonal with \(k_x = k_y = k_y = 2k\) with \(k\) is the stiffness of each strut.
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However, the rotational stiffnesses are increasing with the cube's size but the required size of the platform is also increasing, so there is a trade-off here.
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We found that we can have a diagonal stiffness matrix using the cubic architecture when \(\{A\}\) and \(\{B\}\) are located above the top platform.
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Depending on the cube's size, 3 different configurations were obtained.
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\section*{Conclusion}
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Cubic architecture can be interesting when specific payloads are being used.
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In that case, the center of mass of the payload should be placed at the center of the cube.
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For the classical cubic architecture, it is often not possible.
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Architectures with the center of the cube about the top platform are proposed to overcome this issue.
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This study was necessary to determine if the Cubic configuration has specific properties that would be interesting for the nano-hexapod.
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During this study, it was found that some properties attributed to the cubic configuration (such as uniform mobility and natural decoupling between the struts) were not verified or require more nuances than typically done.
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\chapter{Nano Hexapod}
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\label{sec:detail_kinematics_nano_hexapod}
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For the NASS, the chosen frame \(\{A\}\) and \(\{B\}\) coincide with the sample's point of interest, which is \(150\,mm\) above the top platform.
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This is where we want to control the sample's position.
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Requirements:
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\begin{itemize}
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\item The nano-hexapod should fit within a cylinder with radius of \(120\,mm\) and with a height of \(95\,mm\).
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\item Based on the measured errors of all the stages of the micro-stations, the required mobility of the nano-hexapod should be (with some safety margins):
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It should be able to perform combined translation in any direction of +/-50um.
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At any position, it should be able to perform Rx and Ry rotations of +/-50urad
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\item In terms of stiffness:
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Having the resonance frequencies well above the maximum rotational velocity of \(2\pi\,\text{rad/s}\) to limit the gyroscopic effects.
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Having the resonance below the problematic modes of the micro-station to decouple from the micro-station complex dynamics.
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\item In terms of dynamics:
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|
\begin{itemize}
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\item Be able to apply IFF in a decentralized way with good robustness and performances (good damping of modes)
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\item Having good decoupling for the High authority controller
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\end{itemize}
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\end{itemize}
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|
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The main difficulty for the design optimization of the nano-hexapod, is that the payloads will have various inertia, with masses ranging from 1 to 50kg.
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It is therefore not possible to have one geometry that gives good dynamical properties for all the payloads.
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|
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It could have been an option to have a cubic architecture as proposed in section \ref{ssec:detail_kinematics_cubic_design}, but having the cube's center 150mm above the top platform would have lead to platforms well exceeding the maximum available size.
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In that case, each payload would have to be calibrated in inertia before placing on top of the nano-hexapod, which would require a lot of work from the future users.
|
|
|
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Considering the fact that it would not be possible to have the center of mass at the cube's center, the cubic architecture was considered not interesting for the nano-hexapod.
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\section{Obtained Geometry}
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\label{ssec:detail_kinematics_nano_hexapod_geometry}
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|
|
|
Based on previous analysis:
|
|
\begin{itemize}
|
|
\item The geometry can be optimized to have the wanted trade-off between stiffness in different directions and mobility in different directions
|
|
\item But as the payloads will be so different in terms of inertia, it was found difficult to optimize the geometry so that the wanted dynamical properties of the nano-hexapod are obtained for all the payloads.
|
|
\end{itemize}
|
|
|
|
Therefore, the geometry was chosen by:
|
|
\begin{itemize}
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\item Height between the two plates is 95mm
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\item Taking both platforms with the maximum size available:
|
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Joints are offset by 15mm from the plate surfaces, and are positioned along a circle with radius 120mm for the fixed joints and 110mm for the mobile joints.
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|
\item Make reasonable choice of the angles of the struts.
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|
The positioning angles (Figure \ref{fig:detail_kinematics_nano_hexapod_top}) are \([255, 285, 15, 45, 135, 165]\) degrees for the top joints and \([220, 320, 340, 80, 100, 200]\) degrees for the bottom joints.
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|
\end{itemize}
|
|
|
|
Obtained geometry is shown in Figure \ref{fig:detail_kinematics_nano_hexapod}.
|
|
The geometry will be slightly refined during the detailed mechanical design for several reason: easy of mount, manufacturability, \ldots{} but will stay close to the defined geometry.
|
|
|
|
This geometry will be used for:
|
|
\begin{itemize}
|
|
\item Estimate required actuator stroke (Section \ref{ssec:detail_kinematics_nano_hexapod_actuator_stroke})
|
|
\item Estimate flexible joint stroke (Section \ref{ssec:detail_kinematics_nano_hexapod_joint_stroke})
|
|
\item When performing noise budgeting for the choice of instrumentation
|
|
\item For control purposes
|
|
\end{itemize}
|
|
|
|
\begin{figure}[htbp]
|
|
\begin{subfigure}{0.48\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,scale=1]{figs/detail_kinematics_nano_hexapod_iso.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_nano_hexapod_iso}Isometric view}
|
|
\end{subfigure}
|
|
\begin{subfigure}{0.48\textwidth}
|
|
\begin{center}
|
|
\includegraphics[scale=1,scale=1]{figs/detail_kinematics_nano_hexapod_top.png}
|
|
\end{center}
|
|
\subcaption{\label{fig:detail_kinematics_nano_hexapod_top}Top view}
|
|
\end{subfigure}
|
|
\caption{\label{fig:detail_kinematics_nano_hexapod}Obtained architecture for the Nano Hexapod}
|
|
\end{figure}
|
|
|
|
\section{Required Actuator stroke}
|
|
\label{ssec:detail_kinematics_nano_hexapod_actuator_stroke}
|
|
|
|
Now that the geometry is fixed, the required actuator stroke to have the wanted mobility can be computed.
|
|
|
|
Wanted mobility:
|
|
\begin{itemize}
|
|
\item Combined translations in the xyz directions of +/-50um (basically ``cube'')
|
|
\item At any point of the cube, be able to do combined Rx and Ry rotations of +/-50urad
|
|
\item Rz is always at 0
|
|
\item Say that it is frame B with respect to frame A, but it is motion expressed at the point of interest (at the focus point of the light)
|
|
\end{itemize}
|
|
|
|
First the minimum actuator stroke to have the wanted mobility is computed.
|
|
With the chosen geometry, an actuator stroke of +/-94um is found.
|
|
|
|
Considering combined rotations and translations, the wanted mobility and the obtained mobility of the Nano hexapod are shown in Figure \ldots{}
|
|
|
|
It can be seen that just wanted mobility (displayed as a cube), just fits inside the obtained mobility.
|
|
Here the worst case scenario is considered, meaning that whatever the angular position in Rx and Ry (in the range +/-50urad), the top platform can be positioned anywhere inside the cube.
|
|
|
|
\begin{figure}[htbp]
|
|
\centering
|
|
\includegraphics[scale=1]{figs/detail_kinematics_nano_hexapod_mobility.png}
|
|
\caption{\label{fig:detail_kinematics_nano_hexapod_mobility}Wanted translation mobility of the Nano-Hexapod and computed Mobility}
|
|
\end{figure}
|
|
|
|
Therefore, in Section \ldots{}, the specification for actuator stroke is +/-100um
|
|
|
|
\section{Required Joint angular stroke}
|
|
\label{ssec:detail_kinematics_nano_hexapod_joint_stroke}
|
|
|
|
Now that the mobility of the Stewart platform is know, the corresponding flexible joint stroke can be estimated.
|
|
|
|
\begin{itemize}
|
|
\item conclude on the required joint angle: 1mrad?
|
|
Will be used to design flexible joints.
|
|
\end{itemize}
|
|
|
|
\chapter{Conclusion}
|
|
\label{sec:detail_kinematics_conclusion}
|
|
|
|
Inertia used for experiments will be very broad => difficult to optimize the dynamics
|
|
Specific geometry is not found to have a huge impact on performances.
|
|
Practical implementation is important.
|
|
|
|
Geometry impacts the static and dynamical characteristics of the Stewart platform.
|
|
Considering the design constrains, the slight change of geometry will not significantly impact the obtained results.
|
|
|
|
\printbibliography[heading=bibintoc,title={Bibliography}]
|
|
\end{document}
|